Bearing Design Analysis Apparatus and Method

The details of the invention will be described in connection with the accompanying drawings, in which:

FIG. 1A is a side view of a tilting pad bearing according to the present invention;

FIG. 1B is a side view of another tilting pad bearing according to the present invention;

FIG. 1C is a side view of a hydrodynamic bearing according to the present invention;

FIG. 1D is a side view of one tilt supported bearing pad showing the tilting of the pad under load;

FIG. 1E is a side view of a pad of a prior art tilt pad bearing;

FIG. 2 is a schematic view of a single pad made in accordance with the example illustrated in FIG. 1;

FIG. 2A is a sectional view of a journal bearing illustrating a sector thereof embodying one form of the invention;

FIG. 3 is an edge view of the pad of FIG. 2 illustrating the pad orientation with the support structure in the loaded state;

FIG. 4 is a sectional view of a sector of a second example of a journal bearing made in accordance with the present invention;

FIG. 5 is a view partly in section of a single pad of FIG. 4;

FIG. 5A is a perspective view of a section of a modified form of the bearing of FIG. 4;

FIG. 5B is a perspective view of a modified form of the bearing shown in FIG. 4;

FIG. 6 is an end view of the bearing of FIG. 4;

FIG. 7 is a diagrammatic view of the torsional movement of a beam, greatly enlarged;

FIG. 8 is a sectional view of a journal bearing illustrating an example of a bearing incorporating the features of the present invention which includes two beams;

FIG. 9 is an edge view of the pad of FIG. 1 illustrating local movement of the pad surface without support structure movement, greatly exaggerated;

FIG. 10 is an edge view of the pad of FIG. 8 illustrating the pad orientation with the support structure in the loaded state.

FIG. 10A is an edge view of the pad of FIG. 8 illustrating local movement of the pad surface greatly exaggerated.

FIGS. 11A and 11B are cross sectional views of a cylindrical journal or blank prior to machining;

FIGS. 12A and 12B are cross sectional views of a machined journal or blank;

FIGS. 13A and 13B are cross-sectional views of a further machined journal or blank;

FIGS. 14A and 14B are cross sectional views of a modified machined journal or blank; and

FIGS. 14C and 14D are cross sectional views of a bearing constructed from the modified machined journal or blank of FIGS. 14A and 14B.

FIG. 15 is a top view of a thrust bearing having beam mounted bearing pads.

FIG. 16 is a side cross section of the thrust bearing of FIG. 15.

FIG. 17 is a bottom view of the thrust bearing of FIG. 15.

FIG. 18 is a perspective view of a portion of the thrust bearing of FIG. 15.

FIG. 19 is a top view of a prior art thrust bearing.

FIG. 20 is a cross-section of the prior art thrust bearing of FIG. 19.

FIG. 20A is a schematic representation of a segment of the prior art thrust bearing of FIGS. 19 and 20 showing the pressure distribution across the surface of a bearing pad.

FIG. 21 is a top view of a thrust bearing according to the present invention having two legged support.

FIG. 22 is a side cross-section of the thrust bearing of FIG. 21.

FIG. 23 is a bottom view of the bearing of FIG. 21.

FIG. 23A is a bottom view of a modified version of the bearing of FIG. 21.

FIG. 24 is a perspective view of a segment of the bearing of FIG. 21.

FIG. 25 is a cross-section of another bearing according to the present invention.

FIG. 26 is a cross-section of another bearing according to the present invention.

FIG. 27 is a side cross-section of another bearing construction according to the present invention.

FIG. 28 is a top cross-section of the bearing construction of FIG. 27.

FIG. 29 is a side cross-section of another bearing construction according to the present invention,

FIG. 29A is a cross-section of another thrust bearing construction according to the present invention.

FIG. 29B is a cross-section along the lines indicated in FIG. 30B.

FIG. 30 is a top cross-section of the bearing construction of FIG. 29.

FIG. 30A is a top view of the bearing of FIG. 29A.

FIG. 30B is a bottom view of the bearing of FIG. 29A.

FIG. 31 is a side view of another journal bearing construction in accordance with the present invention.

FIG. 31A is a radial cross-section of a portion of the bearing illustrated in FIG. 31.

FIG. 32 is a side view of another journal bearing construction in accordance with the present invention.

FIG. 32A is a radial cross-section of the bearing of FIG. 32.

FIG. 32B is a perspective view of the bearing of FIG. 32.

FIG. 33 is a side view of another journal bearing construction in accordance with the present invention.

FIG. 33A is a detail of a portion of the outer periphery of the bearing of FIG. 33.

FIG. 33B is a cross-section of the bearing of FIG. 33.

FIG. 33C is another cross section of the bearing of FIG. 33.

FIG. 24 is a side view of another journal bearing according to the present invention.

FIG. 34A is a detail of a portion of the outer periphery of the bearing of FIG. 34.

FIG. 34B is a cross-section of the bearing of FIG. 34.

FIG. 34C is another cross-section of the bearing of FIG. 34.

FIG. 34D is another cross-section of the bearing of FIG. 34.

FIG. 35 is a side view of a combined radial and thrust bearing according to the present invention.

FIG. 35A is a cross-section of the bearing of FIG. 35.

FIG. 35B is another cross-section of the bearing of FIG. 35.

FIG. 36 is a side view of another combined radial and thrust bearing according to the present invention.

FIG. 37 is a diagrammatic cross-section of the bearing of FIG. 36 illustrating the forces acting on the bearing pad.

FIG. 38A is a top view of an easily moldable thrust bearing according to the present invention.

FIG. 38B is a bottom view of the bearing of FIG. 38A.

FIG. 38C is an exploded cross-section along the lines indicated in FIG. 38A.

FIG. 38D is a bottom view illustrating modifications of the bearing illustrated in FIGS. 38A-C.

FIG. 39A is a top view of another easily moldable thrust bearing according to the present invention.

FIG. 39B is a bottom view of the bearing of FIG. 39A.

FIG. 39C is a partial cross-section showing the support structure for the bearing pads in the bearing of FIGS. 39A and 39B.

FIG. 40 is a side view of a self-lubricating bearing according to the present invention.

FIG. 40A is a cross-section of the bearing of FIG. 40.

FIG. 41 is a side view of a self-lubricating combined radial and thrust bearing according to the present invention.

FIG. 41A is a cross-section of the bearing of FIG. 41.

FIG. 42A is a perspective view of a sector shaped thrust pad with arrows indicating the side lines for the top side and edge views.

FIG. 42B is a perspective view of a journal bearing pad with arrows indicating the side lines for a top edge and side view.

FIG. 42C is a perspective view of a combined radial/thrust bearing pad with arrows indicating the side lines for a top, side and edge view.

FIG. 42D is a perspective view of a circular thrust pad.

FIG. 43A is a top view of a thrust pad provided with radius cuts on both edges.

FIG. 43B is a side view of a journal bearing pad with radius cuts formed on both edges.

FIG. 43C is a top view of the journal bearing pad of FIG. 43B.

FIG. 43D is an edge view of a combined radial/thrust bearing/pad having radius cuts formed on both edges thereof.

FIG. 43E is a top view of the combined radial/thrust bearing pad of FIG. 43D.

FIG. 44A is a side view of a thrust pad with tapered edges.

FIG. 44B is a side view of a journal bearing pad with tapered edges.

FIG. 44C is a side view of a combined radial/thrust bearing pad with tapered side edges.

FIG. 44D is a side view of the combined radial/thrust bearing pad of FIG. 44C.

FIG. 45A is an edge view of a thrust pad provided with side edge rails.

FIG. 45B is an edge perspective view of a journal or radial bearing pad provided with side edge rails on its axial edges.

FIG. 45C is an edge view of a combined radial/thrust bearing pad provided with side edge rails.

FIG. 46A is a side view of a thrust bearing pad having grooves formed in the bottom proximate the side edges.

FIG. 46B is a side view of a radial or journal bearing pad having grooves formed in the bottom proximate the sides.

FIG. 46C is a side view of a combined radial/thrust bearing pad having grooves formed in the bottom proximate the side edges.

FIG. 47A is a top view of a thrust bearing in which the individual pads are defined by pad defining grooves.

FIG. 47B is a sectional view of the thrust bearing of FIG. 47A along the lines indicated in FIG. 47A.

FIG. 47C is a side view of a radial or journal bearing in which the individual pads are defined by pad defining grooves.

FIG. 48A is a top view of a thrust bearing pad formed with a bottom access indicated in phantom.

FIG. 48B shows a side view of the thrust bearing pad of FIG. 48A.

FIG. 48C shows a side view of a radial bearing pad formed with a bottom recess indicated in phantom.

FIG. 49A is a top view of a thrust bearing pad formed with a bottom recess on each edge indicated in phantom.

FIG. 49B is a side view of the thrust bearing pad of FIG. 49A with the bottom recesses indicated in phantom.

FIG. 49C is a side view of a radial or journal bearing pad with bottom recesses formed proximate each edge as indicated in phantom.

FIG. 50A is a top view of a thrust or combined radial/thrust bearing.

FIG. 50B is a bottom view of the thrust bearing or combined radial/thrust bearing of FIG. 50A.

FIG. 50C is a cross-section through the lines indicated in FIG. 50A.

FIG. 51A is a top view of a bearing pad for a radial bearing.

FIG. 51B is a side view of the bearing pad of FIG. 51A.

FIG. 51C is a bottom view of the bearing pad of FIG. 51A.

FIG. 52A is a bottom view of a thrust bearing according to the present invention.

FIG. 52B is a partial sectional view of the thrust bearing of FIG. 52A along the lines indicated in FIG. 52A.

FIG. 52C is a top view of the thrust bearing of FIG. 52A.

FIG. 53A is a side view, partially in section, of a self-adjusting continuous combined radial/thrust bearing arrangement according to the present invention.

FIG. 53B is a somewhat schematic perspective view showing the relationship of the bearing to the shaft and runner of the combined radial/thrust bearing arrangement of FIG. 53A.

FIG. 53C is a side view, partially in section, of another continuous self-adjusting combined radial/thrust bearing arrangement according to the present invention.

FIG. 53D is a somewhat schematic perspective view showing the relationship between the shaft and runner and the combined radial/thrust bearing of FIG. 53C.

FIG. 54A shows a cantilever beam having three nodes according to one embodiment of the present invention.

FIG. 54B illustrates the movement of the cantilever beam of FIG. 54A due to the application of 1 lb.sub.f at Node 1.

FIG. 54C illustrates the movement of the cantilever beam of FIG. 54A due to the application of 1 lb.sub.f at Node 2.

FIG. 54D illustrates the application of 2 lb.sub.f at Node 1 and 5 lb.sub.f at Node 2 of the cantilever beam of FIG. 54A.

FIG. 55 is a flow chart corresponding to a RADIAL module used to analyze radial bearings according to one embodiment of the present invention.

FIG. 56 is a flow chart corresponding to a DEFPAD module to be used in conjunction with the RADIAL module of FIG. 55.

FIG. 57 is a flow chart corresponding to a THRUST module used to analyze thrust bearings according to one embodiment of the present invention.

FIG. 58 is a flow chart corresponding to a PAD module to be used in conjunction with the THRUST module of FIG. 57.

FIG. 59 is a plot of the principle and cross-coupling stiffness coefficients as a function of pad tilt stiffness and web thickness for a four-pad movable-pad bearing similar to that shown in FIG. 1A.

FIG. 60 is a plot of logarithmic decrement as a function of pad tilt stiffness and web thickness for a four-pad movable-pad bearing similar to that shown in FIG. 1A.

FIG. 61 is a schematic representation of a high-speed double-overhung air-driven turbocompressor.

FIG. 62 is a cross-section of a rotor model used for rotordynamic analysis of the turbocompressor shown in FIG. 61.

FIG. 63 illustrates the computed undamped mode 6 rates shapes based on the rotor model of FIG. 62.

FIG. 64 is a plot of critical speed as a function of support stiffness based on the rotor model of FIG. 62; also shown is a plot of the frequency-dependent support stiffness of a three-pad bearing like that shown in FIG. 1C.

FIG. 65 is a plot of the first mode log decrement for the rotor model of FIG. 62 as a function of web thickness and pad tilt stiffness.

FIG. 66 is a plot of the second mode log decrement for the rotor model of FIG. 62 as a function of web thickness and pad tilt stiffness.

FIG. 67 is a schematic diagram illustrating the maximum possible pad movement when the bearing shaft is forced between two pads.

FIG. 68 is an illustration of the key points and line segments that are selected for FEA according to the present invention.

The present invention is directed to a method of designing movable pad type hydrodynamic bearings and an apparatus for use therein. The bearings are preferably unitary and include pad support structures formed integrally as a single piece with the pads.

As discussed in detail below, the position of such a bearing pads under load is governed by the geometry of the pad support structure and the mechanical properties of the bearing material. According to one aspect of the invention, the support structure may be modeled as a linear spring by using the spring equation, F=KX, there F is the applied force, X is the extent of movement, and K is the spring constant having units of force per unit length. Alternatively, this relationship can be expressed as X=.alpha.F, where .alpha., the influence coefficient, is the inverse of K and has units of length per unit force.

This equation is used in conjunction with finite element analysis to determine the influence coefficients for a given support structure. For example, in order to generate the influence coefficients, a finite element model of the structure is first generated and unit loads are applied to all or a number of nodes on the surface of the bearing, one node at a time. Although only the movements of the surface nodes are needed to determine the bearing profile, the resulting node movements of the entire support structure are calculated in a known manner using FEA. The surface movements due to the application of the unit loads at each node are stored and assembled to form an N.times.N matrix, where N is the number of nodes on the bearing surface.

This matrix, called the influence coefficient matrix, .alpha., provides an indication of how the bearing will move under given loads through the equation X=.alpha.F where X is the displacement vector and F is the force vector. The matrix may be arranged such that the rows correspond to individual loads and the columns correspond to particular nodes, or vice versa. In this way, the movement of each node due to each unit load is represented in the matrix.

Once the influence coefficient matrix is generated, the movements of the support structure due to any load distribution may be determined by performing a simple matrix multiplication. This method allows rapid analysis of an infinite number of operating conditions without using FEA for each movement calculation and, compared with other methods, significantly reduces the amount of time necessary to obtain the desired result.

This procedure is illustrated in FIGS. 54A to 54D using a simple cantilever beam model with 3 surface nodes. As shown in FIG. 54B, the application of a unit load at node 1 causes movement of the cantilever beam. In this example, the movement at node 1 due to a unit load at node 1, is 4. Similarly, the movement at node 2, due to the unit load at node 1, is 3. This result is summarized as follows:

The application of a unit load at node 2, as illustrated in FIG. 54C, indicates that the movement at node 1 is 2 and the movement at node 2 is 1, i.e.,

From this data, an influence coefficient matrix .alpha. can be generated such as that shown below: ##EQU1## Note that loads applied at node 3 in this example yield no movement by definition of a cantilever beam. Once the influence coefficient matrix .alpha. a is generated, it can be used as shown in the example of FIG. 54D. In FIG. 54D, it is shown that when there is a two-unit load at node 1 and a five-unit load at node 2, according to the equation X=.alpha.F, the matrix can be easily calculated to solve for displacement X1 and X2, as shown below. ##EQU2##

Therefore, a two-unit load at node 1 and a five-unit load at node 2 results in movements at these nodes of 18 and 11, respectively. In practice, more than two nodes would be sampled. For example, on the order of 29 nodes per surface may be desired for greater accuracy. The calculation of the 29.times.29 matrix that is generated as a result of such a process can be easily handled by a simple computer.

As illustrated in the RADIAL module flow chart of FIG. 55, the radial bearing analysis technique of the present invention involves the following steps. First, the operating conditions are identified. The operating conditions may include load, speed, temperature, geometry, lubricant properties and other known conditions and parameters. A range of acceptable performance characteristics is also identified for evaluating the performance of the bearing.

Preferably, acceptable rotordynamic performance characteristics are predetermined or set out in technical specifications such as, for example, the API (American Petroleum Institute) specifications. These specifications are readily available and widely used to identify standards of acceptable behavior.

A bearing model is then designed, typically using engineering judgment, based on the specified conditions. A rotor model is then constructed from the bearing model by dividing the rotor into sections (based on geometry) and replacing the bearings and seals with springs and dampers at the appropriate sections. It may also be desirable to include other effects to provide a more complete model of the system as will be apparent to one of ordinary skill in the art. An initial rotordynamics analysis of the rotor is then conducted using transfer matrices to determine undamped critical speed maps and mode shapes of the rotor. Undamped critical speed maps are plots of rotor natural frequencies v. support stiffness. Mode shapes are normalized shapes assumed by the rotor as it passes through natural frequencies for a specific support stiffness.

If the undamped critical speed maps and mode shapes are unacceptable, the bearing pads or support structure configuration is modified. As discussed below, this is currently performed using engineering judgment, but expert system approaches are also contemplated. If the undamped critical speed maps and mode shapes are acceptable for the operating frequency of interest, the bearing design is then implemented, for example, using computer aided design (CAD). The CAD may, for example, use CADKEY, a well known CAD program, to produce a two-dimensional (or three-dimensional) wire frame model of the bearing design, or part of the bearing design, in a known manner. The bearing design is then translated from CAD to a format compatible with finite element analysis (FEA) by creating key points and line segments from the wire frame model using a known CAD to FEA translator. Alternatively, the bearing design can be directly implemented in the finite element program, without the use of CAD. Nodes and elements are then defined and appropriate boundary conditions applied. FEA is performed (e.g., using a commercially available finite element package such as ANSYS) to generate influence coefficients which may be used to characterize support structure stiffness. The influence coefficients e are generated, assembled in a matrix and stored in the manner described above in connection with FIGS. 54A-54D.

Once the influence coefficient matrix, .alpha., is generated, a radial bearing analysis is begun, for example, using a radial bearing program (such as the DEFPAD module summarized in FIG. 56).

Once the DEFPAD module is called, key data are inputted from the RADIAL module. An initial shaft position, or eccentricity, is then selected, either manually or based on a computer generated determination. It is generally preferred that the initial shaft position be selected in the correct quadrant to minimize calculation time. If this step is automated, the factors taken into consideration include the magnitude and direction of the load. Based on these factors, the correct quadrant for the shaft position is usually obtainable.

The Reynolds equation (a second-order, elliptic, non-linear, partial differential equation based on the Navier-Stokes equation) is then solved for the initial shaft position to calculate the pressures in the oil film. One possible form of the Reynolds equation is, e.g., ##EQU3## where h=f(P,x,y) and is the bearing clearance (also referred to as gap size or film thickness), P is the pressure, x and y are distance coordinates (e.g., in the plane of the bearing surface), .mu. is the viscosity and U is the velocity. Of course, other forms of the Reynolds equation are possible and may be based, for example, on radial or spherical coordinate systems. Regardless of the form, the Reynolds equation can be solved by various known numerical methods, including finite differences and finite elements.

Next, the pad movements for the selected shaft position are determined by applying the pressures calculated using the Reynolds equation to the bearing pads in conjunction with the influence coefficient matrix. The pad movements are recalculated and the Reynolds equation is re-solved until convergence is reached. Convergence may be deemed to have occurred, for example, when two successive pad movement calculations are the same, within a specified tolerance. In addition to the pressure distribution and pad movements, solution of the Reynolds equation provides other information such as temperature profiles.

It is then determined whether the equilibrium force (which is calculated by integrating all pressure profiles and determining the magnitude and direction of the resultant force vector) matches the specified external load vectors. If the equilibrium force does not match the predetermined specified load vectors, a new shaft position, or eccentricity, is assumed and the foregoing steps are repeated. In general, if the equilibrium force is too large, it is desirable to move the shaft position closer to the center. Conversely, if the equilibrium force is too small, the shaft should be moved away from the center.

After assuming a new shaft position, pressures and forces are recalculated and it is determined whether the pad movements have converged. If so, a calculation is again made to determine whether the equilibrium force matches the specified load. This procedure is repeated until the selected shaft position yields a calculated equilibrium force substantially equal to the specified load.

Once the equilibrium force for a given shaft position matches the specified load, linearized dynamic bearing coefficients may be calculated. For example, stiffness coefficients can be calculated by applying a position perturbation to determine the resulting change in force. Similarly, damping coefficients may be calculated by applying a velocity perturbation to determine the resulting change in force. The linearized dynamic bearing coefficients may comprise four damping coefficients and four stiffness coefficients.

To further elaborate, the eight coefficients may represent the force in the X direction due to a displacement in the X direction (K.sub.XX), the force in the X direction due to a displacement in the Y direction (K.sub.XY), the force in the Y direction due to a displacement in the X direction (K.sub.YX), the force in the Y direction due to a displacement in the Y direction (K.sub.YY), the force in the X direction due to a velocity in the X direction (D.sub.XX), the force in the X direction due to a velocity in the Y direction (D.sub.XY), the force in the Y direction due to a velocity in the X direction (D.sub.YX), and the force in the Y direction due to a velocity in the Y direction (D.sub.YY).

The DEFPAD module is then complete and the program is returned to the RADIAL module. The linearized dynamic bearing coefficients are then applied to the stations which the bearing occupy in the above-constructed rotor model. This allows the previous rotordynamics analysis (which yielded undamped critical speed maps and mode shapes) to be extended to further include damped analyses (forced response and stability) and a sensitivity study. The sensitivity study ensures that the design is acceptable over the expected range of bearing clearances, bearing preloads, bearing viscosities, etc. Such a comprehensive rotordynamics bearing analysis is used for radial bearing applications in which the dynamics of the rotor-bearing system are important.

The results of all of the above bearing analyses are then considered. If the bearing meets the performance goals (as defined by predetermined criteria), the design is complete. If any of the above analyses should demonstrate that the bearing design is unacceptable, changes such as bearing thickness, bearing width, bearing clearance, bearing length, bearing preload, machined-in pad profiles, offset, number of pads, shape of the pad support structure, support thickness, support width, and support length may be made. Bearing preload, m, is defined as ##EQU4## where C.sub.b is the bearing clearance. C.sub.b and C.sub.p are further defined by C.sub.b =R.sub.b -R.sub.s and C.sub.p =R.sub.p -R.sub.x, where R.sub.s is shaft radius, R.sub.b is the distance from the bearing center to the nearest portion of the pad surface, and R.sub.p is the radius of the pad surface. Offset is the fraction of the arc length of the pad that comprises the convergence length.

As discussed below, these changes are currently implemented using engineering judgment, but automated expert system approaches are also contemplated.

Although certain modifications are necessary, thrust bearings are analyzed in a manner generally similar to the analysis and design of radial bearings.

For example, thrust bearings, like radial bearings, may have a structural compliance which can be modeled using an influence coefficient matrix resulting from the placement of a unit load at user-defined locations (nodes) on the pad surface as discussed above. Determination of influence coefficients for movable pad thrust bearings requires the generation of a three-dimensional model of the pad. Such a three-dimensional model, as described above, may be constructed as a wire frame using computer aided design which may be translated to a finite element program where the influence coefficients are determined. Alternatively, the model can be constructed directly in FEA without the use of CAD.

According to one embodiment of the present analysis technique for thrust bearings, the bearing pad surface is subdivided into a grid pattern of nodes and elements, preferably in two dimensions (e.g., circumferential and radial). The fluid film system of equations is then established for the grid network and boundary conditions (pressurized boundaries, deformation, etc.) are incorporated in the system of equations. A variable grid finite element numerical method is then employed to obtain a solution to the lubrication equations. Film thickness, pressure distribution, deflected pad shape, temperature rise across the pad, oil flow rate and power loss, for example, are determined for a given set of operating conditions. The predicted film pressure distribution is then applied to the finite element bearing model to determine stresses in the support structure. This process is repeated until the bearing design meets the specific goals of the application.

The analysis technique has many capabilities and options including, but not limited to, pad structural compliance (i.e., load induced movement), pad local misalignment, runner-bearing misalignment, variable location angle and radius of pad center, variable axial location of pad surfaces for multiple-pad bearings (i.e., axial offset of the pads), circular pad automatic mesh generation, arc pad (e.g., step or tapered) automatic mesh generation, manual mesh input, heat balance (to satisfy cavity oil temperature), film rupture (to account for cavitation), pressurized boundaries and laminar or turbulent flow conditions.

The thrust bearing analysis technique may be used, e.g., to determine the steady-state performance characteristics of incompressible fluid film thrust bearings. The invention is applicable, but not limited to a wide variety of hydrodynamic fixed and movable-type pad geometry thrust bearings. The thrust bearing analysis technique, according to the present invention, may yield load capacity, viscous power loss, righting moments about pad local orthogonal axes, righting moments about bearing global orthogonal axes, flow requirements, pressure distribution, clearance distribution, spring and damping coefficients, heat balances and other critical information to bearing performance.

The analysis technique is applicable to a wide variety of bearing types including, but not limited to, step-pad, shrouded step-pad, tapered land-pad and shrouded tapered land-pad bearings having arc shapes. This technique is also applicable, but not limited, to circular pad flat surface bearings, circular pad crown-shaped surface bearings, circular pad cone-shaped surface bearings and virtually any other bearing geometry that can be defined using the manual input option of the program. The analysis technique is applicable with various types of runners including, but not limited to, runners having flat surfaces, crown shaped surfaces, cone-shaped surfaces, and surfaces with circumferential waviness.

According to a novel analysis technique of the present invention, a thrust bearing is characterized by the use of a bearing analysis. For example, according to one embodiment of the present invention, a THRUST module as seen in FIG. 57 may be called wherein user specified input data are initially provided. This data may include pad type and local geometry, the number of pads in the bearing, lubricant properties, global pad and runner geometry, orientation/misalignment, shaft/runner local geometry, operating speed, influence coefficients and printout options.

The next step is to define a finite element grid and modify the influence coefficients to a required form. The model can be constructed directly in the finite element program, without the use of CAD. The bearing model is then meshed and appropriate constraints applied. A FEA is then performed to generate influence coefficients which, for example, may characterize support structure stiffness. The influence coefficients are generated, stored and assembled in a matrix in a manner like that described above in connection with FIGS. 54A-54D.

The user may then choose to specify an oil inlet temperature (and iterate to a correct film temperature), or the user may simply choose to begin a temperature loop by directly specifying a film temperature. If the film temperature is not user specified, an initial bulk film temperature must be estimated. This estimated temperature may be, for example, 120% of the oil inlet or bath temperature. In either case, a runner axial position loop is then begun by selecting an initial axial position for the runner.

Next, a pad loop is begun by selecting a pad on the bearing for analysis. Additional pad loops are necessary, for example, if it is desired to calculate the effects of misalignment.

Using either the estimated or the user specified film temperature, a pad analysis is then conducted. For example, as shown in FIG. 58, a PAD module can be called and provided with input data from the THRUST module including the finite element grid, pad and bearing dimensions, influence coefficients, velocity, viscosity, clearance and angular misalignment. Changes in viscosity with film temperature may be taken into consideration, for example, by inputting viscosity information at specified temperatures and fitting a known expression (e.g., a power curve) to the inputted data.

Next, an initial surface configuration is assigned to the pad, usually based on prior experience, to provide an initial clearance distribution. The lubrication equations, including the effects of turbulence (i.e., non-laminar fluid movement) and cavitation (i.e., the rapid formation and collapse of vapor pockets in a flowing liquid in regions of very low pressure), are then solved to yield the pressure distribution in the fluid. The pressure distribution is then integrated to determine the forces and moments associated with the bearing pad. By comparing selected quantities (e.g., moments about x and y axes, integrated force, and movements at user-specified nodes) over two successive iterations, it can be determined whether the convergence criteria have been satisfied.

If convergence is not reached, a new pad surface deformation/movement is calculated based on the influence coefficients of the bearing pad and on the nodal axial forces previously obtained from the calculated pressure. After modifying the pad clearance distribution with the newly calculated pad surface deformation/movement, the deformation iteration loop is repeated until convergence is reached. Once this occurs, power loss and fluid flow are calculated. When the pad analysis is completed, the overall bearing analysis is continued, for example, as shown in the THRUST module in FIG. 57.

At this point, if the film temperature is not specified by the user, a heat balance is conducted. A simple heat balance can be calculated, for example, using the power loss and the fluid flow calculated in the pad analysis. For example, the equation

can be used to calculate the bulk film temperature where .DELTA.T=P/MC.sub.p and where T.sub.film is the film temperature, T.sub.in is the inlet or bath temperature, P is the power loss, M is the mass flow rate of fluid and C.sub.p is the specific heat of the fluid. If this equation does not yield the correct inlet temperature, the temperature loop is repeated using a new value for T.sub.film.

Once the bulk film temperature satisfies the convergence criteria or, alternatively, if the film temperature has been specified by the user, the load is then considered. If the load is not specified, the damping and stiffness coefficients of the bearing are computed by incrementing displacement and velocity and by solving the lubrication equations. If the load is specified, this step is skipped.

Regardless of whether or not the load is specified, pad performance and detailed pad output parameters may then saved and printed based on the output options specified. Output options include, but are not limited to, pressure profile, clearance distribution, minimum film thickness and temperature.

If there are alignment differences between the various pads of the bearing, the pad loop is then repeated for each of the different pads. After completion of all pad loops, the runner position and axial load are stored. Then, if calculations are desired for additional runner positions, the runner axial position loop is repeated.

Once the runner axial position loop is completed, a table of axial loads as a function of the specified clearances may be printed. The total load is calculated by totaling the loads on each of the pads for a specified runner position.

If the load has not been specified and the film temperature has been iteratively solved, rather than user specified, the program is complete.

If the load has not been specified and the film temperature has been user specified, the temperature loop may be repeated for additional film temperatures. When no additional film temperatures are desired, the program is complete.

If the load is specified, regardless of whether the film temperature has been specified by the user or whether it is iteratively solved, the clearances and applied loads generated above may be used to interpolate a value of the clearance for the specified load. For example, the above-specified clearances can be related to the above-generated axial loads by the second-order polynomial,

where R is the runner position, L is a load and A, B and C are coefficients of the equation. Once A, B and C are determined (e.g., by known non-linear least-squares techniques) the runner position R can be directly calculated for the specified load using the above equation.

The bearing problem is then solved for the interpolated clearance that corresponding to the specified load. This is done, for example, as was previously done, by beginning by a pad loop by selecting a pad on the bearing for analysis. The selected pad is then analyzed, for example, by calling and operating the PAD module as described above with respect to FIG. 58.

Once the overall bearing analysis (represented in this example by the THRUST module) is resumed, if the film temperature has not been user specified, a heat balance is conducted and a new bulk temperature calculated as described above. If the heat balance does not yield the proper inlet temperature, the PAD module is run again. Once the heat balance yields the proper inlet temperature, or if the temperature has been user specified, the stiffness and damping coefficients of the bearing at the interpolated clearance are computed as above by incrementing displacement and velocity and solving the lubricating equations.

Detailed pad outputs may then be printed. The information printed includes detailed flows, loads (6 DOF), frictional power losses, film thicknesses, linearized film data, and stiffness and damping matrices.

If calculations are then desired for additional pads (e.g., to calculate the effects of misalignment), the pad loop is repeated until solutions are obtained for each of the pads desired.

Total bearing performance may then be summarized and printed for the interpolated clearance. This allows the thrust bearing to be assessed based on such criteria as the ability to handle misalignment stresses, minimum clearance, power loss, flow rate and so forth.

If the film temperature has been user specified, the temperature loop may be repeated for addition specified temperatures. Otherwise, the THRUST module is terminated and the thrust bearing analysis complete. As with the above radial bearing analysis, if the steady-state and rotordynamic characteristics do not meet acceptable performance characteristics, the bearing is redesigned and the above process repeated until acceptable performance is provided.

Currently the best way of modifying the pad shape and support structure wherein the steady-state and rotordynamic behavior is found to be unacceptable is manually selecting a new design based on experience and knowledge of how modifications to the support structure and pad shape affect bearing performance, as discussed in detail below. Since this information is known as a result of the present inventor's disclosure, however, it is contemplated that modified bearing designs could be generated automatically by a computer or the like so that the entire bearing design process could be automatic. This could be done in two ways. First, the computer could simply evaluate all possible bearing constructions within a prescribed universe. Alternatively, the computer could be programmed to make "intelligent" choices based on the design considerations discussed herein using expert system technology.

The first option is inefficient and currently is prohibitively expensive because of the number of calculations which would have to be performed. The second option is believed much more practical and will become increasingly practiced as improvements are made in expert systems employing so called "artificial intelligence."

Having described the method and apparatus used to design bearings according to the present invention, applicant will now describe a variety of possible bearing designs to illustrate the structural features which can be used in a bearing designed according to the present invention.

In describing these bearing designs in an understandable way, it is helpful to describe the bearing structures as being formed from a cylindrical blank by providing grooves, slits, bores and other openings in the cylindrical blank. As noted below, this is sometimes a useful technique for manufacturing a prototype bearing. However, the reference to the cylindrical blank is primarily intended to assist understanding of the present invention. It should be noted that although many of the bearings of the present invention could be manufactured from a cylindrical blank, it is not necessary that any of them be so manufactured. Indeed the bearings can be manufactured in numerous ways, some of which are discussed hereinafter.

Although the present invention provides a bearing construction which can be designed such that the pads are free to move in six directions, such freedom of movement is not always needed. For example, in conventional tilt bearings, see FIG. 1E, the individual pads need only tilt or pivot about an axis parallel to the rotor. A known rocker pivot pad has nearly zero rotational pivot stiffness. Such bearings are known to provide adequate performance, but they are expensive and difficult to tailor to individual applications. The function and performance can be replicated using bearings of the present invention which are of course, significantly less expensive than rocker pivot pad bearings.

The present invention also relates to one piece bearings designed to operate as tilt-pad bearings in a lubricant filled environment. In particular, the present inventor has found that the performance of expensive multi-part rocker pivot pad bearings can be replicated in a single piece bearing in which the pads are supported on a single thin web. The pivot stiffness of such a pad is determined by the support web thickness. When the web thickness is low enough, tilt-pad behavior results as illustrated in FIG. 1D.

The effect of web thickness is typically expressed in terms of the principal stresses and cross coupled stiffness. Cross coupled stiffness is a term of art which can be though of as a measure of the resistance to tilting. As tilt stiffness drops, the cross-coupling terms asymptotically approach zero, which by definition yields tilt-pad behavior. At high pad tilt stiffness, the cross-coupling asymptotically approaches the high (negative) fixed-geometry values, resulting in much lower stability that is characteristic of fixed-geometry bearings. The principle coefficients vary slightly from the asymmetric (unequal) fixed-geometry values, to symmetric (equal) values that are characteristic of a four-pad tilt-pad bearing with load between pads.

In general, tests and analysis have shown that the one piece tilt pad bearing of the present invention exhibits fixed-geometry performance with high tilt stiffness, and tilt-pad, variable geometry, performance at low tilt stiffness. Intermediate stiffnesses reflect transition from fixed-geometry behavior to tilt-pad behavior. Thus, the web thickness must be chosen low enough to exhibit tilt-pad stability without becoming overstressed from shaft loads or tilt stresses. The tilt-stresses are low because of the very small tilt angles traversed by the pads during operation.

Another desirable feature available from the design of the bearings of the present invention is the narrower range of pre-load that can be obtained. Tilt pad bearings suffer from the stack-up in tolerances and thus result in a wide range of pre-load. This range increases as the bearing dimensions are reduced. The one-piece bearings of the present invention can, however, be manufactured to closer tolerances. In part, this is due to the fact that the position of the components relative to one another is fixed in a one-piece design. Thus, tolerances are not additive.

FIG. 1A illustrates one form of tilt pad bearing according to the present invention. The bearing is designed to operate in a liquid filled environment. In operation, the pads tilt so as to pressurize the liquid. As shown, the bearing includes five spaced bearing pads 31. The number of bearing pads can, of course, be varied to suit any particular application. The bearing pads 31 are each supported on a bearing housing 30 via a single thin web-like ligament 37. As shown, the ligament has a radial length which significantly exceeds its circumferential width.

In the embodiment illustrated the web 37 is provided on the circumferential center line of the pad 31 so that the bearing supports the shaft rotation in either the clockwise or counterclockwise direction, i.e., the bearing is bidirectional. The web 37 extends generally radially between the pads and the bearing housing. The bearing may be formed by machining a solid bronze puck through an electric discharge machining (EDM) process, but this is not required. According to the present invention, the webs 37 must support the pad with enough radial stiffness to support the shaft loads without becoming overstressed, while also providing enough rotational (tilt) flexibility to exhibit tilt-pad performance. Although the acceptable range of web thickness varies from application to application, the present inventor has found that the web thickness should, at minimum be less than the radial length of the web. If the webs are too thin, the web will be overstressed and the bearing will be destroyed. On the other hand, if the webs are too thick the pads will no longer function as tilt pads, instead functioning either in the transition regime or as fixed geometry pads. Of course, the stresses that result from tilting must also be within the endurance limit to avoid fatigue failure. The endurance limit is defined as the allowable stress below which you can have an infinite number of cycles. Other facts that can affect performance include thermal effects and pad surface movements. Optimization of the support structure configuration for individual applications precludes high stresses and ensures long life. As mentioned previously stresses are minimized because of the small tilt angle. The absence of moving parts eliminates pivot wear and durability concerns by eliminating the pivot pad contact stresses. Manufacturing tolerances are completely eliminated all but the final bearing bore, thus simplifying the manufacturing process. EDM manufacturing is efficient and accurate for low volume applications, while high volume applications can be cast, molded, extruded or forged as discussed herein.

FIGS. 1D and 1E show a comparison of the tilting pad function of the tilt pad bearings of the present invention (FIG. 1D) with a conventional tilting pad construction (FIG. 1E). As is illustrated therein the simple one piece tilt pad bearing construction of the present invention pivots in essentially the same manner as a conventional pivot bearing. Again, the critical design feature for successfully replicating the performance of a tilt-pad bearing is providing the appropriate web thickness.

It should noted that FIG. 1A illustrates a bearing which is extremely simple and is designed to simply replicate the performance of a pivot pad bearing. Consistent with the teachings of the present invention, however, this bearing construction can be further modified to provide additional flexibility if desired. For instance, facing grooves can be provided in any sides of the bearing to reduce the axial thickness of the web so as to enhance the ability of the pads to twist to accommodate shaft misalignment. Moreover, the outer periphery of the bearing housing can be formed with grooves or projections to increase the radial flexibility of the pads so that the pads can move in the radial direction.

FIG. 1B illustrates another tilt-pad bearing according to the present invention. This bearing construction is similar to that shown in Figure A with few exceptions. First, the webs 37 are circumferentially offset so that the bearing is, in effect, designed to support the shaft for rotation in only one direction. Because the support is different for each direction of rotation, the tilting characteristics of the pad will vary and will only operate properly in one direction. The bearings shown in FIG. 1B includes six circumferentially spaced bearing pads 31. Again, each of the pads are supported on a single radially extending thin web 37. The webs are supported on a bearing housing 30. Once again, it is critical that the webs 37 are thick enough to avoid tilting stress, but thin enough such that the pads tilt as tilt-pads rather than as fixed geometry pads. As shown, the ligaments have a length which exceeds their circumferential width. In the embodiment illustrated in FIG. 1B, the bearing housing 30 is provided with radially extending oil lubricating passages 30o to allow the lubricant to flow into a bearing housing. The oil lubricating passages 30O are preferably located between adjacent pads as shown in FIG. 1B.

In accordance with another aspect of the present invention, tapered thrust lands 31T are provided on the bearing housing 30 to carry small thrust loads incurred during operation. This might be necessary, for example, when the bearing is used in a planetary gear arrangement wherein small thrust loads are incurred in positioning the planet gear shaft. The thrust loads 31 should, preferably, be circumferentially spaced along the bearing. Like the embodiment of FIG. 1A, the embodiment of FIG. 1B includes simple pivoting-type webs. Again, however, the support structure could be modified to provide additional flexibility as discussed herein.

Referring now to FIGS. 2, 2A and 3, the structure therein illustrated is a sector of a journal bearing assembly having grooves and slits formed therein so as to define a housing 10 and a plurality of circumferentially arranged bearing pads 12 each of which is supported by a support structure which includes the housing, a beam 14 and a stub section 126. The bearing is not symmetrical about the pad circumferential center line 13a (FIG. 3).

Accordingly, the bearing illustrated is a radial unidirectional bearing, i.e., it is adapted for radially supporting a shaft for rotation in only one direction. In the illustrated embodiment, the bearing supports the shaft 5 only for rotation in the counter-clockwise direction illustrated by the arrow. On the other hand, if the bearing were symmetrical about the center line of the pad would be capable of supporting the shaft 5 for either clockwise or counter clockwise rotation, i.e., the bearing would be bi-directional.

Each bearing pad 12 includes a leading edge 15 and a trailing edge 17. The leading edge is defined as the edge first approached by a point on the circumference of the shaft as it continues to rotate. Similarly, the trailing edge is defined as the edge approached circumferentially later by the same point on the shaft as it continues to rotate. When the shaft 5 is rotating in the proper direction, it moves, on a fluid film, from the leading edge across the bearing pad and off the trailing edge. Optimum performance is obtained when the stub-section 16 supports the bearing pad 12 and hence any load, at a point 16a (FIG. 3) between the circumferential center line 13a of the pad 12 and the trailing edge 17, preferably closer to the center line 13a. The beam 14 should also pivot about a point 14a which is located angularly between the leading edge and the trailing edge so that as a result of movement of the beam 14, the trailing edge 17 moves inwardly. Of course, the degree of movement depends on, among other things, the shape of the beam and the length of the cuts or slits formed in the bearing.

Although specific reference is made to either journal bearings or thrust bearings to facilitate an understanding of this invention, some of the same principles of bearing design apply regardless of the specific form of bearing being designed. For example, both types of bearings operate on the principle of formation of a hydrodynamic wedge. Further, the major axis of both journal bearings and thrust bearings is the central axis of the cylindrical blank from which the bearing is formed. The circumferential pad center line is the radially extending line passing through the geometric center of the pad and the major axis of the bearing. Accordingly, if either a thrust bearing or a journal bearing is symmetrical about this center line axis, i.e., the major axis, the bearing will be bi-directional.

There are significant differences between thrust bearings and journal or radial bearings. The most prominent difference is, of course, the portion of the shaft supported and consequently the orientation and/or attitude of the bearing pad supports. For instance, while journal bearings support circumferential portions of shafts, thrust bearings support shoulder or axial end portions of shafts. Other differences follow from this fundamental difference. For example, in a radial or journal bearing, the pads in the direction of the load take or support the load; whereas, in a thrust bearing, all pads normally share load. Moreover, a journal bearing generally has a built-in wedge due to differences in the shaft and bearing diameters; conversely, there is no such built-in wedge in thrust bearings. Additionally, while a journal or radial bearing controls rotational stability as well as load; a thrust bearing typically only carries load. It should also be understood that the design of journal bearings, particularly hydrodynamic journal bearings, is significantly more complicated than the design of thrust bearings. In part, this is because of the constraints imposed by the need to limit the radial envelope of the journal bearings. In order to accommodate these differences the configuration of the thrust bearings is naturally somewhat different than that of journal bearings. Nevertheless, as is evident from this disclosure, many of the principles discussed herein are applicable to either thrust or journal bearings.

Referring now to FIGS. 2 and 3, it will be seen that the pad 12 is provided with an accurate face 13 which corresponds essentially to the radius or arc of the outer diameter of the shaft which the pad will be supporting (via the fluid film) and each pad is defined by axially extending and radially extending edges. The axially extending edges comprise the leading and trailing edges. The beam is shown both in a static position (solid lines) and in a deflected position (phantom lines) in FIG. 3. The basic construction of the support structure as illustrated in FIG. 1, is created by the use of small slits or cuts through the wall. Typically these slits or radial cuts are between 0.002" to 0.125" wide. The degree of movement can be varied by varying, among other things, the length of the cuts. Longer cuts provide a longer moment arm which yields greater movement. Shorter cuts yield beams having less flexibility and higher load carrying ability. In selecting a length of cut or slit, care must be taken to avoid resonance.

By locating the end of beam 14 as shown, the movement downward about the connection point 16a will result in inward movement of the trailing edge 17 of the pad 12, outward movement of the leading edge 15 and a slight flattening of the pad 12 as seen in the dotted lines of FIG. 9. As a result of this movement, the gap between the pad face 13 and the outer surface of the shaft 5, through which fluid flows, becomes wedge shaped to yield the well-known hydrodynamic support effect.

Ideally the ratio of the spacing between the trailing edge and the shaft versus the spacing between the leading edge and shaft is between 1:2 to 1:5. In other words, the spacing between the leading edge and shaft should be between 2 to 5 times greater than the spacing between the trailing edge and the shaft. In order to attain this ideal spacing or wedge ratio for any specific application, appropriate movement variables including number, size, location, shape and material characteristics of the unitary element must be selected. A computer aided finite element analysis has proven to be the most efficacious means of optimizing these variables. Computer aided analysis is particularly useful in a bearing such as the type described above which permits movement in all six directions (six degrees of freedom).

The most important consideration in the performance of a hydrodynamic bearing is the shape of the space, typically a converging wedge, between the rotating shaft to be supported and the bearing pad surface. Since the shape of the shaft surface to be supported is basically invariable, it follows that the most important consideration in the design of hydrodynamic bearings is the shape of the pad surface under load. The shape of the pad surface under load principally depends upon two factors: the shape of the pad itself and the construction and location of the pad support structure. For purposes of this description, the various support structure designs will be discussed first followed by a discussion of various pad designs. It must be emphasized that the various support structures disclosed herein can be used with any of the pad shapes disclosed herein and the pad-shapes used herein can be used with any of the support structures disclosed herein.

Referring to FIGS. 4 and 5, there is shown a second illustrative example of a bearing incorporating features of the present invention in which the bearing is formed with slits or cuts and grooves to define a bearing housing 30 with a bearing pad 32 that is supported from the housing by a support structure which includes a beam having a pair of beam portions 34a, 34b which extend substantially in a single line away from the pad. Moreover, the pad may be undercut so that it is supported by the beams only on a pad support surface 34ps. Referring to FIG. 5, it will be seen that the beams 34, 34a have a convenient stub beam end as is 36, 36a which acts as a cantilever support for the beam.

As is evident from FIG. 4, the perspective view of FIG. 5 shows only a portion of the pad 32. The complete pad is illustrated in FIGS. 5A and 5B which show possible modifications of the bearings illustrated in FIG. 4. As is clear from the drawings, the pad support surface 34ps is located closer to the trailing edge 37 than the leading edge 35. With this construction, twisting of the beam, as illustrated in FIG. 7, will take place intermediate the beam and create the torsional movement illustrated. Again the primary flexibility is developed by small cuts or slits through the bearing housing wall. These cuts provide the bearing pad with six degrees of freedom (i.e., the pad can translate in the +x,-x, +y,-y, +z and -z directions as well rotate about the x, y and z axes) and are designed to optimize hydrodynamic wedge formation. If the cuts or slits were terminated before breaking through to form beam portions 34a and 34b, the pad 32 would be supported by a continuous cylindrical membrane 34m as shown in FIG. 5A. The membrane acts as a fluid damper upon which the pad 32 is supported. The termination of the cuts would occur at Point A and Point B of FIG. 4. The flexibility of the membrane, combined with the fluid lubricant, provides a means to vary the damping action and to isolate the pad from the housing. The damping takes the form of a dash pot that exhibits high damping characteristics.

As shown in FIG. 5B, the beam may be defined more simply than shown in FIG. 5 by simply extending the cuts or slits downward from points A and B.

In such a case, the bearing is supported for simple flexural rotation, i.e., on a single radially extending beam. As noted earlier, such a construction is well suited for certain applications. It should be noted that with such a construction, the beam is slightly longer in the radial direction than it is wide, to ensure sufficient flexibility.

Referring to FIG. 8, there is shown another illustrative example of a bearing incorporating features of the present invention. In this example, internal slits or cuts are provided to create a beam on beam support structure. Specifically, the bearing is formed with grooves and slits or cuts to define a pad 40 which is supported from a housing by beams 42 and 44. The pad is connected to the beams at support stubs 40a and 40b. Beam attachment to the housing is at support stubs 46 and 48. Again the bearing consists of the thin cuts or slits shown cut through the bearing wall. The cut or slit 60 below the pad surface introduces additional flexibility such that under load the pad changes shape to form an airfoil for the introduction of lubricant. Thus, as a result of the beam on beam two point support, the pad acts as a spring like membrane.

FIG. 10A shows the deflected shape of the pad 40 under load. As shown in the drawings (exaggerated), the pad can be formed and supported so as to move to an airfoil shape under load. The airfoil dramatically improves performance. As is evident from the drawings, the pad is capable of displacement in the x, y, and z directions as well as rotation about the x, y, and z axes, that is, the pad has six degrees of freedom. Again, the structure allows optimal hydrodynamic wedge formation.

Referring to FIG. 9, there is shown the local inherent movement of the face pad 50 where the pad flattens under load. These movements are combined with the support structure movement shown in FIGS. 3 and 10 but are of a lower magnitude. The net result is the shape shown in FIGS. 3 and 10 but with a face curvature that has been minutely flattened.

FIGS. 31 and 31A illustrate another example of a journal bearing in accordance with the present invention. The bearing construction illustrated in FIGS. 31 and 31A differs from the previously described journal bearing constructions in that the bearing is bi-directional, i.e., the bearing is capable of supporting a shaft for either clockwise or counterclockwise rotation as viewed in FIG. 31. The bearing is bi-directional because the pads are symmetrical about their center line, which is defined as the radial extending line passing through the bearing major axis (606) and the geometric center of the pad. Like the previously described journal bearings, the bearing of FIGS. 31 and 31A is formed with a plurality of thin radial and circumferential slits to define a plurality of circumferentially spaced bearing pads 632.

The support structure for each of the bearings pads 632 is somewhat similar to the support structure for the journal bearing illustrated in FIG. 8. In particular, each bearing pad 632 is supported by a beam support structure at two pad support surfaces 632ps. The beam network connected to the bearing pads at each pad support surface 632ps is identical, yielding the symmetrical construction of the bearing which makes the bearing bi-directional. For purposes of simplifying this description, only the network of beams which supports the bearing at one pad support surface will be described since the other pad support surface is supported in an identical fashion. Thus, as shown in FIG. 31, a first, generally radially extending beam 640 is connected to the bearing pad 632 at the pad support surface 632ps. A second, generally circumferential beam 642 is connected to the radially outermost end of beam 640. A third, generally radial, beam 644 extends radially inward from the beam 642. A fourth, generally circumferential beam 646 extends from the radially innermost portion of the beam 644. A fifth, generally radial beam 648 extends radially outwardly from a beam 644 to the housing portion of the support structure. In summary, each bearing pad 632 and the bearing illustrated in FIG. 31 is supported by ten beams and the bearing housing. Further, as discussed below, by forming radially extending circumferentially spaced grooves or continuously extending circumferential grooves in the housing portion of the support structure, the housing portion of the support structure can be designed to act as a plurality of beams or membranes. It should also be noted that, like the bearing in FIG. 8, the cut or slit formed below the pad's surface introduces additional flexibility such that under load the pad changes shape to form an airfoil for the introduction of lubricant. Thus, as a result of the beam on beam two point support, the pad acts like a spring-like membrane.

FIG. 31A is a radial cross-section of FIG. 31 showing the third beam 644, the bearing pad 632 and the housing.

FIGS. 32, 32A and 32B illustrate another journal bearing construction in accordance with the present invention. This bearing construction differs from the previously described bearing constructions in that the bearing pads and support structure are defined by relatively large grooves and openings formed in a cylindrical blank. Normally, this type of construction would be formed by milling the blank rather than electrical discharge machining or some other similar technique for farming small grooves as with the previously described embodiments. An advantage of the bearing construction illustrated in FIG. 32 is that in applications requiring extremely small bearings it is easier to form precisely the proportionately larger cuts and openings required to form a bearing of the type illustrated in FIGS. 32, 32A and 32B as compared to the proportionately smaller cuts and openings required by the construction of, for example, FIGS. 1, and 8. Moreover, the large grooves or openings are generally easier to mold or extrude bearings formed by larger cuts also find use in applications requiring extremely large bearings with stiff bearing pad support structures.

The bearing pads shown in FIG. 32 are symmetrical about their pad center line, 706A. Hence, the bearing is bi-directional. Moreover, as best shown in the perspective view of FIG. 32B, the bearing has a continuous cross-section with no hidden openings. Hence, it is easily extrudable and easily moldable. Naturally, the support structure can be altered by providing discontinuities in the cross-section, e.g., by providing radially extending circumferential grooves or non-symmetrically disposed radially extending openings to alter the support structure and thereby alter the performance characteristics. The bearing's major axis is 706.

As shown in FIG. 32, the bearing includes a plurality of circumferentially spaced bearing pads 732. Each bearing pad 732 is supported by a support structure which includes a pair of generally radial beams 740 connected to the bearing pad 732 at a pad support surface. A second, generally circumferentially extending beam 742 supports each of the beams 740. Beams 742 are connected to the housing or support stubs 744 in a cantilever type fashion. In this bearing, the beams 740 can be regarded as a primary support structure; the beams 742 can be regarded as a secondary support structure; and the beams 744 can be regarded as a tertiary support structure.

The second beams 742 shown in FIG. 32 are defined by forming a plurality of axially extending circumferential grooves 750 in the housing of the support structure. In order to maintain the symmetry of the bi-directional bearing, these grooves are circumferentially spaced about pad center lines 706A in a manner identical to the circumferential spacing of the bearing pads 732. Naturally, similar circumferentially spaced radial grooves could be provided in any of the previous bearing constructions. For instance, as noted above, such grooves could be formed in the periphery of the bearing construction illustrated in FIGS. 31 and 31A to provide a further beam-like support.

FIG. 32A is a radial cross-section of a portion of the bearing illustrated in FIG. 32. In this cross-section, the bearing pad 732 and first beam 740 are visible.

FIG. 32B is a perspective view of the bearing of FIG. 32. It should be noted that although the peripheral, circumferential and cylindrical portions of the bearing are depicted in a somewhat segmented fashion to emphasize the curvature, these curved surfaces are in fact continuously curved.

FIG. 33 illustrates a journal bearing construction according to the present invention. Like the bearing of FIG. 32, the bearing of FIG. 33 is formed by proportionately large grooves and bores. In particular, a plurality of equally spaced radially extending circumferential grooves define a plurality of circumferentially spaced bearing pads 832. The bearing pads 032 are further defined by a pair of axially extending circumferential grooves which extend symmetrically from the planar faces of the cylindrical blank and are best seen in FIGS. 33B and 336 in which the grooves are indicated by the reference numerals 834 and 835. The bearing support structure is defined by the aforementioned structural features and by a plurality of circumferentially spaced symmetrically disposed shallow bores 838 and a plurality of circumferentially spaced symmetrically disposed deep bores 837. Because of the presence of the "hidden" bores 837, 838, the bearing construction of FIG. 33 is not extrudable and not moldable in a simple two-piece mold, i.e., not easily moldable.

As best shown in FIG. 33A, the deep bores 837 intersect the axial grooves 836 so as to define support structures for each bearing pad. The support structure is further defined by a circumferential groove 839 extending from the outer periphery of the cylindrical blank.

With reference to FIGS. 33-33c, it will be understood that the provision of the structural members as discussed above provide a support structure for the bearing pad 832, which includes a beam 840 directly supporting the pad, i.e. a primary support structure, two continuous beams 882, i.e. a tertiary support structure and a secondary support structure comprising a plurality of beams defined in part by bores 837 and 838 connecting the beam 840 to the continuous beams 882.

Because the support structure of the bearing illustrated in FIGS. 33-33C is non-symmetrical about the pad center line extending from the major axis 806, it is unidirectional. Further, like the bearing of FIG. 32, this bearing is particularly well suited to applications requiring extremely small bearings since the proportionately larger grooves and bores which define this bearing and its support structure are more easily manufactured.

FIGS. 34 and 34A-34D illustrate another journal bearing construction in accordance with the present invention. The bearing construction of FIG. 34 is similar to that of FIG. 33 insofar as the bearing pads and their support structures are defined by proportionately large grooves and bores as shown in the drawings. The support structure for the bearing pads 932 is like the support structure for the bearing pads 832. In particular, while the support structure for each of the bearing pads 932 is identical, the support structure is not symmetrical with respect to each bearing pad. Hence, the bearing illustrated in FIG. 34 is unidirectional. Moreover, because the support structure includes "hidden" openings, the bearing is neither extrudable or moldable in a simple two-piece mold.

As shown in the drawings, the bearing support structure includes a primary support structure comprising a pair of beam-like members 940 which are connected to the bearing pads 932 and defined in part by symmetrically disposed openings 942. A shallow circumferential groove formed on the outer periphery of the bearing defines a tertiary support structure comprising a pair of continuous beam-like elements 982. A secondary support structure comprising a beam and membrane network 960 for connecting the beams 940 to the continuous beams 982 is defined by the provision of a plurality of large symmetrically disposed bores 944, the provision of smaller symmetrically disposed bores 946 and the provision of small non-symmetrically disposed bores 948. By virtue of the provision of the non-symmetrically disposed bores 948, the support structure is more flexible, and thus biased, in the direction of those bores.

FIGS. 15-18 illustrate a unitary hydrodynamic thrust bearing in accordance with the present invention. As noted earlier, thrust bearings in accordance with the present invention incorporate some of the same features as journal bearings in accordance with the invention. For instance, like journal bearings, the thrust bearings of the present invention have a major axis defined as the central axis of the blank from which the bearing is formed. Also the bearing pads have a circumferential center line extending from the major axis through the geometric center of the pad. When the thrust bearing is symmetrical about its circumferential center line it is bi-directional; when the bearing is non-symmetrical about its circumferential center lines, it is unidirectional. However, by nature of their different function, the thrust bearings have a slightly different configuration. For example, the thrust bearing shown in FIGS. 15-18 includes a plurality of bearing pads 132 of substantially identical configuration. FIG. 18 shows the circumferential dividing line CDL and radial dividing line RDL of the bearing pad 132. The bearing pad surfaces of the bearing pads 132 lie in a plane which is essentially transverse to the axis of the shaft to be supported and the bearing's major axis. Of course, when the pad surfaces are moved under load, or if it is desired that the bearing be skewed slightly so as to contact the shaft in the installed or static state, the surface of the bearing pads may be somewhat non-planar and somewhat skewed with respect to the major axis or the axis of the shaft to be supported.

A particularly important consideration in the design of thrust bearings of the present invention is the prevention of fluid leakage. To a large extent, this objective is achieved by designing the support structures such that under load the inner edge of the bearing pads move downward (as viewed in FIG. 16) and the outer edge moves upwardly. All of the thrust bearings described herein are designed in this manner. For instance, in the bearing shown in FIG. 16, the beam 134 is connected to the pad 132 at a pad support surface 134ps which is closer to the outer edge of the bearing pad than it is to the inner edge of the bearing pad. Thus, the pad support surface 134ps is located radially outward of the radial dividing line RDL shown in FIG. 18. Hence, the bearing is designed such that, under load, the inner edge of the bearing moves downward.

In operation, the downward movement of the inner edge of the bearing pad corresponds to movement away from the shaft supported and the upward movement of the outer edge of the bearing pad corresponds to movement toward the shaft. The deflected orientation of the bearing pad significantly inhibits the loss of fluid which otherwise occurs as a result of centrifugal forces' action on the fluid.

The loss of hydrodynamic fluid can be further reduced by supporting the bearing pad such that under load, the bearing pad deforms to form a lubricant retaining pocket. Generally, such support is achieved when the bearing pad is supported by a plurality of radially or circumferentially spaced beams and the region between the beams is not directly supported such that the unsupported central region of the pad will tend to deform outwardly so as to form a fluid retaining channel. FIG. 29, which is discussed below, illustrates an example of a bearing having the requisite radially spaced beams therein. A greater pocket is obtained when the beams are spaced further apart. In a similar manner, a channel can be formed in a journal bearing by providing axially or circumferentially spaced beam supports and an unsupported region between the beams.

As best shown in FIGS. 15 and 16, each bearing pad has a chamfer or bevelled edge 132b around its entire periphery. The purpose of the chamfer is to reduce entrance and exit lubricant losses.

Each of the bearing pads 132 is supported by primary support portion, which in the illustrated embodiment comprise a beam-like support member 134 supporting the pad at a bearing pad support surface 134ps. Each beam 134 is in turn supported by a secondary support portion such as a beam supported beam or membrane 136. The beam or membrane 136 is in turn supported by a tertiary support member such as pair of beam-like legs 138a, 138b.

By providing holes or openings 142 in the beam or membrane portion 136, the continuous membrane 136 becomes a set of beams 136. Naturally, if holes or openings 142 are not provided in the membrane 136, the membrane functions as a continuous membrane. Alternatively, the inner beam-like leg 138a could be replaced with short stub-like beams or even eliminated to define a tertiary support such that the secondary support is supported in a cantilever fashion. Finally, because the holes and openings are symmetrically disposed with respect to the major axis the bearing is symmetrical about the major axis and is therefore bidirectional.

As shown in FIGS. 15, 17 and 18 the holes or openings 142 which divide the continuous membrane into separate beams are round. The use of round openings facilitates manufacture of the bearing prototype because circular openings can easily be drilled into the bearing material. This is true of all the bearings described herein. Once such circular openings are provided, it may also be advantageous to extend the openings past the beam or membrane member 136 to the lower portion of the bearing pads 132 so as to define the beam-like members 134. This is why in FIG. 15, the cross-section of the pad support surface 134ps and consequently the sidewalls of the beam 134 have an accurate appearance.

Although the shape of the beam members may be dictated by manufacturing convenience, the shape also effects the performance of the individual bearings. Thus, although the specific shape of the bearings described herein, including the thrust bearing shown in FIGS. 15-18, is primarily attributable to the ease of manufacturing a prototype, it also has been found to yield excellent results for a specific application. Any changes in the shape would, of course, influence the performance characteristics of the bearing by, for example, altering the bending or twisting characteristics of the beams which support the bearing pad. Thus, while other shapes of beams, pads and membranes are certainly contemplated, both the ease of manufacturing and the effect of the beam pad or membrane's shape on bearing performance must be considered.

Examples of other thrust bearing shapes are shown in an FIGS. 21-30 and 38-39. The difference between these bearings and the bearing construction shown in FIGS. 15-18 primarily resides in different constructions of the primary support portion, the secondary support portion and the tertiary support portion.

One such other bearing shape is illustrated in FIGS. 21-24. A top view of the bearing is shown in FIG. 21; a cross-section of the bearing is shown in FIG. 22; a bottom view of the bearing is shown in FIG. 23 and a perspective view of the bearing is shown in FIG. 24. The bearing shown in FIGS. 21-24 is similar to the bearing of FIGS. 15-18 with two notable exceptions. First, the bearing of FIGS. 21-24 includes an angled or slanted support beam 134A rather than a vertical support beam as in FIG. 15. Second, the bearing includes additional holes 144 which extend through the support beam 136 to form a cylindrical opening through the slanted or angled beam 134 so as to form elliptical openings in the support beam. The elliptical openings divide the beam into a pair of complex ligaments, the shape of which can be appreciated with reference to the perspective view of FIG. 24. The provision of the openings 144 and consequent division of the slanted or angled beams 134A into complex ligaments significantly increases the flexibility of the support structure of the bearing shown in FIGS. 21-24 as compared to the bearings shown in FIGS. 15-18. Thus, the pads 132 of the bearing of FIGS. 21-24 move to form a hydrodynamic wedge in response to a lighter load than do the pads 132 of the bearing shown in FIGS. 15-18. It follows that the bearing shown in FIGS. 21-24 is better suited for supporting light loads and the bearing shown in FIGS. 15-18 is better suited for carrying heavier loads. Further, the provision of angled or slanted support beams such as beam 134A, with or without openings to divide the beam into complex ligaments, increases the flexibility of the pad in the vertical direction since a vertically applied load creates a moment which tends to cause the beam to move toward the center or inner diameter of the bearing and thereby eliminate centrifugal leakage of the lubricating fluid.

FIG. 23A shows a bottom view of a bearing of the type shown in FIGS. 21-24 in which additional holes 146 are formed in the membrane or support beam 136 to enhance the flexibility of the beam or membrane 136 even further. As illustrated in FIG. 23A, the holes 146 are formed nonsymmetrically with respect to each bearing segment. The provision of these holes in such a nonsymmetrical fashion results in a bearing in which the pads tend to move more easily in one direction than in the other direction. In other words, the bearing pads are biased in one direction by the provision of nonsymmetrical openings in the support structure. Naturally, such nonsymmetrically disposed openings can be provided in any of the bearing constructions of the present invention in which it is desired to bias the bearing pads in one direction. It may even be desirable to provide the nonsymmetrically disposed openings or holes such that only selected ones of the bearing pads are biased.

FIG. 25 is a cross-sectional view of another bearing according to the present invention. In accordance with this construction, the bearing pad 132 is supported on a pad support stub 1345 which is in turn supported on a horizontally oriented beam portion 134H which is in turn supported on an inversely angled beam portion 1341. In other respects, the construction is similar to that of the previously described bearings. By virtue of this construction, the bearing has a great deal of flexibility in one direction but it is extremely rigid in the opposite direction.

A similar construction is illustrated in FIG. 26. The difference between the bearing illustrated in FIG. 26 and the bearing illustrated in FIG. 25 is that the bearing illustrated in FIG. 26 uses a vertical beam portion 134V rather than an inversely angled beam portion 1341. The bearings are similar in all other respects. The absence of a angled beam in the bearing of FIG. 26 tends to give the bearing more rigidity in the vertical direction.

FIGS. 27-28 illustrate another embodiment of the bearing construction of the present invention.

As shown in the drawings, this bearing includes a plurality of bearing pads 321-326 (shown in phantom in FIG. 28). Each of the bearing pads 321-326 are supported on a pad support surface 342 of a bearing support structure. The bearing support structure includes a primary support portion composed of a pair of nested frustums supported on a secondary support portion which includes a split peripheral membrane 360 which is supported on a tertiary support portion which includes a pair of peripheral beams 382. The peripheral beams 380 and 382 are similar to those of the previously described constructions. The membrane 360 differs from the membrane in previously described constructions since the membrane 360 is radially split by the groove formed in the bottom of the bearing support structure which forms the nested frustums. The inner frustum is inverted with respect to the outer frustum such that the mean center lines of the frustums merge at a point 350 above the pad support surface 342 and have a cross-section which appears similar to an inverted V. Since the center lines of the frustums intersect at point 350 above the pad surface, the primary support structure supports the bearing pad for pivoting about a point above the pad surface. This ensures proper movement.

The beams 346 and 344 which support the bearing pad can be angled toward one another at the same angle, angled toward one another at different angles, one beam angled and one beam not angled, and angled in the same direction. Of course, variations in the degree of angling of the beams in the primary support structure impacts the movement characteristics of the bearing.

A plurality of holes or openings 420 disposed symmetrically about the bearing support structure divide the nested frustum or inverted V structure into a plurality of support beams 344, 346 and divide the apex of the nested frustums so as to define the pad support surfaces 342. Thus, for example, the bearing pad 321 is supported on a pad support surface 342 by a pair of complex support beams 344 and 346 which are tapered toward one another and have a complex geometrical configuration defined by the cylindrical extending openings passing through the nested frustum section. As best shown in FIG. 27, the center lines of the beams 344 and 346 intersect at a point 350 above the pad surface to ensure proper pivoting support. The individual beams 344 and 346 are supported on a peripheral membrane 360 which is split by the groove which defines the frustums. The membrane is supported by peripheral beams 380, 382. Naturally, as discussed above, the peripheral beams 380, 382 and the peripheral membrane 360 can be circumferentially split to define individual beam supports.

Numerous modifications to the bearing support structure are possible. For example, movement of the support structure can be modified by changing the angle of the beams, changing the location of the holes or openings which define the legs, varying the length of any of the beams or membranes, and changing the width or thickness of any of the beams or membranes. In order to illustrate a number of these possibilities, FIGS. 27 and 28 depict a different support structure for each of the bearing pads 321-326. It should be understood that these various support structures are shown in a single bearing for purposes of illustrating the present invention. In normal use, each of the bearing pads 321-326 would have a similar, though not necessarily identical, support structure to assure uniform performance.

The support structure for bearing pad 322 differs from that of bearing pad 321 by virtue of the provision of a hole or opening 422 which extends through the beam 346 so as to divide the beam 346 into a plurality of beams or sub-beams 346a and 346b. If, like the opening 422, the diameter and positioning of the opening is such that the beam is completely separated, the beam is divided into separate beams. On the other hand, if the opening only partially separates the beam (e.g. opening 423) the beam is divided into sub-beams. As shown in FIG. 27, the opening 422 forms an elliptical opening in the side of the beam 346 such that as viewed in FIG. 27, radially outer beam 344 is visible. By virtue of this construction, the pad 322 is supported by three angled ligaments or beams, 344, 346a and 346b.

Bearing pad 223 is supported by four angled beams or ligaments 344a, 344b, 346a and 346b. This structure is achieved by providing a hole or opening 423 which extends through both beam 344 and beam 346 and divides the pad support surface 342 into two sections.

It should be noted that with respect to all of the modifications discussed herein, the size of the openings should be selected based upon the degree to which the beams 344 and 346 are to be divided into separate beams. In some instances it may be desirable to completely separate the beam sections, in which case a larger opening would be used. In other instances, such as that illustrated with respect to the support of bearing pad 323, it is desirable to subdivide the beam at some point along the sidewall of the beam. It should also be noted that although the drawings only show the provision of one opening for bearing pad support structure to divide the beams 344 and 346 it is possible that two or more openings similar to that of the openings 422-426 shown in FIG. 28 could be provided so as to divide the beams 344, 346 into three or more beams or sub-beams. As always, a determination of the type of support to be employed depends on the desired performance characteristics. Generally, dividing the beams into separate beams or sub-beams makes the support structure more flexible. By making the support structure more flexible in one direction as with the support structure for bearing pads 322, 324 and 326, the bearing pads are biased in a predetermined direction.

The support structure for bearing pad 324 is similar to that for bearing pad 322 except that the opening 424 extends through the outer support beam 344 rather than the inner support beam 346. Thus, like the bearing pad 322, the bearing pad 324 is supported by three angled legs.

The support structure for bearing pad 325 is similar to that for bearing pad 321 except that an opening 425 is provided through the outer peripheral beam 380 and peripheral membrane 360 in a nonsymmetrical position. Thus, the bearing pad 325 is biased in a predetermined direction, i.e., the direction of greatest flexibility caused by the provision of the opening 425.

The support structure for the bearing pad 326 is similar to that of bearing pad 322 except that the opening 426 which divides the beam 346 is provided in a nonsymmetrical fashion so as to bias a bearing pad 326 in the direction of greater flexibility, i.e., the direction of the smaller, more flexible beam.

Naturally, any combination of the support structures illustrated in FIGS. 27, 28 could be employed to achieve desired performance characteristics.

FIGS. 29-30 illustrate another embodiment of the bearing of the present invention. As shown in the drawings, this bearing includes a plurality of bearing pads 521-526 (location shown in phantom in FIG. 30). Each of the bearing pads 521-526 are unitary with, and supported on, a bearing pad support structure. Generally, the bearing pad support structure includes at least a primary support structure including an inner circumferential support beam 546 and an outer circumferential support beam 544; a secondary support portion including an inner peripheral membrane 362; and a tertiary support portion including an outer peripheral membrane 364 and an inner peripheral support beam 382 and an outer peripheral support beam 380. As best shown in FIG. 29, the circumferential support beams 544, 546 are defined in part by a deep circumferential channel extending from the bottom of the bearing to the bearing pad. The support beams are further defined by a plurality of holes or openings 620 disposed symmetrically about the bearing pad support structure which separate the beams 544, 546 from adjacent beams. Thus, for example, the bearing pad 521 is supported on a pair of beams 544 and 546, which beams have generally accurate side walls. As mentioned earlier, the beam support structure also includes membranes 364, 362 and peripheral beams 380, 382.

Numerous modifications to the bearing support structure are possible. In order to illustrate a number of these possibilities, FIGS. 29 and 30 depict a different support structure for each of the bearing pads 521-526. As with the previously described embodiment of FIGS. 27-28, these various support structures are shown in a single bearing for the purpose of illustrating the present invention. In normal use, each of bearing pads 521-526 would have a similar, though not necessarily identical, support structure to assure uniform performance.

The support structure for bearing pad 522 differs from that of bearing pad 521 by virtue of the provision of a hole or opening 622 which extends through the inner circumferential beam 546 so as to divide the beam 546 into a plurality of beams 546a and 546b. By virtue of this construction, the pad 522 is supported by three vertically extending beams or ligaments 544,546a and 546b.

The bearing pad 523 is supported by four vertically extending beams or ligaments 544a, 544b, 546a and 546b. This structure is achieved by providing a hole or opening 623 which extends through both beam 544 and beam 546. The thinner beams which result from this modification would naturally have greater flexibility than the support structure for bearing pads 522 and 521.

The bearing pad 524 is supported by five, relatively thin vertically extending beams or ligaments. This structure is achieved by providing a hole or opening 624 to divide the inner beam 546 into two beams and providing two holes 624 to divide the outer beam 544 into three beams.

The support structure for bearing pad 525 is similar to that for bearing pad 522 except that an additional opening 635 non-symmetrically divides the outer beam 544 into two beams. By virtue of the non-symmetrical division of the outer beam 544, the bearing pad is biased in the direction of greater flexibility.

The support structure for bearing pad 526 is similar to that for bearing pad 522 except that the outer beam 544 is split rather than the inner beam 546. Further, the opening 626 is somewhat larger than the opening 622 such that a groove is formed on the outer periphery of the inner beam 546 so as to make the inner beam 546 somewhat more flexible.

Naturally, any combination of the support structures illustrated in FIGS. 29, 30 could be employed to achieve desired performance characteristics.

FIGS. 29A, 29B, 30A and 30B illustrate in detail a thrust bearing in which each of the bearing pads 521A of the support structure are very similar to that used to support bearing pad 521 in FIGS. 29 and 30. The bearing construction is different, however, insofar as the beams 544A and 546A are circumferentially narrower and vertically shorter than their counterparts in the bearing illustrated in FIGS. 29 and 30. Naturally, shorter beams are more rigid than the comparatively longer beams and narrow beams are less rigid than comparatively wider beams. Moreover, the beam 544A is radially narrower than the beam 546A; whereas in the bearing illustrated in FIGS. 29 and 30, the beams 544 and 546 have equal widths. The difference in radial thickness is compensated for since the large opening 620, which defines the circumferential extent of the beams 544A and 546A, is arranged such that beam 544A is significantly wider in the circumferential direction than is beam 546A. Finally, it should be noted that the openings 620 are significantly larger than the corresponding openings 620 in the bearing construction of FIGS. 29 and 30. Naturally, the larger openings increase the flexibility of the support structure defined thereby.

FIGS. 35-37 illustrates a combined thrust and radial hydrodynamic bearing in accordance with the present invention. The bearing illustrated in FIG. 35 is quite similar to the bearing illustrated in FIG. 34 and similar numerals are used to designate similar structure. Similarly, as viewed in the cross-section in FIG. 37, the bearing of FIGS. 36-37 is somewhat similar to the radial bearings illustrated in FIGS. 4 and 14D except that the bearing pad 1032 and the bearing pad support structure, which includes beams and/or membranes 1034, 1036 and 1038, are defined by proportionately larger slits and grooves. However, the radial-thrust bearings differ from radial-only bearings in that the bearing pad surface 1032ps is angled with respect to the major axis 1006. By virtue of its angled pad surface, the bearings of FIGS. 35-37 support loads acting both along the major axis 1006 and radially from the axis 1006.

In order to be supported by the angled pad support face 1032ps, the shaft must be fitted with a runner which is angled at an angle complementary to the angle of the pad support face. The portion of the axial load taken by the bearing and the portion of the radial load taken by the bearing depends on the angle of the pad surface 1032ps. If the pad is angled at an angle .alpha. with respect to the major axis 1006, the axial load applied to the bearing can be determined by the following equation:

Similarly, the radial load applied to the bearing can be determined by the following equation:

The support structure for the bearing shown in FIG. 35 is similar to the support structure for the bearing shown in FIG. 34.

The support structure for the bearing illustrated in FIGS. 36 and 37 includes a primary support structure for the spaced bearing pads 1032 having a beam 1034 which supports the bearing pad 1032, a tertiary support structure which comprises a pair of circumferential beams 1038 which may be continuous. The secondary support structure comprises a membrane 1036 or a network of beams 1036 for connecting beam 1034 to the beams 1038. As shown most clearly in FIG. 36, the support structure for each of the plurality of bearing pads 1032 is nonsymmetrical. Accordingly, the bearing illustrated in FIGS. 36 and 37 is unidirectional.

Generally, any of the general bearing constructions described in this application can be employed in the design of combined radial-thrust bearings of the type illustrated in FIGS. 36 and 37. Of course in order to achieve the combined radial and thrust bearing characteristic, the bearing pad surface must be angled at an angle between 0 and 90 degrees with respect to the major axis. Moreover, the need to accommodate both radial and axial loads necessarily will impact the design of the bearing pad support structure.

In the past, the pad shape of hydrodynamic bearings has been primarily dictated by manufacturing convenience. For a thrust bearing, this has traditionally meant sector shaped pads to maximize the area of support or--in the case of applicant's prior U.S. Pat. No. 4,676,668--circular pads for low cost manufacture. For radial bearings, pads having a simple cylindrical section shape have been used. In many cases, such conventional pad shapes can be supported to obtain optimum results. However, the present inventor has discovered that important performance characteristics can be achieved by modifying conventional pad shapes. Consequently, the support structure can be simplified, and in some cases, even eliminated.

Examples of typical thrust pad shapes are illustrated in FIGS. 42A and 42D. FIG. 42A shows a sector shaped pad 132. The sight lines for a top view T, an edge view E and a side view S are indicated by arrows labeled T, E and S, respectively. FIG. 42D shows a circular pad 20. An example of a typical radial bearing pad is shown in FIG. 42B. Again, the arrows indicate the sight lines for the top view T, edge view E and side view S, as discussed below. Finally, one form of combined radial/thrust pad 1032 is shown in FIG. 42C. The arrows indicate the sight lines for the top view T, edge view E and side view S discussed below. These pad shapes are all characterized by uninterrupted planar surfaces and a uniform pad thickness.

Various modifications to traditional thrust, radial and combined radial/thrust pad shapes will be discussed hereinafter. It should be kept in mind that any of these modifications to the shape of the pad may be used in combination or alone. Also, the modifications can be easily adapted to pads having shapes other than the specific pad shapes illustrated. Moreover, the pads may be symmetrically shaped to allow bidirectional operation or non-symmetrical to provide different operating conditions depending on the direction of rotation. The modified pad shapes discussed hereinafter may be used in combination with any support structures including those described in this application where appropriate or, when used in the proper combination, may eliminate the need for a moving support structure altogether.

The first possible modification to the general pad shape is shown in FIGS. 43A-E. These figures illustrate the modification as applied to thrust bearing (FIG. 43A), a radial bearing (FIGS. 43B-C) and a combined radial/thrust bearing (FIGS. 43D and 43E).

This modification is based on finite element analysis which has shown that, in some instances, increasing the length of the edge where the lubricant enters (the leading edge) can improve bearing performance. Specifically, lengthening this edge allows more lubricant to be directed toward the pad center. To achieve this effect a radius cut may be formed on the pad surface to lengthen the leading edge. The cut may be formed either entirely through the pad or partially through the pad surface to provide a recess in the pad surface. Such a radius cut may be provided in a thrust bearing, a radial bearing or a combined radial/thrust bearing. It should be kept in mind that the provision of such a radius cut decreases the load bearing surface of the pad. Thus, there is a trade off; more lubricant but less load bearing surface.

FIG. 43A shows a top view of a thrust bearing pad 132 in which a radius cut 132C is formed as shown. In the illustrated embodiment, the cut 132C is provided on each edge of the pad 132. This is because the illustrated pad is intended for bidirectional use and the improved result is desired in both directions. If unidirectional operation is sufficient, the cut should only be provided on one edge.

FIGS. 43B and 43C show side and top views respectively of a radial bearing pad 32 formed with radius cuts 32C at each edge. Again, the provision of the radius cuts 32C increases the amount of lubricant entering the pad center at the same time reducing the load bearing surface area of the pad. The radial bearing shown in FIGS. 11B & C is also a bidirectional pads since it is symmetrical with radius cuts 32C formed in each edge.

FIGS. 43D and 43E show a combined radial/thrust bearing pad 1032 supported on an angled support structure 1037 schematically illustrated as a conically tapered block. FIG. 43D is an edge view and FIG. 43E is a top view. Again, the pad is symmetrical and a radius cut 1032C is provided on each edge of the thrust bearing pad to allow bidirectional operation.

FIGS. 44A-D illustrate another possible modification to the basic pad shape. Specifically, it has been learned that tapering the leading edge of the bearing pad results in increased inlet bending. This allows more lubricant to enter into the shaft-pad space which increases the load carrying capability of the pad. Complex finite element analysis using computers can predict the amount of bending needed to obtain optimum lubricant flow.

The drawings illustrate the use of tapered edges in thrust, radial, and combined radial/thrust bearings. Specifically, FIG. 44A is a side view along the S axis in FIG. 42A illustrating a thrust bearing pad 132 with a taper 132t formed at each edge. Again, the taper is provided at each end to allow for bidirectional operation. FIG. 44B shows a side view of a radial bearing pad 32 with a taper 32t formed at each edge thereof to allow bidirectional operation. Finally, FIGS. 44C and 44D illustrate edge and side views of a combined radial/thrust bearing pad 1032 with tapers provided on each edge to increase inlet bending. Of course, if unidirectional operation is sufficient, only one edge, the leading edge, should be tapered.

The basic pad shape may also be modified by providing rails on the side edges of the pads such that, under load, the pad moves to form a channel which retains lubricant on the pad face and minimizes end or side leakage.

Examples of pad shapes so modified are shown in FIGS. 45A-C. FIG. 45A shows an edge view of a thrust bearing pad 132 provided with side edge rails 132r on the radially inner and outer edges. The movement of this pad under load (greatly exaggerated) is indicated in phantom. As can be seen, the pad moves under load to form a lubricant retaining channel.

FIG. 45B shows a radial or journal bearing pad 32 provided with side edge rails 32r on its axial edges. The movement of the pad under load, again greatly exaggerated, is illustrated in phantom. As is apparent from this exaggerated example, the pad deforms under load to form a lubricant retaining channel to prevent leakage of lubricant along the axial ends of the bearings.

FIG. 45C shows a combined radial/thrust bearing pad 1032 formed with rails 1032r on its inner and outer edges. The movement of the pad under-load (greatly exaggerated) is indicated in phantom. As is apparent from this exaggerated view, the pad deforms under load to form a lubricant retaining pocket so that lubricant does not escape from the radially inner and outer edges of the pad 1032.

As mentioned before with reference to FIGS. 44A-44D, it is sometimes desirable to increase the inlet bending of the leading edge of a bearing pad. Another modified bearing pad shape for achieving or enhancing this desired result is shown in FIGS. 46A-46C. Specifically, these drawings show that in addition to or instead of tapering the leading edge, a groove may be formed on the lower edge of the lower side of the pad proximate the leading edge to cause increased leading edge bending while maintaining a flatter surface. FIG. 46A shows a thrust pad 132 with grooves 132g formed in the bottom near both edges to allow bidirectional operation. FIG. 46B shows a radial bearing pad 32 with grooves 32g formed on the outer surface proximate each side edge. FIG. 46C shows a combined radial/thrust bearing pad 1032 with grooves 1032g formed in the bottom surface thereof near each edge.

Another consideration in the design of hydrodynamic pads is that the pads themselves may be formed from a single member by simply providing grooves to define individual pads. Examples of this are shown in FIGS. 47A-47C. FIGS. 47A-47B show how a continuous surface can be divided into individual thrust pads 132 through the provision of pad defining grooves 132p. In this case, FIG. 47A is a top view and FIG. 47B is a side view along the lines indicated in FIG. 47A. For a combined radial/thrust bearing the construction is essentially the same as that shown in FIG. 47A. FIG. 47C illustrates how a cylindrical body may be divided into individual journal pads 32 through the provision of pad defining grooves 32p on the radially inner surface thereof.

A final consideration in the design of specific pad shapes is the provision of bottom recesses on the pads. Specifically, the provision of bottom recesses can cause channeling in a manner somewhat like that shown in FIGS. 45A-45C and allow inlet bending in a way such as the tapered structure shown in FIGS. 44A-44D. Examples of bottom recesses formed in pads designed for unidirectional operation are shown in FIGS. 48A-48D. FIGS. 48A-48B show top and side views of a thrust bearing pad 132 formed with a bottom recess 132b to cause channeling. The reduced pad area also enables compressive movements onto the bottom surface which develops a converging wedge. Since this modification is provided on only one edge of the pad 132, the pad is intended for use in a unidirectional bearing. The pad construction shown in FIGS. 48A and 48B is essentially the same as would be used for a combined radial/ thrust bearing. The only difference is that the pad would be formed of a conical section.

FIG. 48C shows a radial bearing pad 32 provided with a bottom recess 32b on one edge thereof. Again, this is a unidirectional bearing.

FIGS. 49A-49C illustrate bearing pad configurations similar to those shown in FIGS. 48A-48C except that the bottom recesses 132b are provided at both edges of the bearing pad so as to permit bidirectional operation. Specifically, the thrust or combined radial and thrust bearing pad 132 shown in FIGS. 48A and 49B includes bottom recesses 132b at each edge thereof. As is apparent by comparing FIGS. 49A-49B with FIGS. 48A-48B, the bottom recesses are somewhat smaller to accommodate the provision of such recesses at each edge.

Likewise, in FIG. 49C the radial bearing pad 32 includes bottom recesses 32b at each edge thereof. Again, the recesses are somewhat shorter than the recesses provided in the unidirectional bearing shown in FIGS. 48C.

As mentioned before, the design of a pad shape for any particular application depends on the requirements of that application. The foregoing structural modifications and considerations can be used alone or in combination. FIGS. 50A-50C and 51A-51C show how all these features can be combined in a single bearing. This is not to suggest that all these features should necessarily be included in every design. Indeed, this would rarely be required. However, it is possible to combine all these features in a single bearing, if desired.

FIG. 50A shows a top view of a thrust bearing or combined radial/thrust bearing in which the bearing pads 132 are provided with radius cuts 132C to increase the length of the leading edge. The radius cuts 132C are provided on each edge so as to permit bidirectional operation. Of course, if desired, the radius cuts 132C can be provided on only one edge to provide optimum results for unidirectional operation. In FIG. 50A, the individual pads 132 are defined by pad defining grooves 132p.

FIG. 50B shows a bottom view of the thrust bearing of FIG. 50A. In this view, it can be seen that the bearing includes bottom rails 132r, grooves 132g to increase inlet bending, a taper 132t to further increase inlet bending and a bottom recess 132r to further channel liquid and increase inlet bending. In this case, the grooves, taper, and recesses collectively provide the desired movement.

FIG. 50C is a cross-section of the bearing of FIG. 50A along the lines indicated in FIG. 50A. FIG. 50C also shows the bearing mounted on a support structure 137. The support structure is shown schematically as a box to indicate that, in accordance with the present invention, any of the support structures disclosed herein can be used. As noted above, it is possible through proper pad design to obviate the need for a moving support structure. In such a case, the support structure could be rigid, e.g., the housing. Alternatively, however, the support structure can be a moving support structure of any of the types disclosed herein having primary, secondary and tertiary support portions for supporting the bearing pads for movement with six degrees of freedom. Likewise, the pad modifications discussed herein are generally applicable individually or in combination to the bearing pads of any of the bearings disclosed herein.

FIG. 51A shows a top view of a journal or radial bearing pad 32 having a radius cut 32C formed in each edge thereof to increase the length of the leading edge. This increases the amount of lubricant passing on to the bearing pad surface.

FIG. 51B shows a side view of the bearing pad 32 of FIG. 51A. From this view, it is possible to see the radius cut 32C formed on the top surface of the pad, the taper 32t formed at the bottom edges of the pad, the bottom recess 32b formed on the bottom side of the pad, the grooves 32g formed on the bottom side of the pad and the rails 32r extending radially outward from the bottom surface of the pad.

FIG. 51C shows the bottom view of the bearing pad of FIGS. 51A & 51B in which the bottom rails 32r, the grooves 32g and the bottom recess 32p are apparent. If desired, a bearing having pads of the type illustrated in FIGS. 51A-51C could be formed from a single piece with the pads separated from one another by pad defining grooves as shown in FIG. 47C.

Another complete bearing design is depicted in FIGS. 52A-52C. These drawings depict a washer-like thrust bearing in which the desired pad shape is obtained in an extremely thin washer-like cylindrical element. FIG. 52A is a bottom view of the washer-like bearing showing circumferentially spaced bottom recesses 132b and grooves 132p (in phantom) which define a plurality of circumferentially spaced thrust pads 132. The cross-section of the grooves 132p and bottom recesses 132b is best illustrated in the cross-sectional view of FIG. 52B. As shown in this figure, the grooves 132p and 132b are very shallow. Finally, FIG. 52C shows a top view of the washer-like thrust bearing in which the circumferentially spaced pad defining grooves 132p are depicted and the bottom recesses 132b are shown in phantom.

As previously discussed, the pad defining grooves 132p define a circumferentially spaced series of bearing pads 132. The bottom recesses 132b undercut the pad surface to a sufficient extent that the portion of the thrust pad surface that is undercut can move slightly downward so as to form a conveying wedge and a lubricant retaining channel. Collectively, these movements result in the formation of a series of converging wedges so that the shaft runner is supported on a layer of pressurized fluid film. Further, because of the nature of the bottom recesses 132b the lubricant is retained on the pad surface and does not escape from the radially inner and outer edges of the pad. Finite element analysis has shown that, under sufficient load, this simple washer will move so as to operate as a multiple pad hydrodynamic bearing even without a moving support structure. Thus, a simple washer-type bearing pad configuration of the type shown in FIGS. 52A-52C can be mounted on a rigid support structure and still obtain satisfactory results. Of course, a moving support structure could be used, if desired.

An important aspect Of the present invention is the disclosure of machinable bearing shapes i.e., bearing shapes which can be produced by machining a piece of heavy walled tubing or similar cylindrical journal using standardly available machining techniques. Such bearings are characterized by the fact that they are formed from a piece of heavy walled tubing or similar cylindrical journal through the provision of bores, slits and grooves. The advantage of such bearings is that it is easy to manufacture prototypes and to modify these prototypes after testing. Naturally, when the bearings are to be mass produced, using, for example, molding or casting techniques, different manufacturing considerations may dictate different shapes. It is important to recognize that changes in shape affect bearing performance.

Another manufacturing consideration is ease of molding. Naturally, most of the bearing constructions of the present invention are capable of being molded by some molding technique. However, only certain shapes can be injection molded in a simple two-piece mold, i.e., a mold which does not include cams. Another advantage of the bearings of the present invention is that the bearings can be constructed with easily moldable shapes which are defined as shapes which can be injection molded using a simple two-piece mold. An easily moldable shape generally is characterized by the absence of "hidden" cavities which require cams for molding. For instance, with respect to radial bearings, an easily moldable shape includes no radially extending grooves in the inner and outer diameter and a continuous axial cross section. The bearing shown in FIGS. 32, 32A and 32B is an example of an easily moldable radial or journal bearing.

Similarly, easily moldable thrust bearings are characterized by the fact that they can be molded with a single seam line such that, for example, when viewed only from the top and bottom, all surfaces are visible.

FIGS. 38A-38C illustrate an easily moldable thrust bearing. The bearing includes a plurality of circumferentially spaced bearing pads 132m and a support structure supporting each of the bearing pads 132m. The support structure includes a primary support portion which includes circumferential beams 134mb and 134ma, a secondary support portion which includes radially extending beam 136m and a tertiary support portion which includes the stub-like pair of beams 138m. It should be noted that, in FIGS. 38A-38C, the dimensions of the support structure are somewhat distorted to provide clarity. For instance, as shown in FIG. 38C, the circumferential beams 134ma and 134mb are shown as extremely thick. Such the beam structure would provide a very rigid support for the bearing pads 132m and in practice, such a rigid support would probably not be necessary or desirable.

Variants of the specific moldable beam structure illustrated are possible. For instance, either or both of the spaced circumferential beam segments 134ma or 134mb could be formed as a continuous circumferential beam element. Additionally, the secondary support portion could include a plurality of radially extending beams between each bearing pad 132m. Further, the primary support structure could be modified to include three or more circumferential beam segments connecting each pair of adjacent bearing pads and/or circumferential beam segments; also, segments of different radial widths could be used. Further, the stub-like beam portions 138m could be provided along the radially extending edges of the beams 136 rather than the circumferentially extending ends. Finally, as with any bearing in accordance with the present invention, the structure could also be varied by varying the length or thickness of any of the elements in the support structure to modify the movement characteristics of the support structure.

In order to illustrate a number of possible support structure constructions, FIG. 38D depicts a different support structure for each of the bearing pads 321m-326m. In particular, FIG. 38D is a bottom view with the modifications illustrated herein. It should be understood that these various support structures are shown in a single bearing for purposes of illustrating the present invention. In normal use, each of the bearing pads 321-326m would have a similar, though not necessarily identical, support structure to assure uniform performance.

The support for bearing pad 322m differs from that for the bearing pads 132m in that an oval shaped projection extends from the back of the bearing pad surface to provide a rigid support for the outer circumferential edge of the bearing pad 321m. By virtue of this construction, the bearing pad 321m would be extremely rigid at its outer circumferential end.

The support for bearing pad 322m is similar of that to 321m except that rather than a single large projection, two smaller projections 122m extend from the bottom of the bearing proximate the outer circumferential edge of the bearing pad. Like the projection 120m, these two projections 122m provide rigidity to the outer circumferential edge of the bearing pad 322m. However, this construction allows the bearing to move in the unsupported region between the projections.

The bearing pad 323m is supported by modified support structure which includes a continuous circumferential beam 134ma in the primary support portion. Similarly, the bearing pad 324m includes a continuous inner circumferential beam 134mb. The provision of such continuous beams increases the rigidity of the bearing support structure.

The support structure for bearing pad 325 is modified by the provision of large openings 142m in the inner beam 134mb and smaller openings 144 in the outer beam 134ma. The provisions of these openings increase the flexibility of the beams. Naturally, the larger openings increase the flexibility of the beams to a greater extent than the small openings 144. Variants of this support structure include the use of different sized openings or a different number of openings to bias the bearing pad 325m in a predetermined direction.

The bearing pad 326m is supported by a modified structure in which the primary support portion includes a membrane 134m rather than a pair of beams. In the illustrated example, one of the membranes is provided with a opening 146 to bias the bearing pad 326m in a predetermined direction. Of course, the provision of the opening 146m is not necessary and if desired, a number of openings could be provided.

As is evident from these drawings, the moldable bearings do not include any hidden cavities which would necessitate the use of a complex mold and/or a mold including a displaceable cam. In particular, since each surface of the bearing structure is directly visible in either the top view of FIG. 38A or the bottom view of FIG. 38B, the bearing can be simply molded using a two piece mold. Specifically, a first mold piece defines those surfaces which are directly visible only in the top view of FIG. 38A. The second mold piece defines those surfaces which are only visible in the bottom view of FIG. 38B. Surfaces having edges visible in both FIGS. 38A and 38B can be molded using either or both molds. In the illustrated bearing, easy moldability is achieved because the secondary and tertiary support portions are circumferentially located in the space between bearing pads. The modifications illustrated in FIG. 38D do not alter the easy moldability of the bearing.

More complex variants of the moldable thrust bearing illustrated in FIGS. 38A-38D are possible. In particular, any of the previously discussed modifications of the bearing structure which can be adapted to easy molding could be employed. For instance, the primary support beams could be continuous. Thus, the provision of an easily moldable bearing does not necessarily require a simple bearing construction. An example of a more complex bearing structure is illustrated in FIGS. 39A-39C.

As illustrated in FIGS. 39A-C, the bearing includes a plurality of circumferentially spaced bearing pads 232m supported by a bearing pad support structure. The secondary and tertiary portions of the support structure are similar to corresponding portions of the bearing support structure of FIG. 38. However, the bearing of FIG. 39 differs from the bearing of FIG. 38 in that, in the bearing of FIG. 39, the primary support portion includes a plurality of complex beams 234. Specifically, each bearing pad is supported by a radially outer continuous complex circumferential beam 234ma. The pads are further supported by the plurality of spaced circumferential complex beams 234mb. The complex shapes of the continuous beam 234ma and the beam segments 234mb can be best appreciated with reference to FIG. 39C which shows, somewhat schematically, the profile of the complex beams 234. In operation, the beams 234ma and 234mb function as a beam network. Thus, it can be seen that numerous complex thrust bearing constructions can be provided while retaining the ability to mold the bearing with a simple two-piece mold, i.e., easy moldability. Naturally, each structure provides unique movement characteristics which must be considered in designing the bearing for optimum wedge formation.

In certain gas or air lubricated movable pad bearings, there are cases where loads or speeds exceed the capability of an air film. In these cases, it is necessary to introduce a liquid type lubricant into the converging wedge without providing a liquid reservoir or bath. FIGS. 40, 40A, 41 and 41A illustrate bearing constructions for achieving this purpose. In particular, these drawings illustrate a novel self-lubricating movable pad bearing in accordance with another important aspect of the present invention. The bearing is essentially a movable pad bearing of the type described herein which has been modified to include lubricating plastic in its various openings.

The plastic employed in the bearing is a conventional castable porous plastic which is capable of absorbing lubricating liquid when soaked in such a liquid. One such plastic is sold under the trade name POREX.TM.. Generally, the porous plastic can be formed from various plastics by injecting air into the plastic material to form the pores. In particular, the liquid is absorbed into the porous plastic in a wick like manner and held in place by the plastic.

The lubricating movable pad bearing is constructed by taking a conventional journal, thrust or combined radial and thrust movable pad bearing of the type described above and casting or injecting the conventional porous plastic around and into the spaces between the movable members. As a consequence of this construction, during operation, the movement of the shaft and the compression of the movable members causes the lubricating liquid to leave the porous plastic and to be drawn into the leading edge of the converging wedge. The formation of the liquid filled wedge greatly increases the load and speed capability of the bearing. After the liquid passes over the pad surface, it is reabsorbed by the porous plastic after leaving the trailing edge.

An important aspect of the present invention is the composite structure combining a standard bearing material with the porous plastic. By virtue of this composite, it is possible to take advantage of the unique characteristics of both materials. More specifically, conventional porous plastics alone make poor movable pad bearing materials because the pores in the plastic are actual voids that are detrimental to the development of the very thin fluid film. On the other hand, conventional plastic or metal bearing materials not having the pores are incapable of absorbing lubricant to any great extent. However, through the use of both materials in the manner described, an effective self-lubricating hydrodynamic bearing can be obtained. Further, there are synergistic results from the combined use of standard bearing material and lubricant absorbing porous plastic. For example, the movements of the bearing surface assist in forcing the liquid lubricant into the leading edge. Moreover, channelling or lubricant retaining deformation of the bearing surface assists in containing the liquid.

FIGS. 40 and 41 show two examples of the self-lubricating movable pad bearing of the present invention. In particular, these drawings show bearings similar to bearings described previously which have been modified to include the liquid absorbing porous plastic filled into the spaces between the movable members. To some extent, the bearing acts as a skeletal portion and the porous plastic portion acts as a lubricant retaining and releasing sponge.

In particular, FIGS. 40 and 40A show a self-lubricating bearing having an underlying bearing structure which is essentially identical to the bearing shown in FIGS. 32 and 32A. However, the bearing structure of FIG. 40 is modified such that porous plastic fills the openings between the bearings and the openings within the support structure which are continuous with the spaces between the bearing pads 732. Naturally, the spaces under the bearing pads could be filled with porous plastic as well. However, unless there is communication between the porous plastic and the bearing pad surface, the provision of such porous plastic areas would be fruitless.

Likewise, FIGS. 41 and 41A show a bearing having a construction virtually identical to the construction of the combined radial and thrust bearing shown in FIGS. 36 and 37. However, porous plastic is again injected into the interstices or spaces within the support structure between the pads. Again, the injection of the porous plastic as illustrated results in a bearing having a continuous inner diameter. However, like the bearing of FIG. 40, the material characteristics across the inner diameter vary significantly.

Specifically, like the bearing of FIG. 40, the inner diameter of the bearing of FIG. 41 includes wedge supporting bearing pad surfaces and circumferentially spaced lubricant releasing, absorbing and retaining portions. In operation, the movement of the shaft and the compression of the movable members causes the lubricating liquid to leave the porous plastic and to be drawn into the leading edge of the converging wedge. The formation of the liquid filled wedge greatly increases the load and speed capability of the bearings.

The manufacture of the self-lubricating movable pad bearing involves three general steps. First, the basic bearing or skeletal portion is formed of standard bearing material. Second, the porous plastic is injected into the desired spaces in the bearing structure. For purposes of manufacturing convenience, the plastic is injected into the bearing without lubricant. Finally, the bearing, with the porous plastic injected into the desired spaces, is loaded with liquid lubricant. To properly load the plastic with liquid lubricant, it is necessary to work the lubricant in from one side. The merging in the liquid results in an unfilled internal portion. This is caused by not allowing the pores to vent from one side. In FIG. 40, the basic bearing structure is combined radial and thrust structure similar to that shown in FIG. 36. However, porous plastic fills the interstices within the support structure. The provision of the porous plastic yields a composite bearing having a continuous inner diameter surface. However, the movement characteristics across the surface vary greatly. Specifically, the movable pads, which are formed of standard bearing materials such as metal or non-porous plastic, are suited for movement and formation of a fluid wedge. On the other hand, the porous plastic portions are suited for compression so as to release lubricant at the leading edge of the bearing pads and absorbing lubricant at the trailing edge of the bearing pads.

As noted with respect to each of the illustrative examples described above, the bearings of the present invention can be formed to provide for a wedge ratio of 1:2 to 1:5, have a deformable bearing surface the shape of which can be modified, allow six degrees of freedom of the pad, and provide a dash pot type damping action. The bearings are typically of a unitary construction.

By virtue of the wedge formed by movement of the bearing pad and the ability of the pad to move with six degrees of freedom, the bearing of the present invention exhibits exceptional performance characteristics. Specifically, the bearing dimensions and movement variables including number, size, shape, location and material characteristics of the elements defined in the unitary bearing can be tailored for any specific application to support a wide variety of loads. Of these variables, the shape of the support members is particularly important. The impact of shape of the support members on the movement characteristics of the support structure can be appreciated when the variable formula for moment of inertia bh.sup.3 /12 (English units) (the main component of sectional modulus for rectangular section, z=I/c=bh.sup.2 /6) is used as an example. Moreover, the ability of the pad to move with six degrees of freedom allows the bearing to compensate for and correct shaft misalignment. In this regard it is noted that the bearings of the present invention have a self-correcting characteristic resulting from the tendency of the bearing to return to its non-deflected state due to the stiffness of the bearing. Of course, the stiffness of the bearing is primarily a function of the shape of the support structure, and to a lesser extent the other movement variables, including number, size, location, and material characteristics of the elements defined by the grooves and cuts or slits formed in the unitary element. Stiffer bearings have a greater self-correcting tendency but are less able to adjust for shaft misalignment.

Tests have shown that bearings incorporating the features of the present invention exhibit dramatically improved performance even in comparison to the structure disclosed in the present inventor's prior U.S. Pat. No. 4,496,251. In a recent test, the journal bearings of the present invention were utilized in a radial bearing with a radial envelope of 0.091"(2.31 mm). Inward movements of the bearing pad were 0.0003"(0.0076 mm) which provides exceptional stability and bearing performance. A comparable displacement using the arrangement shown in the present inventor's prior U.S. Pat. No. 4,496,251 would have required a radial space of 0.30"(7.6 mm).

In conventional hydrodynamic journal bearings, it is typically necessary to provide a fluid-film clearance between the bearing pad surface and the shaft portion to be supported. This requires extremely close manufacturing tolerances which can present an obstacle to high volume production.

The bearings of the present invention can be designed to obviate the need for such close manufacturing tolerances. Specifically, by providing appropriate bores, grooves and cuts or slits, it is possible to define a bearing having virtually any desired performance characteristic. One such characteristic is the stiffness or spring characteristic of the bearing pad in the direction of load, i.e., in the radial direction (radial stiffness) with respect to journal bearings and in the axial direction (axial stiffness) with respect to thrust bearings.

It is known in the bearing art that the fluid film between the shaft and the bearing may be modeled as a spring since it has a calculatable radial or axial fluid film stiffness or spring characteristic. This is true for both compressible and incompressible fluids but is particularly useful in regard to gas fluid lubricants. The fluid film stiffness and the bearing stiffness act in opposition to one another such that if the fluid film stiffness or spring characteristic exceeds the bearing stiffness or spring characteristic, the bearing will move in the direction of the fluid film stiffness (i.e., radial direction for journal bearings and axial direction for thrust bearings) until the stiffness of the fluid and the bearing are in equilibrium. Thus, it has been found that if a journal bearing is designed such that radial stiffness of the bearing is less than the radial stiffness of the fluid film, it is not necessary to provide a precise spacing between the shaft and the bearing because the radial stiffness of the fluid film will automatically and instantaneously, upon rotation of the shaft, cause appropriate radial movement of the journal bearing. The virtually instantaneous wedge formation results in virtually instantaneous formation of the protective fluid film, thereby preventing damage to wedge forming surface which typically occurs at low speeds during the formation of the fluid film.

The radial stiffness of the bearing is, of course, primarily a function of the section or flexure modulus of the support structure which depends on the shape of the support structure. The radial stiffness of the pad also depends on the length of the slits or cuts formed in the bearing. The same is true of thrust bearings except, naturally, the axial stiffness of the bearing is critical. Accordingly, with the present invention, it is possible to achieve high performance without the close manufacturing tolerances typically required of hydrodynamic bearings.

For example, the bearings of the present invention may be designed to have an interference fit when installed on the shaft such that as the bearing is forced on the shaft, the pads move slightly so as to form a converging wedge shape while in the stationary installed position. The trailing edge bearing pad contacts the shaft. At instantaneous start up, the fluid film enters the wedge and builds up fluid pressure causing separation of the shaft and pad. Thus, in accordance with another important aspect of this invention, the bearings of the present invention may be designed and dimensioned such that the trailing edge of the bearing is in contact with the shaft portion to be supported when the shaft is at rest.

FIG. 1C shows a side-view of a three pad positive-centering movable pad bearing for use in applications where floating of the axis of rotation must be minimized or eliminated. As shown in FIG. 1C, the bearing includes two different types of bearing pads: circumferentially short pads indicated at 32 and circumferentially long pads indicated at 31. The short pads 32 operate as flexible centering pads. These pads begin at zero clearance, i.e., shaft contact and expand at design speeds under hydrodynamic pressure to a larger operating clearance. The larger, centrally pivoted pads 31 offer low pivot rotational stiffness and high radial stiffness to attenuate unbalanced response and maintain stability.

The operation of the larger centrally pivoted pads 31 is similar to tilt type pads described above in connection with FIGS. 1A and 1B. The pads 31 are supported by a single ligament 37 for simple flexibility in the plane of the paper of the drawing. It is critical, however, that the ligaments be so thin as to offer virtually no resistance to pivots. At a minimum, the radial length of the ligaments should exceed their circumferential width. In essence, the larger pads 31 have a support structure 37 which allows simple pivoting of the pad 31. It is known that a simple pivoting construction like this provides adequate support at operational speeds.

To ensure proper shaft centering and support at start up, the smaller pads 32 have a more flexible support structure. Specifically, the support structure of the pads 32 includes a primary support portion 371 in the form of a stub type shaft, a secondary support portion in the form of a elongated circumferential beam 372 and a tertiary support portion 373 in the form of a stub shaft connecting the secondary support portion 372 to the base or outer periphery of the bearing 30. Because of the elongated nature of the beam 372, any force acting on the surface of the pad 32 causes pivoting about a pivot point PP as illustrated in FIG. 1C. This pivot point PP is located circumferentially beyond the trailing edge 32t of the bearing pads 32. As a consequence, any force acting on the pad 32 causes a moment M to be generated in the direction shown in FIG. 1C. This ensures that under static state, contact between the pad 32 and the shaft occurs only at the trailing edge of the pad. In this way, a preformed wedge is formed even in the static state.

Moreover, the contact between the shaft and each trailing edge of each of the pads 32 collectively maintains the shaft center in the proper position. Thus, a hydrodynamic effect occurs immediately upon start up while at the same time the shaft is properly centered and shaft run out does not occur. Thus, this hydrodynamic bearing, unlike known hydrodynamic bearings, can be used in applications where shaft float is unacceptable such as, for example, a mechanical face seal of the gap type. The advantages of hydrodynamic bearings versus rolling element type bearings are set forth above. An additional important advantage occurs at high speed where rolling element bearings are subject to rapid wear, but hydrodynamic bearings perform without wear because there is no shaft-to-pad contact.

The particular bearing construction shown in FIG. 1C includes two types of pads support structures. This provides a wide range of support conditions. It should be understood, however, that bearings could be designed such that each of the pads are supported in the same way. If shaft centering is required, then each support structure should be designed like the support structure of the bearing pads 32 such that the pivoting caused by static load occurs beyond the trailing edge of the pad in the manner shown in FIG. 1C so that under static loading the pads are moved to that only their trailing edge contacts the shaft. This ensures that a preformed wedge is formed and at the same time properly centers the shaft.

The thrust bearings of the present invention can also be designed to provide a statically loaded wedge. In order to provide a statically loaded wedge, the support structure for the bearings is designed such that the bearing pads slope toward the shaft from the radially inner circumferential edge of the bearing pad to the radially outer circumferential edge of the bearing pad. Further, the support structure is designed such that the bearing pad slopes toward the shaft from the radially extending leading edge to the trailing edge. In this way, a statically loaded wedge approximating the optimum wedge is formed. Further, the pad is sloped toward the shaft at the outer circumferential edge so as to provide the desired fluid retaining characteristic. The stiffness of the support structure can also be designed such that an appropriate space in between the pads and shaft is established instantaneously upon rotation of the shaft.

Alternatively, the bearing may be designed such that the entire bearing pad contacts the shaft portion to be supported when the shaft is at rest. This aspect of the present invention is particularly useful in high volume production of the bearings and with bearings using gas lubricating fluids because it allows a much larger variation of machining tolerances. In one example, a 0.003 inch variation can be designed to have an insignificant impact on the wedge whereas conventional machining of known gas bearings require 0.00000x tolerance which can only be attained through the use of sophisticated and expensive machining techniques such as micro inch machining via etching.

In accordance with another aspect of the present invention, the relationship between fluid stiffness and spring rate can be used to provide a self adjusting characteristic to a simple continuous conical combined radial/thrust bearing. Heretofore, the greatest difficulty in getting a simple continuous conical surface combined radial/thrust bearing to work has been the need for precise adjustment and tolerances. The present invention provides a self adjusting radial/thrust bearing which obviates these disadvantages.

The radial/thrust bearing arrangement includes a shaft having a conical runner. The runner may be formed as a part of the shaft or formed separately and rotatably secured to the shaft. The bearing has a continuous conical surface which is similar, but not complimentary to the runner's surface since a complimentary surface would tend to seize. Generally, the bearing surface has a slightly greater diameter than the runner.

The bearing is biased toward the runner by a spring having a predetermined spring characteristic. A hydrodynamic fluid is located between the surface of the shaft runner and the bearing pad surface. The fluid has a calculable fluid film stiffness or spring characteristic. This fluid film stiffness acts in opposition to the force applied by the spring.

When the shaft is at rest, the spring pushes the bearing into contact with the shaft runner. Because the bearing and runner have different shapes this contact occurs along a single line (if the cone angles are equal) or discrete points. Fluid, preferably either air or liquid a lubricant such as oil, fills the remaining space between the runner and bearing. As the shaft begins to rotate, the pressure and stiffness of the fluid increases. Under normal operating conditions, the fluid film has a calculable stiffness when the shaft is at rest. By selecting a spring which has a constant stiffness which is greater than the stiffness of the fluid film when the shaft is at rest, but less than the fluid film stiffness under normal operating conditions, automatic adjustment is achieved. Specifically, when the shaft speed begins to approach normal operating conditions, the fluid film stiffness becomes greater than the spring stiffness, the bearing moves away from the shaft runner until an equilibrium position is reached. At equilibrium, the fluid stiffness is equal to the spring stiffness, the bearing is spaced from the shaft runner and the shaft is supported on a fluid film.

The spring force may be applied by separate washer or coil spring, a separate or integral elastic member or, in the case of the moving support structure bearings of the present invention, an integral beam-like support structure.

In accordance with one aspect of the present invention, it is possible to provide a self adjusting bearing construction in which the bearing surface is in contact with the shaft surface when the shaft is at rest, but the two surfaces are forced apart by a pressurized fluid film when the shaft rotates under normal operating conditions. This is achieved by designing the bearings such that the force tending to push the shaft and bearing surfaces together is less than the counteracting stiffness of the fluid under normal operating conditions. This principle is applicable to multiple pad bearings or continuous surface bearings.

One useful embodiment of this aspect of the present invention is illustrated, somewhat schematically, in FIGS. 53A-53D. Specifically, FIGS. 53A and 53B show a simplified combined radial/thrust support arrangement in which a conically shaped runner 5r is secured to a shaft 5 and a bearing 32 having a conical face is mounted in a housing 10 to support the runner 5r and hence the shaft 5 in both the radial and thrust direction. The bearing 32, for purposes of the illustration, is a simple continuous conical surface. The bearing 32 is typically tapered at the same angle as the runner 5r but is slightly larger so that, at rest, the bearing and runner are eccentric and a wedge shaped space is formed between them. Moreover, when the surfaces contact, they contact along a single line with a converging wedge shaped space extending from each side of the line of contact. The bearing 32 is biased toward the runner 5r by spring 32s. At rest, the surface of the bearing 32 is in contact with the conical surface of the shaft runner 5r. The two surfaces are pressed against one another by the force of the spring 32s and any gravity force. As the shaft 5 begins to rotate, the stiffness of the hydrodynamic fluid increases until the stiffness of the fluid exceeds the force of the spring 32s acting to push the surface of the bearing 32 into contact with the surface of the shaft runner 5r. At that point, the fluid forces the surfaces apart against the bias of the spring 32s and any additional forces until an equilibrium is reached and the shaft runner 5r and shaft 5 are supported on a film of pressurized fluid.

FIGS. 53C and 53D show a combined radial/thrust support arrangement which is similar to that of FIGS. 53A and 53B. However, in this arrangement, the runner 5r is formed at the end of the shaft 5 as shown in FIGS. 53C and 53D. Additionally, the spring in this case is a Belleville type spring washer. The operating principles are the same.

The advantage of such a self adjusting system is that there is no need to maintain close tolerances since the fluid itself balances with the spring force 32s and the other forces to assure proper spacing between the surface of the bearing 32 and the surface of the shaft runner 5r In arranging for a operable balance of spring force versus fluid film stiffness, there are several constraints. For instance, once the fluid to be used is known, the stiffness characteristics of that fluid are fixed since they are physical characteristics. In such a case, the balance must be provided for by selecting an appropriate spring stiffness. The spring force can be provided by any known spring such as a Belleville (initially coned) spring, a spring washer and an elastomeric cushion or, as discussed herein, a beam-like support structure. In FIG. 53A, the spring 32s is indicated schematically as a helical spring. In FIG. 53C, the spring is indicated as a Belleville or initially coned spring. Regardless of the specific type of spring selected, the spring can be designed using known principles to have the necessary spring characteristic to operate as described above. In this way, a very simple and reliable combined radial and thrust bearing arrangement can be provided. Naturally, these principles may be applied to more sophisticated bearing constructions as discussed below.

In small quantities, the bearings disclosed herein are preferably constructed by electrical discharge machining or laser cutting methods. The double lines shown in the drawings are the actual paths of the wire or beam which is typically 0.002-0.060"(0.50-1.52 mm) in diameter. The lubricant that flows into the electrical discharge machined paths acts as a fluid dampener that reduces any vibration or instability at resonant frequencies. In the situations described above where a continuous cylindrical membrane is formed, the damping takes the form of a dash pot that exhibits high damping characteristics. A significant consideration in the design is that the support structure length and direction be oriented to provide the inward movement shown in FIG. 3. Also, minute movements of the pads themselves in the direction of load, as shown in FIG. 9, result in eccentricity changes which further improve bearing performance. It is noted that in Faires, Design of Machine Elements, the distance between the center of the bearing and the center of the shaft is called the eccentricity of the bearing. This terminology is well known to those skilled in bearing design. With the novel approach of tuning or modifying the stiffness of the bearing configuration or structure and particularly the beam to suit a particular bearing application, optimum performance is readily obtained. Recent computer analysis has demonstrated that virtually any stiffness or movement may be accomplished.

As noted above, when manufacturing low volumes or prototypes of the bearings of the present invention, the bearings are preferably constructed by electrical discharge machining or laser cutting methods. Such small volumes or prototypes are usually constructed of metal. However, when higher volume production of a particular bearing is contemplated, other methods of manufacture such as injection molding, casting, powdered metal die casting and extrusion are more economical. In connection with such manufacturing methods, it may be more economical to employ plastics, ceramics, powdered metals or composites to form the bearings of the present invention. It is believed that methods such as injection molding, casting, powdered metal die casting with sintering and extrusion are sufficiently well known that the processes need not be detailed herein. It is also believed that once a prototype bearing is constructed, the method of producing a mold or the like for mass production of the bearing is well known to those skilled in the molding and casting art. Moreover, it is to be understood that only certain types of the bearings of the present invention are adapted to be made in high volumes through extrusion. Generally, these are the bearings that are formed only through the provision of circumferential grooves and radial and circumferential cuts or slits which extend axially throughout the entire bearing, i.e., those bearings having a constant or otherwise extrudable cross-section.

In accordance with another aspect of the present invention, a novel investment casting method has been found to be particularly useful in the manufacture of intermediate quantities, e.g., less than 5,000 bearings. In accordance with this method of manufacture, the first step of the investment casting procedure is manufacture of a prototype bearing. As discussed above and detailed below, the prototype can be manufactured in any number of ways, but is preferably manufactured by machining a piece of heavy walled tubing or similar cylindrical journal. In larger bearings, the cylindrical journal typically is machined using a lathe for forming face and circumferential grooves, and a mill for forming axial and radial bores. In machining smaller cylindrical journals, techniques such as water-jet cutting, laser and wire electrical discharge techniques are generally more suitable. However, in either application, the journals are typically turned and milled to form the larger grooves.

After the prototype bearing is formed, it may be desirable to test the prototype to confirm that the bearing functions in the predicted manner. As a result of such testing, it may be necessary to modify and refine the prototype to obtain the desired results.

Once a satisfactory prototype is obtained, a rubber mold of the prototype is formed. Typically, this step involves encasing the prototype in molten rubber and allowing the rubber to harden so as to form a rubber mold of the prototype. The rubber encasing the prototype is then split and the prototype is removed to yield an open rubber mold.

Once the rubber mold is obtained, it is used to form a wax casting. This step typically involves pouring molten wax into the rubber mold and allowing the wax to harden to form a wax casting of the bearing.

After the wax casting is obtained, it is used to form a plaster mold. This step typically involves encasing the wax casting and plaster, allowing the plaster to harden around the wax casting so as to form a plaster mold.

The plaster mold can then be used to form a bearing. Specifically, molten bearing material, such as bronze, is poured into the plaster mold so as to melt and displace the wax casting from the mold. Thus, the plaster mold is filled with molten bearing material and the melted wax is removed from the plaster mold.

After the molten bearing material is allowed to harden, the plaster mold is removed from around the bearing and a bearing is obtained.

Because this method of manufacture involves the sacrifice of a wax casting, it is known as investment casting or sacrificial casting.

Despite the fact that the investment or sacrificial casting method described above involves sacrifice of a wax casting and the production of both rubber and plaster molds, and is quite labor intensive, it has proven to be cost effective when intermediate quantities, e.g., less than 5,000 units, of a particular bearing are required. The cost effectiveness of this procedure for lower quantity bearing requirements is due to the fact that the molds used in this method are far less expensive to produce than the complex mold required for injection molding or powdered metal casting.

As noted above, the first step in the investment casting method, indeed in any method, of producing bearings in accordance with the present invention is the production of a prototype bearing. In accordance with another aspect of the present invention, the relatively complex journal and thrust bearings of the present invention can be formed using simple manufacturing techniques. Similar techniques are used for both thrust and journal bearings.

With the foregoing in mind, it is believed sufficient to describe the method of making a single journal bearing through the use of electrical discharge manufacturing and machining. It is believed that a description of such manufacture demonstrates the ease with which the relatively complex bearing shapes of the present invention can be achieved.

Each bearing is initially in the form of a cylindrical blank having a cylindrical bore as shown in FIGS. 11A and 11B. The blank is then machined to provide a radial lubricating fluid groove as shown in FIGS. 12A and 12B. For certain applications, it is desirable to further machine the blank to include facing grooves which are preferably symmetrically disposed on the radial faces of the bearings as shown in FIGS. 13A and 13B. The provision of such facing grooves ultimately results in a bearing which is easily torsionally moved. While the groove shown in FIGS. 13A and 13B are cylindrical, it is possible to provide tapered grooves as shown in FIGS. 14A and 14B. As will become evident below, this yields a bearing which exhibits improved movement characteristics by virtue of the angled alignment of the support beams. In this context, it should be noted that it is preferable that the support beams as viewed in FIG. 14A are tapered along lines which converge at a point proximate the center line of the shaft. This ensures that flexibility occurs about the shaft center line by establishing a center of action for the entire system such that the pads may adjust to shaft misalignment. In essence, the tapering of the support beams causes the bearing to act in a manner similar to a spherical bearing by concentrating the support forces on a single point about which the shaft may pivot in all directions to correct any misalignment. The arrows in FIG. 14A illustrate the lines of action of the movement.

Bearings having cross sections of the type shown in FIGS. 12A and 14A are particularly effective at retaining the hydrodynamic fluid. This is because the bearing pad is supported proximate the axial ends of the bearing pad and the central portion of the bearing pad is not directly supported. By virtue of this construction, the bearing pad is supported so as to deform under load to form a fluid retaining concave pocket, i.e. the central portion of the bearing pad moves radially outward. This greatly decreases fluid leakage. Naturally, the degree of pocket formation depends of the relative dimensions of the bearing pad and support structure. A larger fluid retaining pocket could be obtained by providing a thinner bearing pad surface and supporting the pad surface at the extreme axial ends of the bearing pad.

After the cylindrical blank is properly machined as shown in FIGS. 12A and 12B, FIGS. 13A and 13B, or FIGS. 14A and 14B radial and/or circumferential slits or grooves are formed along the radial face of the machined blank to define the bearing pads, the beam supports and the housing. FIGS. 14C and 14D illustrate such grooves formed in the machined blank of FIGS. 14A and 14B. When manufacturing low volumes of the bearings or prototypes of the bearings for use in the construction of a mold, the cuts or slits are preferably formed through electrical discharge manufacturing or through the use of a laser. The machining of the cylindrical blanks to achieve the configurations illustrated in FIGS. 12A and 12B, FIGS. 13A and 13B, FIGS. 14A and 14B or a similar shape can be done through conventional machine tools such as a lathe or the like.

Although the foregoing discussion is specifically directed to journal bearings, the principles apply just as well to thrust bearings. For instance, the thrust bearing shown in FIGS. 15-18 can be formed by machining a section of heavy walled tubing to provide radially inner and outer grooves, facing grooves, axial bores, radial cuts and chamfers so as to define bearing pads and support structure.

The performance characteristics of the bearings of the present invention result from the relative shape, size, location and material characteristics of the bearing pads and the beam supports defined by the bores and cuts or slits formed in the machined blank. These parameters are largely defined by the dimensions and location of the radial circumferential bores, cuts or slits formed in the bearing in conjunction with the shape of the machined blank in which the bores or slits are formed to yield the bearing.

As noted above, while the construction of the bearings of the present invention is most easily understood by reference to the machining process, larger quantities are preferably manufactured through the investment casting method of the present invention, and even larger scale production of the bearings contemplated by the present invention could be more economically performed through injection molding, casting, powdered metal, die casting, extrusion or the like.

In extruding a large number of bearings from a pipe-like cylindrical blank, radial lubricating fluid grooves, as shown in FIGS. 12A and 12B can be provided along the length of the pipe-like cylindrical blank prior to extrusion. However, if facing grooves were desired in the bearing, these can be individually defined after slicing the individual bearings from the extruded and machined blank. For this reason, extrusion might not be a preferred method of producing bearings which require facing grooves to enhance torsional flexibility.

To obtain variable pad geometry in a one-piece design using a single ligament supporting its pad, the ligament must be flexible enough that the pads rotating with the load imposed by the rotating shaft as shown in FIG. 1D. This characteristic, flexural rotation, distinguishes the present invention from other fluid film bearings. The capability of the pad to flex and rotate with the load allows cross coupling stiffness to approach zero as with a tilt pad bearing. This ensures stable operation. The web dimensions depend on the load being applied in a particular application and on other parameters which vary depending on the specific application and material construction of the bearing. The values for the rotational stiffness in a particular application are determined from a stability analysis where the stiffness is varied until a range is reached where the rotational flexibility provides performance comparable to tilt pad bearings. Tilt pad bearings tilt and build a pressure in the oil film which is symmetric around the shaft journal. The bearings of the present invention also tilt, but the tilt is not due to the rolling action as in standard tilt pad bearings. Instead, the tilt in the bearings of the present invention is due to the flexibility of the web section which allows the pad to rotate or tilt and accommodate the applied load. Although specific dimensions depend on the specific application the ligaments should as a rule be longer in the radial direction than they are wide in the circumferential direction.

Having described the method and apparatus of the invention, the following example will serve to illustrate the design of a movable-pad bearing according to the present invention with reference to FIGS. 59-68.

The performance characteristics of such radial bearings can be analyzed as discussed above in FIGS. 55 and 56. As illustrated in FIGS. 55 and 56, once the selected shaft position yields a calculation equilibrium force substantially equal to the specified load, stiffness coefficients Kxx, Kyy, Kxy and Kyx can be calculated.

As shown in FIG. 59, the principle and cross-coupled stiffness coefficients of a four-pad radial bearing design, similar to that shown in FIG. 1A, vary with pad tilt stiffness. The data presented are for a four-pad bearing having a diameter of 3.0 inches, a length of 2.25 inches, a pad arc length of 80.degree., an offset of 0.5 and a preload of 0.3 operating at 10,000 RPM with ISO 32 oil having an inlet temperature of 120.degree. F. under a load of 100 lbf.

As tilt stiffness drops, the cross-coupling terms asymptotically approach zero, which, by definition, yields tilt-pad behavior. At high pad tilt stiffnesses, the cross-coupling coefficients asymptotically approaches high negative fixed-geometry values, giving the much lower stability that is characteristic of fixed-geometry bearings. The principle coefficients vary slightly from the asymmetric (unequal) fixed-geometry values, to symmetric (equal) values that are characteristic of a tilt-pad bearing with load between pads.

The relative stability of various web thicknesses may be illustrated through a simplified stability analysis which models the rotor as a lumped mass orbiting inside the bearing. While not comparable to the comprehensive flexible-rotor stability computation to follow, such a simplified stability analysis is very useful for assessment of relative performance between different bearing designs. FIG. 60 illustrates the bearing stability logarithmic decrement for a 1,000 lb mass revolving at 1,000 RPM inside the above four-pad bearing under varying pad tilt stiffness.

As shown in FIG. 60, the movable pad bearing exhibits unstable fixed-geometry performance with high tilt stiffness, and stable tilt-pad performance at low tilt stiffness. Intermediate stiffnesses reflect transition from fixed-geometry behavior to tilt-pad behavior. In this case, the fixed-geometry behavior results from tilt stiffnesses above approximately 1,000,000 lbf-in, while tilt pad behavior occurs below values of around 10,000 lbf-in. With careful design optimization, the web thickness can be chosen low enough to exhibit tilt-pad stability without becoming overstressed from shaft loads or tilt stresses. The tilt-stresses are low because of the very small tilt angles (less than 0.1 degree) traversed by the pads during operation.

Once additional data is known concerning the rotor design, a more in-depth stability study can be conducted. As an illustration, high-speed compressor requiring bearings with maximum stability characteristics is shown schematically in FIG. 61. B1 and B2 denote first and second bearings, respectively. The rotor type is a high-speed double overhung air driven turbocompressor; the maximum running speed is 135,000 RPM; the impeller diameter is 90 mm (3.5 in); the rotor weight is 2.1 lb.; the rotor length is 8.7 in; and the bearing span is 1.9 in.

The 90 mm turbo-compressor rotor is very lightweight and runs at relatively high speeds, making it inherently susceptible to bearing-induced rotordynamic instability. This requires that the rotor be equipped with bearings of a highly stable design to preclude subsynchronous whirl at higher operating speeds. In addition, it is desirable to improve shaft centering which allows for lower clearances and improves machine efficiency.

In such applications, a bearing design is needed to maintain or improve the stability characteristics of the original bearings, while also providing better shaft centering characteristics. A practical solution is the use of a set of movable-pad bearings that will minimize the destabilizing cross-coupling effects and also provide the needed positive-centering effects through cantilevered secondary pads. A three-pad positive-centering movable-pad bearing appropriate for this application is shown in FIG. 1C.

The three cantilevered centering pads 32 begin at zero clearance and expand at operating speed under hydrodynamic pressure to a larger operating clearance. The larger centrally-pivoted pads 31 offer low pivot rotational stiffness and high radial stiffness to attenuate unbalance response and maintain stability. A parametric study of the movable-pad bearing design geometry can be conducted using the method of the present invention to optimize the bearings for maximum stability, maximum critical speed margins, and minimum unbalance response sensitivity.

FIG. 62 shows a cross section of the rotor model used in the rotordynamic analyses. The scale is in inches and the supported vertical lines represent bearing placement. This model assumes first and second bearing end overhangs of 3.41 inches and 3.37 inches, respectively, and first and second bearing reactions of 0.6 lb and 1.4 lb, respectively. FIG. 63 shows the first, second and third computed undamped modeshapes M1, M2 and M3, respectively. FIG. 64 shows the undamped critical speed map of the rotor model.

The first undamped critical speed (shown in FIG. 64) occurs at approximately 8,000 RPM and has classic rigid rotor conical mode shape (shown in FIG. 63) typical of double overhung machines with short bearing spans. Because nearly all of the modal compliance is in the bearings, rather than in the shaft, the bearing damping is a high percentage of the critical damping, making this a well attenuated mode that is relatively insensitive to unbalance. The amplification factor from the forced response analysis is only 1.0, thus eliminating any unbalance response concerns passing through this critical speed. Since nearly all of the modal stiffness is in the bearings, the first mode is also highly sensitive in both frequency and amplitude to bearing stiffness changes. At 8,000 RPM, this mode is very adequately removed from the running speed of 135,000 RPM for resonance considerations.

The second undamped critical speed occurs at approximately 25,000 RPM and has a "C" mode shape, making it the first flexible rotor mode. Unlike the first mode, the second critical speed is characterized by significant shaft bending, making it less damped than the first mode, and much less sensitive to bearing changes. This is because the bearing damping is now a smaller percentage of the critical damping, yielding a higher amplification factor of 1.6 and a greater unbalance response. Since the bearing modal participation is lower, this mode is less sensitive in both frequency and amplitude to bearing stiffness changes. The generous separation between the second mode frequency at 25,000 RPM from running speed at 135,000 RPM eliminates unbalance response concerns at running speed. However, the higher unbalance sensitivity requires that care is taken to properly balance the rotor to prevent impeller rubs when passing through the second mode during startup and coastdown.

While similar in modeshape to the second mode, the third mode at 210,000 RPM is fundamentally different in nature because it is the first free-free flexible rotor mode, meaning that it is unaffected by bearing stiffness at low stiffness values. The high angular end displacements of this mode introduce high modal stiffness due to gyroscopics, and high modal mass due to rotary inertia. These make the bearing dynamic stiffness ineffective at low stiffness values, resulting in free-free rotor motion and high dynamic amplification factors. As the bearing stiffness is increased to around 10,000 lbf/in, this mode becomes susceptible to bearing stiffness and is raised in frequency like the other modes. Fortunately, at the actual frequency-dependent stiffnesses of the 3-pad bearings (shown in FIG. 64), the third mode is raised well above the maximum operating speed of 135,000 RPM, making it inconsequential if the rotor does not experience excessive overspeed.

A complete flexible rotor stability analysis can also be performed to further optimize the flexure-pivot bearings for assured rotordynamic stability. This involves computation of damped natural frequencies and corresponding logarithmic decrements at the maximum rotor operating speed for a range of bearing dimensions that are varied parametrically until maximum log decrements (stabilities) are achieved. The stability rotor model is the same as the forced response model, with speed-dependent bearing coefficients, gyroscopics, and rotary inertia effects. Two additional cross-coupling terms may be added to include the effects of aerodynamics in the compressor and turbine blades and seals. For a single stage compressor, the aerodynamic cross-coupling may be estimated (approximately) as:

where:

T=torque (lbf-in)

R=Blade mean radius (in)

h=blade axial length at tip (in)

.beta.=cross-coupling factor (20 for high-speed single stage compressor).

For the 90 mm compressor running at 135,000 RPM and 120 hp, the aerodynamic cross-coupling per impeller becomes

FIGS. 65 and 66 show the first and second mode computed logarithmic decrements versus pad tilt stiffness for three bearing radial clearances. In these figures, bearing diameter is 0.55 inches, bearing length is 0.5 inches, pad arc length is 70.degree. offset is 0.5, preload is 0.4, and oil viscosity is 5.times.10.sup.-6 Reyns. Rotor stability is computed at running speed (135,000 RPM). The computed logarithmic decrements must be positive for stable operation, and should generally be above 0.2 for flexible rotors.

As expected, the logarithmic decrements are negative (unstable) for high pad tilt stiffnesses that yield fixed-geometry behavior. As tilt stiffness is decreased, the logarithmic decrements increase asymptotically to three respective positive values that all reflect the stable behavior of a tilt pad bearing. Smaller bearing clearances (Cb) improve stability in the fixed-geometry regime, while larger bearing clearances appear to be better in the tilt-pad region.

Optimum bearing geometry requires a tradeoff between a thick web to support shaft loads, and a thin web to maximize stability. In this case, the shaft weight and unbalance loads are low enough to allow a relatively thin web of 0.020 inches that satisfies both. Table I summarizes the parametric study that reveals the optimum web thickness for an assumed (conservative) shaft unbalance load of ten times the static load (10.0 lbf). Also, for conservatism, the entire 10 lbf load is assumed to be carried by a single pad, rather than shared between several pads as would actually happen. Values shown are for a radial clearance of 0.0020 inches.

Since the logarithmic decrements become satisfactory for web thicknesses below 0.020 inches, and the corresponding unbalance stress of 1,000 psi is also negligible for a 0.020 inch web, the optimum web thickness becomes that of case number 5 in Table I. It will be shown below that the tilt-induced stresses in the 0.020 inch web are also inconsequential.

Other bearing parameters were similarly optimized and are provided in Table II. Table II lists the bearing design parameters for the optimized movable-pad bearings. The movable-pad bearings are installed in the load-between-pad orientation. The final web thickness and radial clearance are 0.020 in and 0.002 in, respectively. A relatively high viscosity oil (1000 SSU @100 F) is used by the customer, requiring an oil flowrate of approximately 1.2 gpm per bearing to carry away the generated heat. The only difference between the turbine and compressor ends is the static gravity loading.

Maximum possible pad tilt rotation occurs when the shaft is forced radially between two pads to its maximum dry-bearing eccentricity as shown in FIG. 67. The resulting pad rotation is a conservative upper bound for the actual (lower) oscillatory pad rotations that occur in response to the orbital journal motion. Therefore, if the upper-bound web stresses in the dry bearing can be shown to be acceptable, then the actual operating stresses that occur as the shaft orbits (from unbalance) at a much lower amplitude are assured to be inconsequential.

A geometric analysis gives the pad tilt rotation as: ##EQU5## For the 90 mm compressor having a shaft radius of 0.275 inches and a radial clearance of 0.002 inches, the maximum shaft sink becomes ##EQU6## This yields a maximum possible dry-bearing shaft eccentricity of ##EQU7## Substituting this into the expression for pad tilt rotation gives ##EQU8## Therefore, the maximum possible induced web stresses are those corresponding to a 0.53 degree (dry bearing) pad rotation.

For an accurate assessment of the corresponding induced web stresses, the 0.53 degree pad tilt rotation was applied to the finite element model illustrated by the system of key points and line segments shown in FIG. 68. Subsequent stress analysis, calculated using FEA, indicates a maximum Von Mises stress of 35,000 psi. Since this is well under the yield stress for tempered Aluminum Bronze of 45,000 psi, there is no possibility of overstressing the pad web statically.

During operation, the pad tilt oscillations will be much lower than the 0.53 degrees computed above for the dry bearing. This is because operating shaft eccentricities from unbalance typically range from 0.05 to 0.05, rather than the maximum possible dry-bearing eccentricity of 2.0 given above. Unbalance response computations indicate that the computed operating orbit amplitudes for the compressor with typical mass unbalance are approximately 0.000004 inches-peak, giving a shaft eccentricity of 0.000004/0.002=0.002. For conservatism, assume the orbit amplitude to be ten times higher, or 0.00004 inches-peak. Substitution of this into a bearing analysis program gives the computed pad tilt angle as 0.068 degrees. Linear extrapolation of the induced static web stress yields the oscillatory web stress as ##EQU9## The total dynamic stress induced in the pad web is the superposition of the 4,480 psi tilt stress and the 1,000 psi radial unbalance load stress given in Table I. To this dynamic stress, an additional static stress of approximately 4,000 psi from the hydrodynamic force induced by the pad preload must be carried. Adding these three together gives the total oscillatory web stress as ##STR1##

With an aluminum, bronze, or similar tempered material, having an endurance stress capability near 36,000 psi, the 9,480 psi oscillatory stress becomes completely inconsequential. Therefore, the pad support web can safely withstand both the maximum static (35,000 psi) and maximum dynamic (9,480 psi) stresses without danger of either a yield or fatigue failure.

Thus, an embodiment of the present invention has been described wherein a specific bearing design is selected having a set of initial bearing parameters. A steady-state analysis can be conducted for the bearing design to determine principle and cross-coupling coefficients. Undamped mode shapes and critical speed maps can also be generated and forced response analysis can be performed, with bearing parameters selected to minimize unbalance response concerns. Using the above-generated coefficients, a complete flexible rotor stability analysis is also conducted. Bearing parameters are modified to provide maximum logarithmic decrement. A stress analysis is also performed to ensure that the maximum static and dynamic stresses do not exceed the limits of the bearing material, and the material or web geometry is accordingly adjusted if such limits are exceeded.

The present invention, therefore, provides for the optimization of bearing parameters. Using such performance characteristics as critical speed maps, mode shapes, forced response, stability and stress analyses as discussed above, bearing web thickness (or any other bearing parameter) can be selected to provide the most favorable bearing performance. Since all criteria are quantitatively defined, the above process is well suited for automated bearing optimization.