US 6,236,895 B1Grant

Reference estimator in a discrete-time sliding mode controller

Issue Date:2001-05-22

•18 Claims

•24 Drawing Sheets

Abstract

A discrete-time sliding mode controller (SMC) controls the motion of mechanical apparatus such as a read head in a disk storage system. The overall control effort is generated by combining a linear control effort with a discrete-time sliding mode control effort generated by switching between gains in order to drive the system's phase states toward a sliding line trajectory. An estimate of a reference is generated and added to the control effort, thereby providing an approximation of the derivative of the reference signal. Estimating the reference signal may be performed by various methods, depending on whether the reference is known, unknown but repeatable, or completely unknown and non-repeatable. A least-mean-square (LMS) algorithm is employed to estimate the reference signal by computing coefficients of a function which minimizes a particular system parameter. If the reference is an unknown, repeatable sinusoid, such as the runout signal in a disk storage device, the coefficients of a synthesized sinusoid may be determined by minimizing the position error phase state. Alternatively, the coefficients of the synthesized sinusoid may be determined by minimizing the sliding mode variable σ_kwhich defines the position of the system phase states relative to the sliding line. For references that are unknown and non-repeatable, an estimate of the derivative of the reference signal is computed, weighted, and added to weighted derivatives of the estimate, where the weights or coefficients of this function are also determined by minimizing the sliding mode variable σ_k.

Metadata

Assignee

Cirrus Logic, Inc.

Inventors

Paul M. Romano
Louis Supino
Christopher T. Settje

Application Information

Application Number:US 09/145,525

Filing Date:1998-09-02

Priority Date:1998-09-02

Art Unit:7

Classifications

IPC:

G05B 1302

Field of Search:

700 71700 40700 78700 45700 28700 77360 7809360 7806438 1531856822318802318135

Patent Drawings (24 sheets)

Description

[0002] This application is a related to U.S. patent application Ser. No. 08/943,997 entitled “Improved Chatter Reduction in Sliding Mode Control of a Disk Drive Actuator” which is hereby incorporated by reference.

FIELD OF INVENTION

[0003] The present invention relates to control systems technology, and more specifically, to a discrete-time sliding mode controller and method and apparatus for estimating a pseudo derivative reference signal for use in generating the control effort.

BACKGROUND OF THE INVENTION

[0004] Sliding mode control (SMC) is a relatively new development in control systems which was first developed in Russia in the 1950's. It is a subclass of Variable Structure Control (VSC), control systems that switch between structures in a non-linear manner in order to drive phase states of the system toward a phase plane trajectory. The phase states of the system include the position error and its derivatives (velocity, acceleration, etc.); the location of the phase states within a phase plane define the state of the system at any given time, and the movement of the phase states through the phase plane is referred to as the phase state trajectory.

[0005] When the SMC is operating in a first structure, the phase states follow a first phase state trajectory, and when the SMC is operating in a second structure the phase states follow a second phase state trajectory. By switching between the first and second structures, the phase states are driven toward a third phase state trajectory, referred to as the sliding line (or hyperplane for higher order systems), defined within the phase plane where the first and second phase state trajectories intersect in opposite directions. The switching action is controlled by the location of the phase states relative to the sliding line; when the phase states cross the sliding line while following the first phase state trajectory, the system switches to the second structure to drive the phase states toward the sliding line by following the second phase state trajectory. In this manner, the phase states continuously switch across the sliding line as they follow the sliding line toward the origin of the phase plane (i.e., sliding mode). SMC has the advantage in that the closed loop response is defined by parameters in the controller and it is substantially insensitive to parameter variations in the plant and external load disturbances.

[0006] Initially, SMC systems were developed and implemented in continuous-time wherein the phase states are continuously monitored such that the system switches structures instantaneously when the phase states cross the sliding line. An inherent problem with this approach is that the continuous switching action may induce undesirable noise in the system (electrical and acoustic) and it may excite modelled (as well as unmodelled) system dynamics. The above referenced co-pending patent application entitled “Improved Chatter Reduction in Sliding Mode Control of a Disk Drive Actuator” discloses a method for reducing the amount of switching noise by defining a boundary layer around the sliding line and switching between structures only when the phase states exceed the boundary layer. Although this technique reduces the switching noise, there are other inherent problems with continuous-time SMC. Namely, to achieve the desired robustness to parameter variations and external disturbances, it can require gains in the individual structures that exceed the control effort limitations (e.g., exceed the available drive current).

[0007] Discrete-time SMC is a more recent development which addresses the drawbacks of continuous-time SMC by combining a conventional linear control effort with a discrete-time sliding mode control effort. This approach is discussed by Weibing Gao in “Discrete-Time Variable Structure Control Systems,” IEEE Transactions on Industrial Electronics, Vol. 42, No. Apr. 2, 1995. With discrete-time SMC, the phase states are monitored in discrete-time and the system switches between structures at the sampling rate rather than continuously. Thus, there is an inherent boundary layer about the sliding line with a width defined by the sampling period, as well as other parameters of the controller. Rather than switch continuously such that the phase states “slide” along the sliding line, the phase states switch across the sliding line in a zigzag manner while sliding toward the origin of the phase plane. Another characteristic of discrete-time SMC is that nominally the phase states will cross the sliding line at every sampling period, and the absolute magnitude of the distance between the phase states and the sliding line will remain within the inherent boundary layer.

[0008] The position error phase state is typically generated by subtracting an estimated position from a reference position. In disk storage systems, for example, the position error is generated as the difference between the centerline of a target track and the estimated position of the read head. Although the reference position (the track centerline) is static with respect to the disk, the eccentricities of the disk will induce a perturbation into the reference position with respect to the read head, particularly in optical disk storage devices where the media is removable. This perturbation signal is referred to as “runout” and it is typically dominated by a fundamental sinusoid at a frequency equal to the angular velocity of the disk, and a linear combination of the fundamental harmonics. The discrete-time sliding mode control effort is a function of a psuedo derivative of the reference (PDR) signal; it is necessary to generate an estimate of the PDR signal in order to implement a discrete-time sliding mode controller.

SUMMARY OF THE INVENTION

[0009] A discrete-time sliding mode controller (SMC) is disclosed for controlling the motion of mechanical apparatus such as a read head in a disk storage system. The overall control effort is generated by combining a linear control effort with a discrete-time sliding mode control effort generated by switching between gains in order to drive the system's phase states toward a sliding line trajectory. An estimate of the reference is generated and added to the control effort, thereby providing an approximation of the derivative of the reference signal. Various methods are disclosed for estimating the reference signal depending on whether the reference is known, unknown but repeatable, or completely unknown and non-repeatable. A least-mean-square (LMS) algorithm is employed to estimate the reference signal by computing coefficients of a function which minimizes a particular system parameter. In one embodiment, the reference is an unknown, repeatable sinusoid, such as the runout signal in a disk storage device, and the coefficients of a synthesized sinusoid are determined by minimizing the position error phase state. In a similar embodiment, the coefficients of the synthesized sinusoid are determined by minimizing the sliding mode variable σ_kwhich defines the position of the system phase states relative to the sliding line. For references that are unknown and non-repeatable, an estimate of the derivative of the reference signal is computed, weighted, and added to weighted derivatives of the estimate, where the weights or coefficients of this function are also determined by minimizing the sliding mode variable σ_k.

BRIEF DESCRIPTION OF THE DRAWINGS

[0010] FIG. 1 is a block diagram of the disk drive control system of the present invention.

[0011] FIGS. 2A and 2B show an example data format of a magnetic disk comprising a plurality of concentric data tracks with embedded servo fields.

[0012] FIG. 3A shows an example second order system controlled by a sliding mode controller designed using the continuous time existence equation.

[0013] FIG. 3B are the phase plane plots for the position error and error velocity phase states for the positive and negative feedback modes e control system shown in FIG. 3A.

[0014] FIG. 4 illustrates the operation of the sliding mode controller in driving the phase states toward a predetermine linear phase trajectory.

[0015] FIG. 5A is a block diagram of the discrete-time sliding mode controller of the present invention comprising a linear control signal generator and a sliding line signal generator.

[0016] FIG. 5B shows details of the linear control signal generator of FIG. 5A, including a means for estimating the pseudo derivative of the reference signal.

[0017] FIG. 5C shows details of the sliding line signal generator of FIG. 5A.

[0018] FIG. 6 illustrates the zigzag switching action of the sliding mode variable σ_kand the effect on the magnitude of σ_kwhen the plant gain charges.

[0019] FIG. 7 illustrates various regions of operation which defines when the sliding mode variable σ_kwill cross the sliding line on every sample period, and when the system will become unstable.

[0020] FIG. 8A is a block diagram of the discrete-time sliding mode controller comprising an adaptive processor for adaptively adjusting the gain of the plant by minimizing the deviation in the magnitude of σ_kfrom nominal.

[0021] FIG. 8B shows details of the adaptive processor of FIG. 8A.

[0022] FIG. 9 is a flow diagram executed by the adaptive processor of FIG. 8A.

[0023] FIG. 10 is a plot of the analytical versus simulated values of the magnitude of the sliding mode variable σ_kover a range of plant gain variations.

[0024] FIGS. 11A-11D illustrate the step response of the system for various values of plant gain.

[0025] FIG. 12 is a plot illustrating chaotic onset of the discrete-time SMC where the sliding mode variable σ_kdoes not cross the sliding line on successive s periods if the plant gain is too low.

[0026] FIG. 13 is a plot of the chaotic boundary for various values of the slope of the sliding line c.

[0027] FIGS. 4A-14C show the response of the system to various step values when the system is operating near the chaotic boundary.

[0028] FIG. 15A shows a first embodiment for estimating the reference signal in a disk storage device by minimizing the position error phase state.

[0029] FIG. 15B shows an alternative embodiment for estimating the reference signal in a disk storage device by minimizing the deviation from nominal in the magnitude of the sliding mode variable σ_k.

[0030] FIG. 15C illustrates a method for estimating an unknown, non-repeatable reference by minimizing the deviation from nominal in the magnitude of the sliding mode variable σ_k.

DETAILED DESCRIPTION OF THE DRAWINGS

SYSTEM OVERVIEW

[0031] In disk storage systems, such as magnetic and optical disk drives, a write transducer or write head writes digital data onto a disk storage medium in response to a write command received from a host system. The digital data serves to modulate a current in a write coil or an intensity of a laser beam so that a sequence of corresponding magnetic flux or optical transitions are written onto the disk medium in a series of concentric or spiral data tracks. To read this recorded data, a read transducer or read head passes over the disk medium and transduces the magnetic or optical transitions into pulses in an analog signal. These pulses are then decoded by read channel circuitry to reproduce the digital data.

[0032] The read head is typically actuated over the disk by means of a voice coil motor (VCM). In magnetic disk storage devices, the read head comprises a transducing coil suspended by a load beam and actuated radially over the disk by a rotary type VCM. In optical disk storage devices, the read head comprises optics and photodetectors housed in a sled assembly actuated by a two stage servoing mechanism: a first stage VCM actuator slides the sled assembly along a lead screw for coarse positioning the read head over a data track while seeking, and a second stage VCM actuator rotates an optical lens radially for fine positioning while tracking.

[0033] The servo system performs two functions: a “seek” or “access” function in which the servo system moves the head to a selected track; and when the head reaches the selected track, the servo system commences a “track following” or “tracking” function in which it accurately positions the head over a centerline of the track and maintains that position as successive portions of the track pass by the head. Servo control information embedded within the data provides inter-track head position information so that a head position error, indicative of a difference between the estimated head position and the desired head position, can be computed. In response to the head position error, the servo control system generates a VCM control signal to align the head over the centerline of the selected track, thereby driving the head position error to zero.

[0034] FIG. 1 is an overview of the disk drive control system of the present invention. A spin motor 2 spins a magnetic or optical disk 4 with computer data recorded thereon under a read head 6. An actuator 8 positions the read head 6 over a selected track, and a voice coil motor (VCM) 10 controls the motion of the actuator 8. Read channel circuitry 12, connected to receive the analog signal from the read head 6, demodulates the digital data recorded on the disk and transmits servo information to a state estimator 14. The state estimator 14 models the VCM control system in order to generate an estimated actuator position 16 that is subtracted from a reference actuator position 18 at adder 20 to produce an actuator position error X1 22. The reference actuator position 18 is the position of a selected track at which data is to be read (plus a runout signal 28 described below). A sliding mode controller 26, responsive to the actuator position error X1 22, computes an acceleration motor control signal U 28, amplified by amplifier 30, and applied to the VCM 10 to position the read head over the selected track. The state estimator 14 also processes the motor control signal U 28 to generate the estimated actuator position 16.

[0035] The state estimator 14 filters out errors in the servo position information caused by noise in the recording channel. State estimators are well known in the prior art such as described in U.S. Pat. No. 4,679,103, the disclosure of which is hereby expressly incorporated by reference. There are also other well known techniques other than state estimators for generating the actuator phase states for use by the present invention.

[0036] Referring now to FIGS. 2A and 2B, shown is an exemplary data format of a typical magnetic disk storage medium 4 comprising a plurality of concentric data tracks with an inner data track 32 and an outer data track 34. Each data track comprises a plurality of sectors 36 and a plurality of servo fields 38 embedded therein. The servo fields 38 comprise track number information 40 processed by the state estimator 14 to generate the estimated actuator position 16 while seeking the selected track. Once the read head slows to within a predetermined velocity as it approaches the selected track, the state estimator 14 processes the track number 40 and fine position information, such as servo bursts 42 in the servo fields 38, to align the head over the centerline of the selected track while reading the data. Servo bursts are commonly employed in magnetic disk storage devices and comprise a plurality of pulses recorded at precise intervals and offsets from the track centerline. The magnitude of these burst pulses sensed by the read head indicates the off track position of the head. In optical disk storage devices, the off track position information is derived by sensing the read signal's offset from the center of the photodetector.

[0037] In both magnetic and optical disk storage devices, the eccentricities of the disk storage medium may result in a sinusoidal reference signal referred to as runout. In FIG. 1, runout is modelled in the system by adding 24 a runout signal 25 to the position reference signal 27 representing the static centerline of the selected track. Thus, the runout is modelled as a component of the actual reference signal 18 used to generate the read head position error phase state X1 22. As described in greater detail below, it is necessary to derive an estimate of the derivative of the runout signal 25 (if not negligible) in order to enable operation of the sliding mode controller 26 of the present invention.

THEORY OF OPERATION

[0038] Operation of a conventional continuous-time sliding mode controller is understood with reference to FIG. 3A. Shown is an example second order system 44 controlled by an example sliding mode controller 45 that switches 46 between a positive gain 47 and negative gain 48 not necessarily equal in magnitude. A position error X1 49 is generated at the output of adder 50 by subtracting an estimated position 51 of the controlled system from a desired position reference command 52. The position error X1 49 is multiplied by the positive gain 47 or the negative gain 48 depending on the state of switch 46 to generate an acceleration command U 53 as the input to the controlled system 44. The output of integrator 54 is the velocity of the controlled system 44 which is also the negative of the position error velocity −X2 55. When switch 46 selects the positive gain 47, it is a negative feedback system, and when switch 46 selects the negative gain 48, it is a positive feedback system. In their individual structures the system is unstable; however, the system can be made stable by repeatedly switching between the two structures.

[0039] The state space equation in negative feedback is

\begin{matrix} \frac{ⅆ X_{1}}{ⅆ t} = X_{2} \frac{ⅆ X_{2}}{ⅆ t} = - {KX}_{1} & (1) \end{matrix}

[0040] The general solution to equation (1) is

\begin{matrix} X_{1} = A \sin (kt + φ) & (2) \\ X_{2} = \sqrt{K} A \cos (kt + φ) & (3) \end{matrix}

[0041] Combining equations (2) and (3),

\begin{matrix} \frac{X_{1}^{2}}{A^{2}} + \frac{X_{2}^{2}}{{KA}^{2}} = 1 & (4) \end{matrix}

[0042] The phase plane plot of equation (4) is a set of ellipses with eccentricities A and {square root over (KA)} as illustrated in FIG. 3B.

[0043] The state space equation in positive feedback is

\begin{matrix} \frac{ⅆ X_{1}}{ⅆ t} = X_{2} \frac{ⅆ X_{2}}{ⅆ t .} = + {KX}_{1} & (5) \end{matrix}

[0044] The solution to equation (5) is

\begin{matrix} X_{1} = B_{1} ⅇ^{\sqrt{K} t} + B_{2} ⅇ^{- \sqrt{K} t} X_{2} = \sqrt{K} B_{1} ⅇ^{\sqrt{K} t} - K B_{2} ⅇ^{- \sqrt{K} t} & (6) \end{matrix}

[0045] Combining equations (5) and (6),

\begin{matrix} \frac{X_{1}^{2}}{4 B_{1} B_{2}} - \frac{X_{2}^{2}}{4 {KB}_{1} B_{2}} = 1 & (7) \end{matrix}

[0046] The phase plane plot of equation (7) is a set of hyperbolas with two asymptotes as shown in FIG. 3B.

[0047] The two individual phase plane trajectories of equations (4) and (7) result in an unstable system since the phase states never reach the origin. It is possible, however, to reach the origin by driving the phase states along a third phase trajectory defined at the intersection of the negative and positive feedback trajectories. This is achieved by switching between the positive and negative gains in response to the current phase state values so that the phase states follow the predetermined third phase trajectory.

[0048] The switching operation is understood with reference to FIG. 4 where the predetermined third phase trajectory is shown as a linear segment 60. When a new track is selected, the initial actuator position error is at point A, and the control system is initially switched to select the positive gain (i.e., negative feedback). As the actuator begins to accelerate toward the selected track, the phase states follow the arc trajectory 64 of the negative feedback mode. When the phase states reach the beginning of the third phase trajectory 60 at the intersection point B, the sliding mode controller switches to the negative gain and the phase states begin to follow the hyperbola trajectory 66 of the positive feedback mode. When the phase states cross the third phase trajectory 60 at point C, the controller switches back to the positive gain to drive the phase states along arc 68 back toward the third phase trajectory 60. This switching action is repeated so that the phase states slide along the linear segment 60 toward the origin of the phase plane. When the phase states are within a predetermined minimum distance from the origin of the phase plane, the system switches to a tracking mode where the sliding mode controller 26 repeatedly switches between positive and negative feedback in order to maintain the phase states near the origin of the phase plane, thereby aligning the read head 6 over the centerline of the selected track while reading the data.

[0049] The time domain response of the control system when the phase states follow the sliding line of FIG. 4 is

[0050] X1(t)=X1(t1)e^−C(t−t1) (8)

[0051] where t1 is the time when the phase states reach the sliding line at point B. Equation (8) is the average response of the system along the sliding line and it is substantially unaffected by variations in the parameter K or by external load disturbances. Consequently, it is not necessary to know the exact parameters of the system in order to determine the value for K. Equation (8), together with the existence Equation (11) below, demonstrate that the system's response is first order and globally stable within the sliding mode region.

[0052] The sliding mode controller determines when to switch between the positive and negative gains by observing the phase state values. The linear phase trajectory of FIG. 4 is defined by

[0053] X2=−CX1 (9)

[0054] where the constant C is the slope of the linear segment 60. By observing the phase states, the sliding mode controller switches the gains so that

[0055] σ=X2+CX1=0. (10)

[0056] The sliding mode controller switches to the positive gain when σX1>0 and to the negative gain when σX1<0 in order to drive the phase states toward the sliding line.

[0057] The overall response of the system is made faster by increasing the slope of the sliding line (i.e., increasing C). However, an important limitation in sliding mode control is that the sliding must be constrained to a region in the phase plane where the positive and negative feedback phase trajectories intersect in opposite directions. From FIG. 4 it follows that the slope of the sliding line must be constrained to 0<C<{square root over (K)}. A further relationship derived from this constraint is

\begin{matrix} \lim_{σ -> 0} \frac{σ ⅆ σ}{ⅆ t} < 0. & (11) \end{matrix}

[0058] Equation (11) is known as the existence equation and is used to determine values for the positive and negative gains.

DISCRETE-TIME SLIDING MODE CONTROL

[0059] The present invention overcomes the drawbacks of sliding mode control which operates according the above-described continuous-time existence equation (11) by employing discrete-time sliding mode control. Consider a discrete-time system

[0060] X_k+1=ΦX_k+ΓU_k (17)

[0061] where X is a state matrix representing the phase states of the system (position, velocity, acceleration, etc.), Φ is a linear control matrix, and Γ is a scalar. A discrete-time control law is given by

[0062] σ_k+1=λσ_k−Δsgn(σ_k) (18)

[0063] where σ_kis a sliding mode variable computed from discrete-time phase state errors ε_k, λ and Δ are predetermined constants, and sgn(x) returns the sign of x. The discrete-time phase state errors ε_k, such as the position error, velocity error, etc., are computed by subtracting the estimated phase states X_kfrom a reference signal R_k

[0064] ε_k=R_k−X_k (19)

[0065] or by a suitable means for estimating the phase state errors. The sliding mode variable σ_kof equation (18) is computed by multiplying the discrete-time phase state errors ε_kby a vector c which defines the sliding line in the phase plane

[0066] σ_k=cε_k. (20)

[0067] Substituting equation (20) into equation (18) yields

[0068] cε_k+1=λcε_k−Δsgn(σ_k). (21)

[0069] Substituting equations (17) and (19) into equation (21) yields

[0070] c(R_k+1−(ΦX_k+ΓU_k))=λc(R_k−X_k)−Δsgn(σ_k).

[0071] Solving for U_kyields the control law for the servo problem

[0072] U_k=c(Φ−λI)(cΓ)⁻¹ε_k+c(R_k+1−ΦR_k)(cΓ)⁻¹+Δ(cΓ)⁻¹sgn(σ_k). (22)

[0073] Defining

[0074] Ψ=c(Φ−λI)(cΓ)⁻¹; and

[0075] Λ_k+1=c(R_k+1−ΦR_k)(cΓ)⁻¹;

[0076] yields

[0077] U_k=Ψε_k+Λ_k+1+Δ(cΓ)⁻¹sgn(σ_k). (23)

[0078] The control law (23) for the servo problem is a linear combination of the error states, a feed-forward term that requires knowledge of the reference, and a switching term based on the sliding line. Note that for the general regulator problem, the reference term Λ_k+1is normally set to zero for all states which is an accurate model for many systems such as magnetic disk storage systems.

ESTIMATION OF Λ

[0079] The term Λ_k+1in the control law (23) approximates the derivative of the reference signal R_kand is thus called the pseudo derivative of the reference R_k. For a large class of problems, Λ_k+1does not present a significant problem because the phase state trajectories of the system are well defined in an a priori sense, and the system trajectories are controlled in real time by manipulating Λ_k+1. Robotic manipulators are a good example of such systems. However, for a wide class of servo systems direct access to the reference is not available, and only information at the error node(s) may be used to estimate the apparent reference. Magnetic and optical disk storage devices are examples of such systems.

[0080] Equation (22) can be rewritten as

[0081] Λ_k+1=U_k−cΦ(cΓ)⁻¹ε_k+λ(cΓ)⁻¹σ_k−Δ(cΓ)⁻¹sgn(σ_k). (24)

[0082] Using the discrete-time existence equation (18), equation (24) can be written as

[0083] Λ_k+1=U_k−cΦ(cΓ)⁻¹ε_k+(cΓ)⁻¹σ_k+1.

[0084] For most systems where the reference is changing slowly compared to the sample rate, Λ_k+1may be estimated as

[0085] Λ_k+1≈Λ_k=U_k−1−cΦ(cΓ)⁻¹ε_k−1+(cΓ)⁻¹σ_k. (25)

[0086] The accuracy of equation (25) can be improved using a Taylor series expansion

[0087] Λ_k+1≈Λ_k+(Λ_k−A_k−1)/T. (26)

[0088] Equation (25) is a function of the prior control effort, the prior error, and the current value of σ. Other methods could be employed to estimate Λ_k+1, including Kalman Estimators.

HARDWARE DESCRIPTION

[0089] FIG. 5A is a block diagram of the sliding mode controller 26 of the present invention for use in a second order system (the aspects of the present invention can easily be extended to higher order systems). In this embodiment, the sliding mode controller 22 is responsive to two phase state errors, ε1(k) and ε2(k), which may represent a position error and a velocity error of the actuator 8. Various methods are known in the art for generating phase state errors, including the state estimator 14 shown in FIG. 1. The phase state errors are input into a linear controller 90 and a sliding line controller 92, and their outputs are combined at adder 94 to implement the control effort U_kof equation (23). The sliding line controller 92 generates the sliding line variable σ_kwhich is input into the linear controller 90 for use in computing the pseudo derivative reference term Λ_k+1.

[0090] Details of the linear controller 90 of FIG. 5A are shown in FIG. 5B. The error phase states are multiplied 96 by

[0091] c(Φ−λI)(cΓ)⁻¹

[0092] to generate the term

[0093] Ψε_k

[0094] of equation (23). To generate an estimate of the pseudo derivative reference term Λ_k+1, the phase state errors are delayed through delay elements 98A and 98B and then multiplied 100 by

[0095] cΦ(cΓ)⁻¹

[0096] to generate the term

[0097] cΦ(cΓ)⁻¹ε_k−1

[0098] of equation (25). The sliding line variable σ_kis multiplied 102 by

[0099] (cΓ)⁻¹

[0100] to generate the term

[0101] (cΓ)⁻¹σ_k

[0102] of equation (25). The control effort U_kis delayed by delay element 104 and the estimated pseudo derivative reference (PDR) term Λ_kgenerated at the output of adder 106 thereby implementing equation (25). The first difference 108 of Λ_kis computed and added 110 to Λ_kto generate the estimated PDR term Λ_k+1according to equation (26). The estimated PDR term Λ_k+1is then added 112 to the output of multiplier 96 to generate the term

[0103] Ψε_k+Λ_k+1

[0104] of equation (23).

[0105] . Details of the sliding line controller 92 of FIG. 5A are shown in FIG. 5C. The phase state errors are multiplied 114 by the sliding line c where c defines the phase state trajectory in the phase plane as described above. For example, in equation (16) the sliding line c is defined as

[0106] c=[1, C3].

[0107] The multiplication of the phase state errors by the sliding line c generates the sliding line variable σ_kper equation (20). The sign 116 of the sliding line variable σ_kis multiplied 118 by

[0108] μ=Δ(cΓ)⁻¹

[0109] to generate the term

[0110] μsgn (σ_k)

[0111] of equation (23).

σ

[0112] In the control law of equation (18), σ_kis non-increasing and changes sign on successive sample periods. When σ_k<0, to maintain stability and simultaneous switching it requires

[0113] σ_k+1≦−σ_k.

[0114] From the above equations

[0115] cε_k+1≦−cε_k;

[0116] c(R_k+1−(ΦX_k+ΓU_k))≦−cε_k.

[0117] Solving for U_{k yields}

[0118] U_k≧c(Φ+I)(cΓ)^−1ε_k+c(R_k+1−ΦR_k)(cΓ)⁻¹. (27)

[0119] However, an expression for U_khas already been derived in equation (22). Substituting equation (22) into (27) yields

[0120] c(ΦλI)(cΓ)⁻¹ε_k+c(R_k+1−ΦR_k)(cΓ)⁻¹+Δ(cΓ)⁻¹sgn(σ_k)≧c(Φ+I)(cΓ)⁻¹ε_k+c(R_k+1−ΦR_k)(cΓ)⁻¹

[0121] Combining terms and simplifying leads to

[0122] (−λcε_k+Δsgn(σ_k)≧cε_k

[0123] which leads to

[0124] Δ/(1+λ)sgn(σ_k)≧σ_k

[0125] A similar result follows for σ_k>0 with the inequality reversed, which leads to

[0126] α/(1λ)≦σ_k≦Δ/(1λ) (28)

[0127] Equation (28) specifies that the absolute magnitude of the sliding mode variable σ_kwill be constrained within a boundary layer such that

[0128] |σ_k|≦Δ/(1+λ)

[0129] The width of the boundary layer is a function of the Δ, λ and the sampling rate. The width of the boundary layer is generally defined through selecting an appropriate value for Δ, whereas the time constant of the loop is generally defined through appropriate selection of λ and the slope of the sliding line c. The system's insensitivity to parameter variations and load disturbances is increased by increasing the width of the boundary layer (i.e., increasing Δ), the trade-off being an increase in the required control effort and an increase in switching noise.

[0130] As described in greater detail below, the servo system can be adapted in real time so as to maintain the optimal condition where the magnitude of the sliding mode variable σ_kin steady state remains constant (i.e., σ_k+1=−σ_k) while satisfying the discrete-time switching condition of crossing the sliding line at every sample period. This maintains a constant, and arbitrarily small boundary layer that in turn minimizes the switching noise.

DESIGN OF THE SLIDING LINE

[0131] The steady state behavior of σ_kas described above can be used to determine the optimal value for the sliding line c. Multiplying both sides of equation (28) by ε_k^Tyields

[0132] σ_kε_k^T=cε_kε_k^T=Δ/(1+λ)sgn(σ_k)ε_k^T.

[0133] Taking the expectation E of both sides with E(ε_k^T)=0, yields the matrix equation

[0134] cE(ε_kε_k^T)=0. (29)

[0135] Expanding equation (29) and assuming a second order system without loss of generality, yields the simultaneous equations

[0136] c₁E(ε_k¹ε_k¹)+E(ε_k¹ε_k²)=0

[0137] c₁E(ε_k²ε_k¹)+E(ε_k²ε_k²)=0

[0138] For a stationary or deterministic process

[0139] E(ε_k¹ε_k²)=E(ε_k²ε_k¹).

[0140] Solving the simultaneous equations results in an expression for c

[0141] c₁²=E(ε_k²ε_k²)/E(ε_k¹ε_k¹). (30)

[0142] Equation (30) illustrates that the slope of the sliding line c is a function of the ratio between the rms error of the two states (i.e., the ratio of the rms position error over the rms velocity error) for a second order system. The expected rms position error is generally one of the design criteria of a system, and is therefore known (it is usually specified as a ratio between the reference and the error at specific reference frequencies). The rms velocity error will follow as a result of the system model.

ADAPTING TO PLANT GAIN VARIATIONS

[0143] The present invention uses the discrete-time existence equation (18) together with the sliding mode condition that σ_kcross the sliding line at every sample instance in order to adapt the controller to compensate for gain variations in the plant due, for example, to temperature or parameter drift. Adapting to gain variations in the plant increases the system's insensitivity to parameter variations without having to increase the boundary layer and attendant switching noise. Furthermore, because the boundary layer is minimized, the slope of the sliding line can be increased to a more optimal value while maintaining global stability.

[0144] Expressing the plant gain variation as β (with β=1 nominal), the discrete-time system (17) can be rewritten as

[0145] X_k+1=ΦX_k+βΓU_k.

[0146] From equations (22) and (23), algebraic manipulations leads to the discrete-time error equation

[0147] ε_k+1=ε_k(Φ−βΓΨ)+(I−βΓc(cΓ)⁻¹)(R_k+1−ΦR_k)−βΓΔ(cΓ)⁻¹sgn(σ_k). (31)

[0148] Multiplying by c and simplifying results in an expression for σ

[0149] σ_k+1=c(1−β)(R_k+1−ΦR_k)+(1−β)cΦε_k+β(λσ_k−Δsgn(σ_k)). (32)

[0150] The third term in equation (32) is equivalent to the nominal value of σ_k+1multiplied by the gain variation β and thus represents a direct measurement of the plant gain departure from nominal. The first and second terms of equation (32) represent movement away from the nominal gain of unity. This is understood with reference to FIG. 6 which shows the sliding line c and the nominal amplitude Δ/(1+λ) of the sliding mode variable σ_kaccording to equation (28). Thus, when the gain is nominal (β=1) the sliding mode variable σ_kwill switch between positive and negative values at every sample period and remain on the dashed lines representing the sliding line boundary layer. If the plant gain decreases then the magnitude of the sliding mode variable σ_kwill decrease, and if the plant gain increases the magnitude of the sliding mode variable σ_kwill increase as shown in FIG. 6. Thus, one adaptive strategy is to adapt the loop gain in order to adjust the measured value of σ_ktoward the nominal steady state value Δ/(1+λ) (i.e. toward the dashed lines in FIG. 6).

[0151] As discussed in greater detail below, if the gain of the plant drops below a certain threshold, then the sliding mode variable σ_kwill not cross the sliding line and change sign on every sample period. Conversely, if the gain exceeds a certain threshold, then the system will become unstable. Thus, there are three regions of operation as illustrated in FIG. 7 which is a plot of the gain variance β versus the magnitude of the sliding mode variable σ_k. In region I, the gain of the plant is below the lower threshold and σ_kdoes not switch across the sliding line at every sample period. In region III, the gain of the plant exceeds the upper threshold and the system is unstable. In the region between I and III (region II), the system is stable and the sliding mode variable σ_kcrosses the sliding line and changes sign on every sample period. Thus, the system will operate normally and adapt to changes in the plant gain as long as the gain changes slow enough such that magnitude of σ_kremains within region II.

[0152] FIG. 8A is a block diagram of the adaptive, discrete-time sliding mode controller of the present invention. The sliding line variable σ_koutput by the sliding line controller 92 is processed by an adaptive processor 120 which in turn adjusts the plant gain Kpa 30 according to the flow diagram of FIG. 9. First at step 122 a check is made to determine if the sliding line variable σ_kis crossing the sliding line and changing signs at every sample period. If not, then a loop is executed where the plant gain is incremented at step 124 until σ_kbegins to switch at every sample interval. Then at step 126 a branch is executed based on the absolute magnitude of σ_kIf the magnitude of σ_kis greater than nominal (i.e,. greater than Δ/1+λ), then at step 128 the plant gain is decreased incrementally. If at step 126 the magnitude of σ_kis less than nominal, then the plant gain is increased incrementally at step 130. Steps 128 and 130 are repeated until the magnitude of σ_kreaches the nominal value of Δ/1+λ.

[0153] Details of the adaptive processor 120 of FIG. 8A are shown in FIG. 8B. The adaptive processor 120 comprises: a switching detector 121 for determining whether σ_kis switching across the sliding line at every sample interval, an amplitude detector 123 for measuring the absolute magnitude of σ_k, an error detector 125 for detecting an error between the measured amplitude of σ_kand the nominal amplitude, and a stability detector 127 for detecting when the system has the potential for going unstable (i.e., when σ_kcrosses into region III in FIG. 7).

[0154] Many filtering options exist for implementing the switching detector 121; in FIG. 8B, a simple one-delay correlator is employed which operates according to the following equation

D_{k} = \frac{1}{m} \sum_{j = 0}^{m} sgn (σ_{k - j}) sgn (σ_{k - j - 1})

[0155] where m is a predetermined integer. In the above equation, if all m prior values of σ_khave changed sign, then D_kwould equal −1. If not, then D_k>−1. A threshold 129 may be employed in the switching detector 121 to compensate for noise; for example, −1<D_k>t where t is the threshold based upon anticipated noise. More filtering may be added if necessary by prior filtering σ_kprior to the correlator.

[0156] When _kis in region II or III of FIG. 7, it is necessary to determine the magnitude for σ_kwhich is then compared to the nominal value to generate the error signal, as well as to determine stability of the system. In these regions, the magnitude of σ_kis either constant or increasing, therefore the first difference of σ_kis a convenient detector (other techniques, such as the rms value of sigma are also possible). If the first difference is constant, then operation in region II is assured. If the first difference is increasing, then σ_kis in region III. The amplitude detector 123 of FIG. 8B operates according to

[0157] Sam_k=|σ_k−σ_k−1|_F

[0158] where the subscript F denotes a filtering operation 131 on the absolute value 133 of the first difference 135. The filter is chosen based on the expected noise; a simple moving average filter with binary coefficients will generally suffice.

[0159] The error detector 125 of FIG. 8B generates the error between the measured amplitude of σ_kand the nominal amplitude; the error is then used in the adaptation algorithm as described above. The nominal value for the amplitude of σ_kis

[0160] Δ/(1+λ)

[0161] the error is detected as

[0162] err_k=2Δ/(1+λ)−|σ_k−σ_k−1|_F.

[0163] The stability detector 127 of FIG. 8B determines when σ_khas crossed over into region III of FIG. 7 where the system may become unstable. Detecting when σ_kcrosses into region III allows higher gains to be used in the adaptation algorithm. Furthermore, the adaptive, discrete-time sliding mode controller of the present invention can stabilize an unstable system when σ_kcrosses into region III. The stability detector 127 is implemented by passing the measured amplitude of σ_kthrough a simple 1-D low-pass filter, and comparing the output to a threshold 137. When the average amplitude of σ_kexceeds the threshold 137, it has crossed into region III of FIG. 7.

[0164] The output of the switching detector 121 and stability detector 127 are used to determine which of the three regions in FIG. 7 σ_kis currently in. Based on this decision, the gain of the adaptation loop is adjusted by selecting one of three predetermined gains through a multiplexer 139 as shown. The decision logic 141 and gain selected is illustrated in the following table

[0165] The selected gain is then multiplied 143 by the error in σ_kand the result added 145 to the previous gain adjustment value β_k−1to generate the current gain adjustment value σ_k. The gain adjustment value β_kis then used to adjust the gain of the system amplifier 30 shown in FIG. 1.

[0166] The above-described adaptation strategy will work for small deviations of σ_kfrom nominal, but may not be adequate for cases where the deviation is significant since the first and second terms may dominate the third term in equation (32). To determine the regions where the adaptation strategy will work, it is first necessary to determine the steady state value of the errors ε_kand by inference σ_k.

ε

[0167] The steady state errors ε_kcan be determined using equation (31). Defining

[0168] Φ₀=Φ−βΓΨ

[0169] A=I−βΓc(cΓ)⁻¹

[0170] B=βΓΔ(cΓ)⁻¹

[0171] equation (31) can be written as

\begin{matrix} \begin{matrix} ϵ_{k + 1} = Φ_{0} ϵ_{k} + A (R_{k + 1} - Φ R_{k}) - Bsgn (σ_{k}) \\ ϵ_{k + 2} = Φ_{0} ϵ_{k + 1} + A (R_{k + 2} - Φ R_{k + 1}) - Bsgn (σ_{k + 1}) \\ = Φ_{0}^{2} ϵ_{k} + Φ_{0} A (R_{k + 1} - Φ R_{k}) - Φ_{0} Bsgn (σ_{k}) + \\ A (R_{k + 2} - Φ R_{k + 1}) - Bsgn (σ_{k + 1}) . \\ ϵ_{k + 3} = Φ_{0} ϵ_{k + 2} + Φ_{0}^{2} A (R_{k + 3} - Φ R_{k + 2}) - Bsgn (σ_{k + 2}) \\ = Φ_{0}^{3} ϵ_{k} + Φ_{0}^{2} A (R_{k + 1} - Φ R_{k}) - Φ_{0}^{2} Bsgn (σ_{k}) + \\ Φ_{0} A (R_{k + 2} - Φ R_{k + 1}) - Φ_{0} Bsgn (σ_{k + 1}) + \\ A (R_{k + 3} - Φ R_{k + 2}) - Bsgn (σ_{k + 2}) . \\ ϵ_{k + n} = Φ_{0}^{n} ϵ_{k} + \sum_{j = 0}^{n - 1} Φ_{0}^{j} (A ((R_{k + n - j} - Φ R_{k + n - j - 1}) - \\ Bsgn (σ_{k + n - j - 1}))) \end{matrix} & (33) \end{matrix}

[0172] Equation (33) may be simplified if we first consider the regulator problem where R=0. The steady state regulator error may be determined by taking the limit of the resulting equation

\begin{matrix} \lim_{n \to \infty} ϵ_{k + n} = \lim_{n \to \infty} {Φ_{0}^{n} ϵ_{k} - \sum_{j = 0}^{n - 1} (Φ_{0}^{j} B) sgn (σ_{k + n - j - 1})} & (34) \end{matrix}

[0173] With the assumption that the sign of σ changes on successive sample intervals, equation (34) represents a geometric series which can be further reduced

\begin{matrix} \lim_{n \to \infty} {Φ_{0}^{n} ϵ_{k} - \sum_{j = 0}^{n - 1} (Φ_{0}^{j} B) sgn (σ_{k + n - j - 1})} = \lim_{n \to \infty} {Φ_{0}^{n} ϵ_{k} - \sum_{j = 0}^{n - 1} (I - {(- 1)}^{n - j} Φ_{0}^{j + 1}) {(I - {(- 1)}^{1} Φ_{0})}^{- 1} B} & (35) \end{matrix}

[0174] With all elements of Φ₀less than one, equation (35) reduces to

\begin{matrix} \lim_{n \to \infty} ϵ_{k + n} = \lim_{n \to \infty} {Φ_{0}^{n} ϵ_{k}} + {(I + Φ_{0})}^{- 1} B = 0 + ({(I + Φ_{0})}^{- 1} β) {ΓΔ (c Γ)}^{- 1} & (36) \end{matrix}

[0175] The steady state value of σ may also be determined from equation (36). Multiplying by c and sgn(σ_k), σ_k+1is

[0176] σ_k+1=c(I+Φ₀)⁻¹βΓΔ(cΓ)⁻¹sgn(σ_k). (37)

[0177] FIG. 10 shows the analytical solutions overlaid with the simulated values for σ steady state. Note that for certain threshold values of β less than one, the analytical solutions do not agree with the simulated values. These regions correspond to areas where the assumption of sgn(σ_k+1)=−sgn(σ_k) is violated and equation (37) is no longer valid. FIGS. 11A-11D show a series of step responses with varying plant gain (beta).

SUFFICIENT CONDITIONS FOR ZERO CROSSING

[0178] The assumption that a will cross the sliding line and change sign at every sample period depends on the values selected for the sliding mode variables c, λ and Δ, as well as the plant transfer function and gain variation β. The values which satisfy this condition can be determined from equations (31) and equation (34). From equation (34), the error for the regulator problem (R=0) at state k+n is

ϵ_{k + n} = Φ_{0}^{n} ϵ_{k} - \sum_{j = 0}^{n - 1} (Φ_{0}^{j} B) sgn (σ_{k + n - j - 1})

[0179] From equation (31), the error at state k+n+1 is

[0180] ε_k+n+1=Φ₀ε_k+n−Bsgn(σ_k+n).

[0181] Therefore, for σ_k+1>0 a sign change will occur at every sample period if

[0182] cε_k+n+1<0

[0183] cΦ₀ε_k+n−cBsgn(σ_k+n)<0

[0184] cΦ₀ε_k+n<CB.

[0185] A similar result can be derived for σ_k+1<0 resulting in the combined requirements of

[0186] −cB<cΦ₀ε_k+n<cB. (38)

[0187] Equation (38) is valid for any location of a in the phase plane. Assuming equation (38) is satisfied such that a changes sign at every sample period, equation (38) can be written as

[0188] −cB<cΦ₀(I+Φ₀)⁻¹<cB. (39)

[0189] Expanding equation (38) using equation (34) and multiplying by cB)¹, equation (39) can be written as

\begin{matrix} - 1 < \lim_{n \to \infty} {c Φ_{0}^{n + 1} ϵ_{k} - c \sum_{j = 1}^{n - 1} Φ_{0}^{j} Bsgn (σ_{k + n - j - 1})} {(cB)}^{- 1} < 1 & (40) \end{matrix}

[0190] Assuming that the initial condition term tends to zero, equation (40) can be written as

\begin{matrix} - 1 < \lim_{n \to \infty} c {Φ_{0}^{1} B (sgn (σ_{k + n}) + Φ_{0}^{2} B (sgn (σ_{k + n + 1}) + \dots))} {(cB)}^{- 1} < 1 & (41) \end{matrix}

[0191] If successive values are non-increasing, then the series in equation (41) will converge to a bounded value between zero and one. The conditions for assuring that σ will cross the sliding line and change sign on every sample period is thus

[0192] cΦ₀^j+1B<cΦ₀^jB (42)

[0193] FIG. 12 demonstrates equation (42) for a given system with c=[0.8 1] over a range of values for the plant gain (beta). When the plant gain β falls below a certain threshold, equation (42) is violated and the system becomes chaotic. The region where equation (42) is violated is primarily a function of the sliding line c and the gain β. FIG. 12 illustrates that the analytical estimates of steady state behavior are lower bounds to the potential steady state behavior. FIG. 13 shows the value of β that delineates the chaotic boundary for each value of c.

[0194] When equation (42) is violated and the system becomes chaotic, the steady state behavior will depend on the initial conditions of the system. It is possible that the steady state behavior, while stable, may be significantly different depending on initial conditions. FIGS. 14A-14C illustrate this by showing step responses of varying amplitudes while the system is in the chaotic region. Notice that in FIG. 14A and FIG. 14B when the amplitude of the step response is −0.1 and −0.2, σ does not change sign on every sample period, whereas in FIG. 14C σ does change sign on every sample period when the amplitude of the step response is −0.5.

EXTENSION TO THE SERVO PROBLEM

[0195] The above analysis of discrete-time sliding mode control applied to a regulator can be extended to a servo system having a non-zero reference signal. For σ_k+1>0, the above analysis with a non-zero reference signal leads to

[0196] cε_k+n+1<0

[0197] cΦ₀ε_k+n+cA(R_k+n+1−ΦR_k+n)−cBsgn(σ_k+n)<0

[0198] c Φ₀ε_k+n+cA(R_k+n+1−ΦR_k+n)<cB.

[0199] A similar result can be derived for σ_k+1<0 resulting in the combined requirements of

[0200] −cB<cΦ₀ε_k+n+cA(R_k+n+1−ΦR_k+n)<cB. (43)

[0201] Equation (43) is valid for all locations of σ in the phase plane, and it does not require that steady state behavior be attained. For the specific case of steady state behavior where σ crosses the sliding line and changes sign on every sample period, further simplification is possible

\lim_{n \to \infty} {c Φ_{0} ϵ_{k + n} + cA (R_{k + n + 1} - Φ R_{k + n})} = \lim_{n \to \infty} {c Φ_{0}^{n + 1} ϵ_{k} - c Φ_{0} \sum_{j = 0}^{n - 1} Φ_{0}^{j} A (R_{k + n - j} - Φ R_{k + n - j - 1})} + (cA) (R_{k + n + 1} - Φ R_{k + n}) - \lim_{n \to \infty} {c Φ_{0} \sum_{j = 0}^{n - 1} Φ_{0}^{j} Bsgn (σ_{k + n - j - 1})}

[0202] Combining terms and taking the limit of the initial condition term leads to

\begin{matrix} \lim_{n \to \infty} {c Φ_{0} ϵ_{k + n} + cA (R_{k + n + 1} - Φ R_{k + n})} = \lim_{n \to \infty} {c \sum_{j = 0}^{n - 1} Φ_{0}^{j} A (R_{k + n + 1 - j} - Φ R_{k + n - j})} - \lim_{n \to \infty} {c Φ_{0} \sum_{j = 0}^{n - 1} Φ_{0}^{j} Bsgn (σ_{k + n - j - 1})} & (44) \end{matrix}

[0203] From equations (35) and (36), the second term in equation (44) reduces to

[0204] cΦ₀(I+Φ₀)⁻¹Bssn (σ_k).

[0205] For the servo problem, the residual derivative term modulates the switching action of σEquation (43) then simplifies to

\begin{matrix} - (cB + c {Φ_{0} (I + Φ_{0})}^{- 1} B) < \lim_{n \to \infty} {c \sum_{j = 0}^{n - 1} Φ_{0}^{j} A (R_{k + n + 1 - j} - Φ R_{k + n - j})} < (cB + c {Φ_{0} (I + Φ_{0})}^{- 1} B) & (45) \end{matrix}

[0206] The magnitude of the middle term in equation (45) is more easily evaluated in the z domain

\begin{matrix} | \lim_{n \to \infty} {c \sum_{j = 0}^{n - 1} Φ_{0}^{j} A (R_{k + n + 1 - j} - Φ R_{k + n - j})} | = | c (Φ_{0}^{0} A (zI - Φ) R (z) + Φ_{0}^{1} z^{- 1} A (zI - Φ) R (z) + Φ_{0}^{2} z^{- 2} A (zI - Φ) R (z) + \dots) | = | c ({(\frac{Φ_{0}}{z})}^{0} + {(\frac{Φ_{0}}{z})}^{1} + {(\frac{Φ_{0}}{z})}^{2} + \dots) A (zI - Φ) R (z) | = | {cz (zI - Φ_{0})}^{- 1} A (zI - Φ) R (z) | & (46) \end{matrix}

[0207] where the geometric series in equation (46)

({(\frac{Φ_{0}}{z})}^{0} + {(\frac{Φ_{0}}{z})}^{1} + {(\frac{Φ_{0}}{z})}^{2} + \dots)

[0208] converges to

[0209] z(zI−Φ₀)⁻¹.

[0210] The resulting bounds are therefore given as

[0211] |cz(zI−Φ₀)⁻¹A(zI−Φ)R(z)|<2(cB+cΦ₀(I+Φ₀)⁻¹B) (47)

PSEUDO DERIVATIVE REFERENCE ESTIMATORS

[0212] Equations (24) is the pseudo derivative reference (PDR) Λ_k+1and equations (25) and (26) set forth above disclose a technique for estimating the PDR Λ_k+1in the control law of equation (23). This section describes various alternative embodiments for estimating the pseudo derivative reference Λ_k+1through the use of a least-mean-square algorithm.

[0213] In general, servo systems can be divided into three categories: systems where the reference is known, such as in robotic systems; systems where the reference is unknown but repeatable, such as the runout signal in disk storage systems; and systems where the reference is unknown and non-repeatable. For the first type of systems where the reference is known, the pseudo derivative reference Λ_k+1can be determined exactly from equation (22)

[0214] Λ_k+1=c(R_k+1−ΦR_k)(cΓ)⁻¹.

[0215] For systems where the reference is unknown, the pseudo derivative reference Λ_k+1must be estimated.

[0216] One embodiment for estimating the Λ_k+1when the reference is unknown and repeatable is shown in FIG. 15A. In this example, the servo controller controls the motion of a read head in a disk storage system. The eccentricities of the disk storage medium 4 results in an unknown repeatable perturbation of the static reference signal 27 of FIG. 1. This perturbation is referred to as “runout” and is modelled as a noise signal 25 added 24 to the static reference signal 27 to generate the actual reference signal 18 for generating the position error phase state ε122. References of this type are harmonic in nature and are related to the angular velocity of the disk. They can be modelled as

\begin{matrix} R_{k} = \sum_{n = 1}^{m} {An}_{k} \sin (nwk) + {Bn}_{k} \cos (nwk) & (48) \end{matrix}

[0217] where m is an integer greater than zero, the coefficients An and Bn are unknown, and w is the angular velocity of the disk 4 as determined from a speed transducer 132 (FIG. 15A).

[0218] Referring to FIG. 15A, the plant 134 represents the elements of the recording device (actuator, read head, spindle motor, read channel, etc.). The input to the plant 134 is a control signal U_kgenerated by summing 136 the output of the sliding mode controller 26 (described above) and an estimated reference signal ER. The output of the plant is the measured position of the read head 6 relative to the surface of the disk 4. The detected angular velocity w is input into a sinusoid synthesizer 134 which synthesize sinusoidal signals (and harmonics) of the form in equation (48). An observer 138 estimates the non-measurable system phase states: the position phase state ˜Xp and the velocity phase state ˜Xv (or, alternatively, it may estimate the phase state errors). These phase states cannot be measured directly due to the effect of the unknown reference signal on these states. The input into the observer 138 is a position error generated by subtracting 139 the position signal X output by the plant 134 from the estimated position phase state ˜Xp output by the observer 138. The estimated phase states ˜Xp and ˜Xv are subtracted from static reference signals Rp and Rv at adders 140A and 140B to generated a position error phase state ε1_kand a velocity error phase state ε2_k. Alternatively, for many classes of systems the higher order error phase states, such as the velocity error phase state, may be estimated by taking the derivative of the position error phase state.

[0219] The coefficients An and Bn of equation (48) are estimated by minimizing the position error phase state ε1^kusing a least-mean-square (LMS) algorithm. A sinusoid synthesizer 142 synthesizes the sinusoidal signal (and harmonics) of equation (48) which are input into an LMS adaptor 144. The LMS adaptor processes the sinusoidal signals output by the synthesizer 142 and the position error phase state ε1^kto compute the coefficients An and Bn of the estimated reference signal ER according to the following LMS algorithm

{ER}_{k} = \sum_{n = 1}^{m} {An}_{k} \sin (nwk) + {Bn}_{k} \cos (nwk)

{An}_{k + 1} = {An}_{k} + g {ϵ1}_{k} \sin (nwk)

{Bn}_{k + 1} = {Bn}_{k} + g {ϵ1}_{k} \cos (nwk)

[0220] where g is a predetermined gain constant. This technique minimizes the position error, but leaves a residual modulation on α/(1λ).

[0221] Adding the estimated reference ER to the control effort generated by the sliding mode controller 26 approximates the feed forward term Λ_k+1of equation (23). Therefore, the hardware shown in FIG. 5B for generating Λ_k+1is obviated.

[0222] Estimating the reference by minimizing the position error phase state ε1^kwill induce a residual modulation on the sliding mode variable σ_kas it switches across the sliding line c. This is because the LMS algorithm reduces the error in the estimated reference at specific frequencies more than would be expected from the pseudo derivative reference term Λ_k+1alone. If no further adaptation is required, this residual modulation is acceptable; however, it is possible to attenuate the modulation in σ_kby minimizing the error in σ_krather than minimizing the position error phase state ε1_k. This embodiment of the present invention is understood with reference to FIG. 15B.

[0223] FIG. 15B is essentially the same as FIG. 15A except that the LMS adaptor minimizes the error in σ_krather than the position error phase state ε1_k. Thus, the LMS algorithm becomes

{ER}_{k} = \sum_{n = 1}^{m} {An}_{k} \sin (nwk) + {Bn}_{k} \cos (nwk)

{err}_{k} = σ_{k} - sgn (σ_{k}) \frac{Δ}{(1 + λ)}

{An}_{k + 1} = {An}_{k} + {gerr}_{k} \sin (nwk)

{Bn}_{k + 1} = {Bn}_{k} + {gerr}_{k} \cos (nwk)

[0224] where the variables Δ an λ determine the nominal switching boundary for σ_kas described above with reference to the discrete-time sliding mode controller 26. This method increases the magnitude of the residual position error within specification, but it essentially eliminates the modulation in σ_k. In addition, it provides a better estimate of the pseudo derivative reference Λ_k+1than does the LMS method of minimizing the position error phase state ε1_k.

[0225] If the reference signal is completely unknown (non-repeatable), then the preferred method for estimating the reference is illustrated in FIG. 15C. This method enhances the estimate of the pseudo derivative reference Λ_k+1described in equations (25) and (26) by taking the local derivative and adding it to the estimate yielding an increasingly better estimate of Λ_k+1

[0226] Λ_k+1≈Λ_k

[0227] Λ_k+1≈Λ_k+(Λ_k−Λ_k−1)

[0228] Λ_k+1≈A_kΛ_k+B_k(Λ_k−Λ_k−1)

[0229] where A and B are unknown coefficients. This technique may be generalized to a predictor of m derivatives similar to the LMS algorithms described above. In general, a one step predictor is sufficient to minimize the modulation in σ_k. If, however, the reference has higher frequency components, then this technique is extensible to higher order derivatives. The LMS adaptor of FIG. 15C computes the coefficients A and B, and therefore the estimated reference signal ER, according to

Λ_{k + 1} = U_{k - 1} - c {Φ (c Γ)}^{- 1} ϵ_{k - 1} + {σ_{k} (c Γ)}^{- 1}

{err}_{k} = σ_{k} - sgn (σ_{k}) \frac{Δ}{(1 + λ)}

A_{k + 1} = A_{k} + g_{0} {err}_{k} Λ_{k}

B_{k + 1} = B_{k} + g_{1} {err}_{k} (Λ_{k} - Λ_{k - 1})

{ER}_{k} = A_{k} Λ_{k} - B_{k} (Λ_{k} - Λ_{k - 1})

[0230] where g₀and g₁are predetermined gain constants. The above 17 algorithm uses the past error states ε_k−1, the past control effort U_k−1, and the current value of σ_kto generate the estimated reference signal ER. It does not require any a priori knowledge of the reference, and its convergence speed can be increased by increasing the convergence factors g₀and g₁(g₁may be larger than g₀, corresponding to the slope of c).

[0231] Many changes in form and detail could be made without departing from the essential function of the present invention; the particular embodiments disclosed are not intended to be limiting. For instance, the discrete-time sliding mode controller may be implemented in hardware or software, and higher order phase states could be used in place of, or in addition to, the particular phase states disclosed. These and other modifications derived from the disclosed embodiment are within the intended scope of the present invention as properly construed from the following claims.

Claims

We claimed:

1. A discrete-time sliding mode controller for controlling the motion of a mechanical apparatus as part of a controlled system, the diserete-time sliding mode controller comprising:

(a) a phase state generator for generating a discrete-time phase state signal X1_k, the discrete-time phase state signal X1_kcomprising sample values occurring at a predetermined interval T;

(b) a linear signal generator, responsive to the discrete-time phase state signal X1_k, for generating a linear control signal;

a sliding mode signal generator, responsive to the discrete-time phase state signal X1_k, for generating a sliding mode control signal according to:

μΔsgn(σ_k)

where μ is a predetermined gain, Δ is a predetermined constant, σ_kis a sliding mode variable computed from the discrete-time phase state signal X1_k, and y sgn(σ_k) returns the sign of σ_k;

(d) a reference estimator for generating an estimated reference signal ER; and

(e) a combiner for combining the linear control signal, the sliding mode control signal, and the estimated reference signal ER to generate a motion control signal U_kfor controlling the motion of a mechanical apparatus.

2. The discrete-time sliding mode controller as recited in claim 1, wherein the discrete-time phase state signal X1_kis a position error phase state, and the reference estimator comprises:

(a) an angular velocity detector for detecting an angular velocity of a rotating device in the controlled system;

(b) a sinusoid synthesizer for generating a synthesized sinusoidal signal;

(c) a least-mean-square (LMS) adaptor for generating the estimated reference signal ER from the sinusoidal signal and the position error phase state X1_k.

3. The discrete-time sliding mode controller as recited in claim 2, wherein the LMS adaptor generates the estimated reference signal ER according to:

{ER}_{k} = \sum_{n = 1}^{m} {An}_{k} \sin (nwk) + {Bn}_{k} \cos (nwk)

{An}_{k + 1} = {An}_{k} + {gX1}_{k} \sin (nwk)

{Bn}_{k + 1} = {Bn}_{k} + g {X1}_{k} \cos (nwk)

wherein:

(a) w represents the angular velocity of the rotating device in the controlled system;

(b) An_ksin(nwk)+Bn_kcos(nwk) represents the sinusoidal signal;

(d) m is a predetermined integer greater than zero.

4. The discrete-time sliding mode controller as recited in claim 3, wherein:

(a) the linear signal generator generates the linear control signal according to:

Ψε_k

where Ψ is a constant and ε_kis a discrete-time phase state error signal generated from the discrete-time phase state signal X1_kand a reference signal R_k;

(b) the sliding mode signal generator generates the sliding mode control signal according to:

μΔ sgn(σ_k)

where μ is a predetermined gain, Δ is a predetermined constant, σ_kis a sliding mode variable computed from the discrete-time phase state signal X1_k, and sgn(σ_k) returns the sign of σ_k; and

Ψε_k+μΔ sgn(σ_k)+ER.

5. The adaptive discrete-time sliding mode controller as recited in claim 3, wherein the sliding mode signal generator generates the sliding mode control signal according to:

μΔ sgn(σ_k)

where μ is a predetermined gain, Δ is a predetermined constant, σ_kis a sliding mode variable computed from the discrete-time phase state signal X1_k, and sgn(σ_kreturns the sign of σ_k.

6. The adaptive discrete-time sliding mode controller as recited in claim 5, wherein the sliding mode variable σ_kis computed according to:

where ε_kis a plurality of discrete-time phase state errors of the controlled system and c is a predetermined vector that defines a sliding line in a phase plane.

σ_k=cε_k

7. The adaptive discrete-time sliding mode controller as recited in claim 5, wherein the sliding mode variable σ_kchanges sign at substantially every sample index k.

8. The adaptive discrete-time sliding mode controller as recited in claim 7, wherein:

(a) the sliding mode variable σ_kis substantially constrained to:

−W<σ_k<+W;

(b) W is a predetermined constant.

9. The adaptive discrete-time sliding mode controller as recited in claim 7, wherein the sliding mode variable σ_kis substantially constrained to:

σ_k+1=λσ_k−Δsgn(σ_k)

where λ is a predetermined constant and λ<1.

10. The adaptive discrete-time sliding mode controller as recited in claim 9, wherein the magnitude of the sliding mode variable σ_kis substantially constrained to:

|σ_k|≦Δ/(1+λ).

11. The adaptive discrete-time sliding mode controller as recited in claim 1, wherein the sliding mode variable σ_kis computed according to:

σ_k=cε_k

where ε_kis a plurality of discrete time phase state errors of the controlled system and c is a predetermined vector that defines a sliding line in a phase plane.

12. The adaptive discrete-time sliding node controller as recited in claim 1, wherein the sliding mode variable σ_kchanges sign at substantially every sample index k.

13. The adaptive discrete-time sliding mode controller as recited in claim 12, wherein:

(a) the sliding mode variable σ_kis substantially constrained to:

−W<σ_k<+W;

(b) W is a predetermined constant.

14. The adaptive discrete-time sliding mode controller as recited in claim 12, wherein the sliding mode variable σ_kis substantially constrained to:

σ_k+1=λσ_k−Δsgn(σ_k)

where X is a predetermined constant and λ<1.

15. The adaptive discrete-time sliding mode controller as recited in claim 14, wherein the magnitude of the sliding mode variable σ_kis substantially constrained to:

|σ_k|≦Δ/(1+λ).

16. The discrete-time sliding mode controller as recited in claim 15, wherein the discrete-time phase state signal X1_kis a position error phase state, and the reference estimator comprises:

(a) an angular velocity detector for detecting an angular velocity of a rotating device in the controlled system;

(b) a sinusoid synthesizer for generating a synthesized sinusoidal signal;

(c) a least-mean-square (LMS) adaptor for generating the estimated reference signal ER from the sinusoidal signal and the sliding mode variable σ_k.

17. The discrete-time sliding mode controller as recited in claim 16, wherein the LMS adaptor generates the estimated reference signal ER according to:

{ER}_{k} = \sum_{n = 1}^{m} {An}_{k} \sin (nwk) + {Bn}_{k} \cos (nwk)

{err}_{k} = σ_{k} - sgn (σ_{k}) \frac{Δ}{(1 + λ)}

{An}_{k + 1} = {An}_{k} + {gerr}_{k} \sin (nwk)

{Bn}_{k + 1} = {Bn}_{k} + {gerr}_{k} \cos (nwk)

wherein:

(a) w represents the angular velocity of the rotating device in the controlled system;

(b) An_ksin(nwk)+Bn_kcos(nwk) represents the sinusoidal signal;

(d) m is a predetermined integer greater than zero.

18. The adaptive discrete-time sliding mode controller as recited in claim 1, wherein;

wherein:

(a) the sliding mode signal generator generates the sliding mode control signal according to:

μΔ sgn(σ_k)

where μ is a predetermined gain, Δ is a predetermined constant, σ_kis a sliding mode variable computed from the discrete-time phase state signal X1_k, and sgn(σ_k)returns the sign of σ_k;

(b) σ_kis computed according to:

σ_k=cε_k

where εl_kis a plurality of discrete-time phase state errors of the controlled system and c is a predetermined vector that defines a sliding line in a phase plane;

σ_k+1=λσ_k−Δsgn(σ_k)

where λ is a predetermined constant and λ<1;

(d) a plurality of discrete-time phase states X_kof the controlled system are substantially modeled relative to the motor control signal U_kaccording to:

X_k+1=ΦX_k+ΓU_k

where Φ is a matrix and Γ is a scalar;

(e) a pseudo derivative reference signal Λ_k+1is computed according to:

Λ_k=U_k−1−cΦ(cΓ)⁻¹ε_k−1+σ_k(cΓ)⁻¹; and

(f) ε_kis a discrete-time phase state error vector generated from the discrete-time phase states X_kof the controlled system and a reference signal matrix R_k;

(g) the reference estimator comprises a least-mean-square (LMS) adaptor for generating the estimated reference signal ER according to:

{err}_{k} = σ_{k} - sgn (σ_{k}) \frac{Δ}{(1 λ)}

A_{k + 1} = A_{k} + g_{0} {err}_{k} Λ_{k}

B_{k + 1} = B_{k} + g_{1} {err}_{k} (Λ_{k} - Λ_{k - 1})

{ER}_{k} = Λ_{k} Λ_{k} - B_{k} (Λ_{k} - Λ_{k - 1})

(i) w represents the angular velocity of a rotating device in the controlled system;

(ii) A_k+B_kare coefficients; and

(iii) g₀and g₁are a predetermined gain constants.

Patent Citations (16)

Patent	Date	Inventor	Cited By
US3701889	1972-10-01	Barron et al.	Applicant
US4679103	1987-07-01	Workman	Applicant
US4713596	1987-12-01	Bose	Applicant
US5249117	1993-09-01	Greenough et al.	Applicant
US5276387	1994-01-01	Gamble	Applicant
US5285379	1994-02-01	Gamble	Applicant
US5341078	1994-08-01	Torii et al.	Applicant
US5345348	1994-09-01	Suzuki	Applicant
US5442270	1995-08-01	Tetsuaki	Applicant
US5510939	1996-04-01	Lewis	Examiner
US5699207	1997-12-01	Supino et al.	Examiner
US5781365	1998-07-01	Romano et al.	Examiner
US5825582	1998-10-01	Supino et al.	Examiner
US5901010	1999-05-01	Glover et al.	Examiner
DE4405087	1994-08-01		Applicant
EP13326	1980-07-01		Applicant

Non-Patent Literature (21)

Katsuhisa Furuta, “Sliding Mode Control of a Discrete System”, Systems & Control Letters, vol. 14, No. 2, Feb. 1990.Applicant
J. C. Hung, “Chattering Handling for Variable Structure Control Systems”, Proceedings of the IECON '93, vol. 3, 1993.Applicant
Raymond A. DeCarlo, Stanislaw H. Zak, and Gregory Mathews, “Variable Structure Control of Nonlinear Multivaribale Systems: A Tutorial”, Proceedings of the IEEE, vol. 76, No. 3, Mar. 1988.Applicant
V. I. Utkin, “Discontinous Control System: State of Art In Theory and Applications”, Automatic Control World Congress 1987, vol. 1.Applicant
Weibing Gao and James C. Hung, “Variable Structure control of Nonlinear Systems: A New Approach”, IEEE Trans. on Industrial Electronics, vol. 40, No. 1, Feb. 1993.Applicant
M. A. El-Sharkawi, “Development and Implementation of High Performance Variable Structure Tracking Control for Brushless Motors”, IEEE/PES 1990 Summer Meeting, Mineapolis, minnesota, Jul. 15-19, 1990.Applicant
G. C. Verghese, B. Fernandez R., and J. K. Hedrick, “Stable, Robust Tracking by Sliding Mode Control”, Systems & Control Letters, vol. 10, 1988.Applicant
Kar-Keung D. Young and Harry G. Kwatny, “Variable Structure Servomechanism Design and Applications to Overspeed Protection Control”, 1982 International Federation of Automatic Control.Applicant
B. K. Bose, “Sliding Mode Control of Induction Motor”, CH2207-9/85/0000-0479 IEEE (1985).Applicant
“Sliding Mode Control For Arrivals and Small Movement” IBM Technical Disclosure Bulletin, vol. 23, No. 4, (1990).Applicant
Weibing Gao, Yufu Wang, and Abdollah Homaifa, “Discrete-Time Variable Structure Control Systems”, IEEE Trans. on Industrial Electronics, vol. 42, No. 2, Apr. 1995.Applicant
John Y. Hung, Weibing Gao, and James C. Hung, “Variable Structure Control: A Survey”, IEEE Trans. on Industrial Electronics, vol. 40, No. 1, Feb. 1993.Applicant
Yasuda et al., “Controller Using Sliding Mode Control”, Patent Abstracts of Japan, vol. 12, No. 411.Applicant
Jean-Jacques E. Slotine, “Sliding controller design for non-linear systems”, Int. J. Control, vol. 40, No. 2, 1984, pp. 421-434.Applicant
G. Ambrosino, G. Celentano, F. Garofalo, “Variable structure model reference adaptive control system”, Int. J. Control, vol. 39, No. 6, 1984, pp. 1339-1349.Applicant
Chandrasekhar Namuduri and Paresh C. Sen, “A Servo-Control System Using a Self-Conrolled Synchronous Motor (SCSM) With Sliding Mode Controller”, IEEE Trans. on Industry Applications, vol. IA-23, No. 2, Mar./Apr., 1987.Applicant
F. Harashima, H. Hashimoto, and S. Kondo, “MOSFET Converter-Fed Position Servo System with Sliding Mode Control”, IEEE Transactions on Industrial Electronics, vol. IE-32, No. 3, Aug. 1985, pp. 238-244.Applicant
C. Denise Mee, Eric D. Daniel, “Magentic Recording vol. II: Computer Data Storage”, McGraw-Hill, 1988, pp. 53-70.Applicant
Andrzej Bartoszewicz, “Remarks on 'Discrete-Time Variable Structure Control Systems”, IEEE Transactions on Industrrial Electronics, vol. 43, No. 1, Feb. 1996.Applicant
U.S. application No. 08/943,997, filed Oct. 3, 1997.Applicant
S. Weerasooriya and T.S. Low, “Adaptive Sliding Mode Control of a Disk Drive Actuator”, Asia-Pacific Workshop on Advances in Motion Control Proceedings, Singapore, Jul. 15-16, 1993, IEEE, NY, USA, pp. 177-182.Applicant

Abstract