Electric Machine System

1. Field of the Invention

The present invention relates to electric machine systems.

2. Description of the Prior Art

U.S. Pat. application Ser. Nos. 3,467,844, 3,239,701 and 3,956,629 disclose basic synchronous machines in which a rotor of a motor is supplied with a direct current (DC) power supply so as to avoid the use of slip rings and brushes. The synchronous machines of those patents, however, provide synchronous operation but only at one speed.

Previous systems that have employed a second rotor/stator combination have generally not been multiphase systems. Moreover, they have generally been rectified to supply DC to the rotor. U.S. Pat. Nos. 4,459,530 and 4,634,950 disclose electric rotating apparatus adapted to function as a motor or a generator. The apparatus described therein includes two balanced phase electric machines that can be either a balanced phase synchronous motor or a power generator.

It is an object of the present invention to provide an improved electric machine system that is readily adapted for use as an electric motor or electric generator.

The foregoing and other objects are realized by the present invention of an electric machine system. Although rotating concepts are used herein to explain the workings of this invention, linear concepts are equally applicable. In the linear case, the word "rotor" as used in the discussion should be replaced with "moving body" and "rotating" should be replaced with "moving". The present invention includes a moving body, such as a rotor, and a stationary body, such as a stator, that surrounds the moving body. The system also includes a circuit formed by a first pair of windings and a second pair of windings. The first pair of windings are separated by an air gap. These windings generate a torque to rotate the moving body. This pair of windings includes windings on the moving body and windings on the stationary body. The second pair of windings is also separated by an air gap, but serves to alter the excitation of the first pair of windings. Like the first pair of windings, the second pair of windings includes windings on the moving body and windings on the stationary body.

The circuit of the electric machine system also includes a modulator for supplying at least one modulated carrier signal to one of the windings of the pair of windings. A demodulator is provided for demodulating the carrier signal to produce demodulated information signals. The demodulator forwards the demodulated information signals to one of the windings. Preferably, each of the windings are formed from separate phase windings. Specifically, it is preferred that each of the windings be provided with a separate phase excitation signal.

The windings are powered by a means for providing power to the modulator and to the windings. Thus, if there are three windings in every set of windings, each of the three windings may be provided with a unique phase signal. Moreover, at least one of the windings of the moving body in the first pair of windings may be provided a phase signal that is different from the phase signal that is supplied to the corresponding winding on the moving body in the second pair of windings. Analogously, at least one winding of the stationary body in the first pair of windings may be provided with a phase signal that is different from the phase signal supplied to a corresponding winding on the moving body in the second pair of windings.

In accordance with one embodiment, the means for providing power further comprises a power source for supplying alternating current phase signals of different phases. The means for providing power further includes bidirectional power switches for coupling the respective phase signals to respective windings. Preferably, there are as many switches as there are phase signals. However, there may be instances where there are fewer switches than there are phase signals. A processor means may be included to control the operation of these switches. This processing means may also perform other useful functions in the electric machine system.

The electric machine system may also include at least one bypass capacitor that is coupled to the means for providing power to one of the pairs of windings. The bypass capacitor serves to diminish coupling between circuit elements and to filter unwanted transients. The number of bypass capacitors that are employed depends in part upon whether the windings of the stationary body in the first pair of windings is connected in series with the windings on the stationary body in the second pair of windings or is connected in parallel. The capacitance ratings of these bypass capacitors may be selected so as to establish circuit resonance at the frequency of the utility power source, which is 60 hertz in the United States. In addition to these bypass capacitors, the electric machine system may include a resonant switching system for switching the means for providing power on and off. These resonant switching systems may include resonating capacitors that are in addition to the bypass capacitors.

FIG. 1 is an electrical schematic of the electric machine system of the present invention;

FIG. 2 is an electrical schematic of a conventional single phase rotating electric machine;

FIG. 3 is an electrical schematic of a conventional balanced two phase, smooth air gap rotating electric machine;

FIG. 4 is an electrical schematic of the rotor excitation generator of the present invention;

FIG. 5a is an electrical schematic of a first embodiment of the present invention;

FIG. 5b is an electrical schematic of a second embodiment of the present invention;

FIG. 5c is an electrical schematic of a third embodiment of the present invention;

FIG. 6 is an electrical schematic of a fourth embodiment of the present invention;

FIG. 7 is a block diagram depicting the major components required for the electric machine system of the present invention to implement resonant switching;

FIG. 8a is a block diagram depicting a fifth embodiment of an electric machine system of the present invention in which the stator windings are connected in series;

FIG. 8b is a block diagram depicting the fifth embodiment of the present invention in which the stator windings are connected in a parallel arrangement; and

FIG. 9 is a block diagram depicting a sixth embodiment of the electric machine system of the present invention in which a direct current winding or permanent magnet assembly is employed.

A parallel connected embodiment of the present invention will be described hereinafter with reference, initially, to FIG. 1. The electric machine system of the present invention includes a rotor 10 surrounded by a stator 12. The rotor 10 rotates about a central axis 11 shown as a broken line in FIG. 1. The stator 12 includes three stator phase windings 16 which are shown as being connected in a wye configuration in FIG. 1. These windings 16 are excited by high frequency modulated signals output from the modulator 14 over connections 17 leading to the winding 16. The modulator is powered by a direct current source which is connected to the modulator 14 by connection 20. Similarly, it may be connected to an alternating current source. The modulator receives three alternating current signals, denoted as phase 1, phase 2 and phase 3 signals, respectively, over connections 22, 24 and 26.

The stator 12 also includes stator phase windings 28. The windings 28 comprise three phase windings 28a, 28b and 28c connected in a wye configuration. Each respective winding 28a, 28b and 28c is connected to a separate one of the three alternating current sources phase 1, phase 2 and phase 3. In particular, winding 28a is connected to the phase 1 current source through connection 30, and winding 28b is connected to the phase 2 current source through connection 32. Lastly, winding 28c is connected to the phase 3 current source through connection 34. The rotor 10 also includes two sets of windings 36 and 38. The windings 36 are of the same configuration and size as the windings 16 on the stator 12. Likewise, the windings 38 are matched in configuration and size to the windings 28 on the stator 12.

The above described components can be divided into two categories. The first category is the power generator and motor (denoted as PGM) which is the mechanical power and torque producing entity that produces torque to drive the rotor. The PGM includes windings 28 and 38. It may be similar to a conventional three phase wound rotor induction electric machine. It does not, however, include the traditional means of rotor excitation, nor does it include sliding electrical contacts. Furthermore, it does not include a slip ring body.

The second category of components is the rotor excitation generator (denoted as REG) that electrically excites the rotor windings 38 of the PGM. The components that constitute the REG are modulator 14, windings 16, windings 36 and demodulator 40. The windings 36 and 16 form a high frequency rotating transformer which will be referred to hereinafter as HFRT. How the REG excites the windings 38 of the PGM will be described below in more detail.

The general operation of the electric machine system of FIG. 1 will be described hereinafter with reference to FIG. 1. The alternating current signals: phase 1, phase 2 and phase 3, cause excitation of windings 28 on the stator 12. This excitation of the windings 28 also causes excitation of the windings 38 positioned on the rotor 10. The field resulting from the excitation creates a torque which causes the rotor 10 to rotate as is conventionally known for three phase wound rotor induction electric motors. This electric machine system, however, differs from conventional system in that it includes the REG portion of the system.

The REG portion of the system may serve to step up or step down the excitation voltage in the windings 38, so as to provide a higher dynamic range of rotor speeds. This stepping up or stepping down is realized by applying the modulated signal from modulator 14 to the REG windings 16 on the stator 12. The excitation of these winding 16, in turn, brings about excitation of the windings 36 on the rotor. The signal resulting from the excitation in the windings 36 passes to the demodulator 40. This modulated signal is comprised of a carrier signal which carries the encoded modulated signals. In particular, the carrier signal carries three separate modulator signals whose phase of modulation are 120.degree. apart so as to provide balanced phase operation. Hence, one of the respective modulator signals excites each of the respective phase windings in the windings 36.

The demodulator demodulates the carrier signal so that only the information signals encoded in the carrier signal are passed to windings 38. It should be appreciated that the information signals propagate electrical power as well as encoded information. These information signals alter the excitation of windings 38. This alteration of the excitation of windings 38 may cause the above described stepping up or stepping down of rotor speed. Further, the electrical frequency and phase of the stator modulation are resolved into rotor modulation whose frequency and phase is the function of the electrical frequency and phase of the stator modulation as well as the rotor mechanical speed and position.

Although the modulator 14 is shown on the stator 12 and the demodulator 40 is shown on the rotor 10 in FIG. 1, it should, nevertheless, be appreciated that these components 14 and 40 may be reversed so that the modulator is on the rotor and the demodulator is on the stator. In addition, although the above discussion focusses on the use of a single carrier signal, it should be appreciated that multiple carrier signals may be used. Specifically, multiple carrier signals that are balanced multiple phases may be used. In such a case, each winding of the three phase HFRT is driven by a respective carrier signal. The modulation of the carrier signals would remain phase shifted.

The concepts of the classical, smooth airgap balanced two phase rotating electric machine will now be discussed to develop a mathematical analysis of the present invention. This analysis will help to explain several novel features of the present invention. Initially, it is helpful to begin with a simple single phase rotation electric machine. FIG. 2 is a schematic of such a simple single phase rotating electric machine. The machine is referred to as a smooth airgap machine so as to specify that the magnetic path seen by each winding is independent of rotor position.

The generalized Flux Relations for this type of an electric machine are:

where:

t is time;

F.sub.s is the total flux linkage of the stator windings;

F.sub.r is the total flux linkage of the rotor windings;

L.sub.r is the self-inductance of the rotor windings;

L.sub.s is the self inductance of the stator windings;

Q(t) is the instantaneous angular displacement between the axis of the stator and rotor windings;

M.sub.sr (Q(t)) is the mutual inductance between the rotor and stator windings;

I.sub.r (t) and I.sub.s (t) are the rotor and stator port currents.

The generalized terminal relations for the simple single phase electric machine are:

The Terminal Current Relations:

where:

I.sub.s (t) represents the stator port current;

I.sub.r (t) represents the rotor port current;

I.sub.s is the amplitude of the stator current;

I.sub.r is the amplitude of the rotor current;

W.sub.s is the angular frequency of the stator current;

Q.sub.s is the angular phase shift relative to the utility source;

W.sub.r is the angular frequency of the rotor current;

Q.sub.r is the angular phase shift relative to the utility source;

t is the time;

COS (W.sub.s t+Q.sub.r) is the cosine of the term (W.sub.s t+Q.sub.r).

The Terminal Voltage Relations:

where:

V.sub.s (t) is the stator port voltage;

V.sub.r (t) is the rotor port voltage;

F.sub.s is the stator magnetic flux;

F.sub.r is the rotor magnetic flux;

(d/dt)(F.sub.s) is the derivative of the function F.sub.s with respect to time.

The Torque Relation:

where:

M.sub.sr represents the mutual inductance between the stator and rotor;

(d/dQ)(M.sub.sr) is the derivative of the function M.sub.sr with respect to the angular displacement.

From these relations for a single phase machine, the relations for a two phase smooth airgap, rotating electric machine (like that of FIG. 3) may be derived. By modifying the generalized relations for the single phase machine, the terminal relations for the two phase machine are as follows:

The Terminal Voltage Relations: ##EQU1##

The Terminal Current Relations (balanced): ##EQU2##

The Terminal Magnetic Flux Relations: ##EQU3##

The Torque Relation: ##EQU4## where:

(d/dQ)(mutual inductance) is the derivative of the mutual inductance with respect to the displacement.

W.sub.s is the angular frequency of the electrical power source

Q is the instantaneous angular position between the electromechanical axis of the rotor and stator windings.

where:

W.sub.m is the "apparent" angular mechanical speed (which will be explained below) of the rotor;

t is the time;

Q.sub.1 is the relative angular position between the rotor and stator windings at a given angular velocity and time.

R.sub.as, R.sub.bs, R.sub.ar, R.sub.br are the losses (eddy current losses, resistive losses, etc.) associated with each winding arrangement. Since the machine is considered to be phase balanced,

M.sub.ar COS(Q), M.sub.br SIN(Q), M.sub.as COS(Q), and M.sub.bs SIN(Q), represent represent the mutual inductance (magnetic coupling) of each winding with any other non-quadrature winding (by definition, quadrature windings have no mutual magnetic path). The mutual inductances are a function of position. Since this discussion concerns a smooth airgap, balanced phase electric machine

where:

N.sub.s is the number of winding turns on each stator winding;

N.sub.r is the number of winding turns on each rotor winding;

L.sub.m is related to the permeance (the inverse of the core reluctance) of the magnetic circuit mutually linking a rotor and stator winding.

Permeance or its inverse, reluctance, is a function of the magnetic permeability of the magnetic material (including the air gap) and the "physical volume" (and other physical dimensions) of the mutual magnetic path linking the electrical winding.

L.sub.br and L.sub.ar are the self inductances of the rotor windings. L.sub.bs and L.sub.as are the self-inductances of the stator windings. Because a smooth airgap machine is being considered, the self inductances are not a function of rotor position and can be factored into two components. One component, L.sub.m, is related to the permeance of the mutual magnetic path and the other component, L.sub.1x (where x is "r" or "s" indicating the rotor and stator, respectively), is related to the permeance of the remaining magnetic circuits (other than the magnetic circuit attributed to L.sub.m).

Leakage inductance contributes nothing to torque development: yet, it lowers the power factor of the electric machine. Hence, in the torque producing entity of any electric machine, leakage inductance should be kept to a minimum. Unfortunately, all electric machines require an airgap between their moving and stationary bodies which is the major cause of leakage inductance for such machines. As will be shown, the electric machine system of this invention can cancel its leakage inductance.

By solving the relations of equations 8-11 and letting (W.sub.r =W.sub.s -W.sub.m), the Terminal Voltage Relations and the Torque Relation for the two phase machine are: ##EQU5##

As indicated in equation 25, constant (non pulsating) torque can only be generated when:

Under this condition, the moving magnetic field of the rotor and the moving magnetic field of the stator are synchronized. As a result:

When the relations of equations 21, 22, 23 and 24 were developed earlier, W.sub.r was equated as follows:

and the relation of equation 26 is satisfied.

In more general terms, the relation of equation 26 suggests that the electrical frequency of the rotor must be equal to the electrical frequency of the stator less the mechanical frequency (velocity) of the rotor for constant torque to be developed.

The term, W.sub.m, in the relation of equation 26 is related to the electrical or magnetic angular velocity of the rotating magnetic field and not the "true" mechanical angular velocity of the rotor. Hence, W.sub.m was previously referenced as the "apparent" mechanical angular velocity. The relationship between the "apparent" mechanical angle (Q.sub.e) and the mechanical angle (Q.sub.m) is:

where:

P is the number of electrical (magnetic) poles.

Therefore, equation 26 becomes:

where W.sub.m of equation 28 is the "true" mechanical angular displacement.

The PGM follows an analysis similar to the analysis of the two phase machine. Its terminal relations are as follows:

PGM Terminal Current Relations (balanced): ##EQU6##

PGM Terminal Voltage Relations: ##EQU7##

PGM Frequency Relation:

PGM Torque Relation:

where:

W.sub.s is the electrical angular frequency of the power supply;

W.sub.r is the electrical angular frequency of the rotor;

W.sub.m is the mechanical angular frequency of the rotor;

Q.sub.s is the electrical angular displacement of the stator signal;

Q.sub.r is the electrical angular displacement of the rotor signal;

Q.sub.1 is the mechanical angular displacement of the rotor;

M is the mutual inductance of the PGM;

L.sub.s is the stator inductance of the PGM;

R.sub.r and R.sub.s are the rotor and stator electrical resistances respectively.

The PGM entity of this invention is the torque producing entity. Accordingly, its leakage inductance (air gap) should be made as small as possible. The REG is shown schematically in FIG. 4. The discussion that follows will focus on the relations for it. For mathematical simplicity, the discussion that follows assumes Double Sideband Suppressed Carrier Amplitude Modulation (DSB). The envelope of the modulated signal is proportional to the magnitude of x(t), .vertline.x(t).vertline.; where x(t) is the modulation. Hence, both the negative and positive frequency signatures of the modulation propagate on the carrier. Whenever the modulation signal crosses zero, the modulated wave has a phase reversal. By sampling the modulated signal at the carrier frequency and being aware of the phase reversal of the modulation envelope (a demodulation technique known as Synchronous Balanced Modulation/Demodulation), full recovery of the modulation signal is assured.

The Terminal Current Relations to the REG modem are: ##EQU8##

After modulation, the Terminal Current Relations of the High Frequency Rotating Transformer (HFRT) are: ##EQU9## where:

W.sub.s is the angular frequency of the modulation (it is equal to the angular frequency of the power source supplying the PGM, ie. (60hz)(2)(PI) radians (where PI is equal to 3.14 two digits) and is generally fixed in is the angular frequency of the carrier of the

W.sub.x is the angular frequency of the carrier of the modulation. It is at least an order of magnitude larger than W.sub.s.

The development of the HFRT Terminal Voltage Relations is similar to the development of the PGM Terminal Voltage Relations. Therefore, only one phase of the HFRT will be discussed below.

The Flux relation for one phase of the HFRT is: ##EQU10## where:

Q.sub.x is the instantaneous angular position between the electromechanical axes of the rotor and stator windings:

where:

W.sub.m is the angular speed of the rotor;

t is time;

Q.sub.2 is the angular position between the rotor and stator windings at a given angular velocity and time;

After substituting equations 42 through 46 into equation 47, F.sub.asx becomes: ##EQU11## The Voltage Relation due to the changing flux of the HFRT is: ##EQU12## since W.sub.x >>W.sub.s,: ##EQU13##

The Terminal Voltage Relation of the HFRT, which includes the resistive voltage drop, becomes: ##EQU14##

After demodulating (or multiplying the modulated signal by a "time-sliced function" of the carrier signal SIN(W.sub.x t)), the Terminal Voltage Relation becomes: ##EQU15##

The (+/-) option in the previous relation is the result of using a synchronous balanced demodulator which gates (i.e., ON or OFF), the "carrier" current or voltage signals at the zero crossing of their amplitudes. As a result, the negative and positive frequency terms of W.sub.s can be combined at unipolar half periods of the sampling (or carrier) frequency.

Upon filtering the high frequency terms containing 2W.sub.x and 4W.sub.x, etc., which are harmonics of the carrier frequency, the Terminal Voltage Relation becomes: ##EQU16##

The high frequency components are reduced by the inherent filtering capabilities of the REG, particularly when operating under resonance, and by the inherent filtering capabilities of the low frequency PGM.

By the same analysis as previously performed on V.sub.asx, it follows that the Terminal Voltage Relations of the HFRT are: ##EQU17## where:

W.sub.s is the electrical angular frequency of the power supply and is the modulation angular frequency of the HFRT stator;

W.sub.r is the electrical angular frequency of the modulation of the rotor signal and is equal to (W.sub.s -W.sub.m);

W.sub.x is the electrical angular frequency of the carrier of the modulation;

Q.sub.sx is the electrical angular displacement of the stator modulation;

Q.sub.rx is the electrical angular displacement of the rotor modulation;

Q.sub.2 is the mechanical angular displacement of the rotor;

M.sub.x is the mutual inductance of the HFRT and is equal to N.sub.sx N.sub.rx L.sub.mx ;

L.sub.sx is the stator inductance of the HFRT and is equal to N.sub.sx N.sub.sx (L.sub.mx +L.sub.1sx)

L.sub.rx is the rotor inductance of the HFRT and is equal to N.sub.rx N.sub.rx (L.sub.mx +L.sub.1rx)

R.sub.rx and R.sub.sx are the rotor and stator electrical resistance of the HFRT (respectively)

There are several mathematical equations that characterize the behavior of this system. These relations are: ##EQU18## where:

W.sub.s is the angular frequency (radians/sec) of the electrical power source;

W.sub.x is the angular frequency (radians/sec) of the carrier signal;

W.sub.m is the angular frequency (radians/sec) of the rotor;

P is the number of electrical poles of the machine;

V.sub.in is the voltage amplitude of the electrical power source;

PF is the power factor of the machine;

M.sub.x is the mutual inductance of the REG;

M is the mutual inductance of the PGM;

L.sub.s is the self inductance of the PGM stator;

L.sub.L is the leakage inductance of the PGM:

R.sub.r is the rotor resistance;

p.sub.rx is the REG carrier frequency impedance;

A is the user selectable amplitude of the REG modulation;

Q.sub.user is the user selectable common phase shift of the REG amplitude;

K is a constant which accounts for multiphase arrangements.

Given the above discussion of the basic operation of the electric machine system of the present invention, it is useful to further examine several novel aspects of this system in more detail. Hence, the discussion will now focus on the modulation strategies employed by the modulator 14. The electronic modulator may be a common pulse width modulation (PWM) variety having the option of employing additional efficiency and enhancing techniques such as resonant switching technology. Furthermore, alternative modulation strategies such as matrix switching, amplitude modulation and frequency modulation are all viable modulation approaches for this invention. In fact, any modulating means which can successfully propagate electrical power signal information is a viable candidate. Still further, pulse density modulation may be employed and is perhaps the best option for facilitating the use of the resonant switching technology.

To understand the application of resonant switching technology to the electric machine system of the present invention, it is helpful, first, to look at the state of the magnetic fields involved in the system, which in this case utilizes a single phase carrier. In particular, unlike the synchronized moving magnetic fields of the PGM, the magnetic field of the REG rotor and stator do not move, but only change field amplitude at the carrier frequency, W.sub.x. Specifically, all the phase windings of the REG are excited by a high frequency carrier signal of the same phase. Because the frequency of the carrier signal is significantly greater than the frequency of the modulator signals, the rotor of the REG barely appears moving to the high frequency magnetic field produced by the carrier signals. Essentially, the REG is acting as a classical electrical transformer operating under single phase principles and at the carrier frequency W.sub.x.

The effective impedances of the self inductance terms, L.sub.sx W.sub.x and L.sub.rx W.sub.x, where L.sub.sx is the self inductance term of the stator of the REG at its high frequency of operation (i.e., the carrier frequency W.sub.x), can be modified by strategically placing resonating capacitors either in series or in parallel with these self inductance terms. Because of the high frequency of operation of the carrier signal W.sub.x, the electrical capacitance and the physical size of these resonating capacitors is small.

The frequency of resonance occurs when:

where:

W.sub.r is the resonance frequency of the circuit;

L is the inductance of the resonating circuit; and

C is the capacitance of the resonating circuit.

After implementing the series placed method of resonance with a resonating capacitor, C.sub.x, the previously described self inductance terms act as a band pass filter and their effective impedances are as follows: ##EQU19##

Similarly, in implementing the parallel placed method of resonance with a resonating capacitor, C.sub.x, the self inductance terms act as a band pass filter and their effective impedances can be expressed as follows: ##EQU20##

It can, thus, be seen under resonance, that the REG serves as a band pass filter to block the low frequency components (i.e., the modulation frequency W.sub.s) and passes the high frequency component (i.e., the carrier frequency W.sub.x). Further, it serves to block the harmonics of the carrier frequency (e.g., 2W.sub.x,4W.sub.x,...). As a result of this filtering effect, the resonant switching technology can significantly alter the effects of the self inductance terms.

In addition, it may be beneficial to institute additional inductance into each phase of operation to decrease the size of the capacitors needed to implement resonance rather than depending solely on the leakage inductance of the REG. With the addition of mutual windings, these additional inductors may function as current sensor for the control electronics. Although these additional inductors are separate from the leakage inductance of the REG, they may be integrated into the structure of the REG. Further benefits realized by the resonance switching are that it greatly reduces the electrical losses and stresses of the high frequency electrical and electronic components of the REG such as power semiconductors. It also allows the otherwise parasitic parameters of the machine such as leakage inductances and capacitances to be part of the tuned electrical circuit.

Another novel aspect of the present invention is that the HFRT and the PGM are mirrored electromagnetic images of each other with one exception. The exception is that the HFRT is designed for operation in much higher electrical frequency than the PGM. As such, the HFRT is physically smaller than the PGM, and it has a much lower electrical impedance. Both rotors of the PGM and the HFRT are attached to the same body and move at the same mechanical phase and velocity. By suggesting that the HFRT and PGM are mirrored electromagnetic images, it is meant that they exhibit similar air gap magnetic field distributions which are proportional in magnitude when their field windings are excited by polyphase signals of the same frequency. It does not necessarily mean they have the same arrangement or number or position of phase windings, although this would be normal.

FIGS. 5a, 5b and 5c show more detailed electric schematics of apparatus for implementing the above described concepts using zero current resonant switching. FIG. 5a is an electrical schematic that utilizes a unipolar synchronous modulator and demodulator. As can be seen in FIG. 5a, the rotor 10 has windings 38 like that shown in FIG. 1, except that the windings are connected in a delta configuration as opposed to a wye configuration. Furthermore, the rotor has windings 36. The stator, on the other hand, has windings 28 and winding 16. All of these windings are connected in a delta configuration as opposed to a wye configuration.

In addition, resonating capacitors 52 are provided on the stator, and resonating capacitors 54 are provided on the rotor 10. Each resonating capacitor 52 and 54, in combination with the leakage inductance of its designated phase winding, implements a resonating circuit whose frequency of resonance is the carrier frequency W.sub.x. The resonating capacitors are selected so that the combined circuit, which is the resonating capacitances and leakage inductance of the HFRT rotor and stator, becomes a resonating circuit. To decrease the size of the resonant capacitor, 52 and 54, additional inductors could be placed in series (or parallel) with the windings, 16 and 36, as mentioned earlier. The capacitors 56 on the stator and 58 on the rotor block the low frequency component (i.e., the utility frequency, W.sub.x). These capacitors, however, are not mandatory because the HFRT voltage and currents are always referenced and synchronized to the power grid regardless of the mechanical speed. Lastly, capacitors 60 on the rotor bypass the high frequency component (i.e., the carrier frequency W.sub.x. They likewise are not a required component. Some additional variation to the circuit, FIGS. 5a, 5c, 5d, 6, and 7, may be needed for electrical integrity, such as flyback diodes, etc.

Switches 62 are employed on the stator 12, and switches 64 are employed on the rotor 10. These switches are bi directional power switches which implement unipolar synchronous modulation and demodulation functions on the high frequency carrier to reproduce and pass the low frequency component. By judiciously selecting the on and off times of the power switches 62 and 64 at the carrier frequency, the stored energy in the resonating circuit is passed to the rotor winding 38. The switches are controlled, on the stator, by the switch controller 50a and on the rotor, by the switch controller 50b.

FIG. 5b depicts a bipolar implementation of the system which uses bipolar synchronous modulator/demodulators. This implementation is much like the implementation of FIG. 1 except that the windings 16 are organized in pairs as are the windings 36. Each of the windings 16 on the stator 12 is center tapped and driven by a set of bi directional switches 70. Each bi direction power switch 70 is realized by using two conventional power semiconductor devices such as two SCRs or MCTs in parallel or in series with opposite polarity connections. With the use of resonant technology, the bi-directional power switches 70 switch polarity at the zero crossing points of the voltage (or current amplitudes) of the carrier signal. For the given circuit, each bi directional switch 70 remains on; once per carrier frequency period and remain on for a portion of the carrier frequency period between the zero crossing points of the current and voltage amplitudes to carrier. Switches 72 are, likewise, provided for the pairs of windings 36. These switches 72 are at opposite half cycles of the carrier frequency period of the switches 70.

Resonating capacitors 76 are provided on the stator 12 and resonating capacitors 78 are provided on the rotor 10. These capacitors 76 and 78 may serve also as commutation capacitors for their corresponding bi directional switches 70 and 72, respectively. The capacitors 56, 58 and 60 serve the same roles that their counterparts serve in implementation of FIG. 5a and may be optional. The switches are, once again, controlled by controllers 50a and 50b, respectively.

FIG. 5c presents yet another embodiment that adopts a unipolar implementation using zero voltage resonant switching. This embodiment includes the PGM windings 28 and 38 configured in a wye configuration. It also includes windings 16 and 36 for the HFRT of the REG configured in the wye configuration. The windings 16 and 36 for the HFRT of the REG are provided with bi-directional switches 84 and 86, respectively. The switches on the rotor adjacent to the windings 36 are controlled by the rotor power switch control 80, whereas the switches 84 on the stator located adjacent to the windings 16 are controlled by the stator power switch control 82. Capacitors 88 are provided on the stator, and capacitors 90 are provided on the rotor as shown in FIG. 5c.

Another alternative embodiment is depicted in FIG. 6. This is an embodiment that can be configured for a unipolar or a bipolar implementation. It is shown in FIG. 6 for a unipolar implementation. In accordance with this arrangement, the REG stator windings 36 are in series with the PGM stator windings 38. Further, the inductors 16 for the PGM which are located on the stator are not interconnected in a wye configuration; rather, they are kept separate in a non connected fashion and directly coupled to respective windings of the PGM stator winding 28. The inductors 16 are connected in series with switches 94 and capacitors 92 using zero voltage resonant switching. As mentioned above, switches 94 are depicted as unipolar switches but they may, likewise be bipolar switches.

FIG. 7 shows implementation of a system for implementing the rotating machine with zero voltage resonant switching. This block diagram shows a single phase of a possibly multiple phase winding arrangement. The rotor side of the arrangement is composed of a PGM rotor winding 38 and a HFRT rotor winding 36. The rotor side of the system also includes a resonant inductor with an integrated current sensor 100. In addition, the rotor side includes a fast edge and zero crossing point detector and peak (or level) detector 104a which is connected to the resonant inductor having an integrated current sensor 100. The detector 104a additionally connected to a synchronous demodulator controller 108. The demodulator controller 108 controls a switch 116. The switch 116 is a bi directional power switch that is triggered at the zero crossing point of the carrier signal. The circuit having the switch 116 also includes a capacitor 118 which is a rotor resonant capacitor. Although current "state" detectors are described, voltage "state" detectors may be equally applicable.

The stator side of the system shares many of the same type components as the rotor side . For instance, the stator side includes a PGM stator winding 28 and a HFRT stator winding 16. Furthermore, it includes a stator resonant inductor having an integrated current sensor 102. Still further, it includes a fast edge and zero crossing point detector 104b, a bi directional power switch 114 and a resonant capacitor 120.

The stator side, however, differs from the rotor side in that it includes a detection delta time generator 106 that is connected to a CPU module 110. The CPU module 110 is in turn, connected to a modulator 112 which may be a pulse density modulation (PDM), frequency modulation (FM), a pulse width modulation (PWM) type modulator or any modulation technique which carries electrical information and power.

The resonating circuits for this system are formed by the resonant inductors 100, 102 and capacitors 118 and 120. To understand the operation of the resonating circuits, it is useful to first examine the operation of the CPU module 110. The CPU module 110 selects the weighting for the modulation performed by the modulator 112. The CPU 110 also selects the frequency of the carrier signal and controls the on/off time for the power switch 114. The CPU 110 sends this control information as parameters to the modulator 112. The modulator, in turn, opens or closes the power switch according to the supplied parameters and generates an appropriate modulated signal.

The opening and closing of the power switches causes a secondary action in the current sensing windings of the inductors 102. If the switch closes before the zero crossing point of the voltage of the carrier signal, impulse on the current (fast edge) appears on the current sensor 104b. Frequencies much greater than the natural frequency are considered fast edge. In all cases, the current sense signal follows the voltage signal across the resonant capacitor 120 and crosses the zero and the voltage signal. The fast edge and zero crossing point detector 104b ensures that the switches are switched coincidently with the zero crossing points. This fast edge and zero crossing point event information is supplied to the delta time generator 106 by the detector 104b. The delta time generator 106 generates a time count between the fast edge and the zero crossing points. This information is then used by the CPU 110 to establish correcting pulse with information to the modulator 112 for correcting the switching time of the power switch. Therefore, compensation and correction of the inherent delays in the circuit between the turn on (and turn off) commands and the actual power switch response can be accomplished. Also, slower, less expensive electronic/electrical components may be utilized.

The resonant capacitor or inductor (as well as parasitical impedances) is effectively switched into or out of the resonant circuit by the on and off actions of the power switches (semiconductors). As a result, by judiciously selecting the on and off times of the power switches, the resonant frequency of the circuit may be actively changed. Essentially, the carrier frequency of the modulator must be substantially equal to the resonant frequency but as just suggested, the resonant frequency is adjustable. Changing the resonant frequency can have an important effect, such as adjusting the power factor of the electric machine system. This concept is inferred in the previous mathematical relations.

Similar activities occur on the rotor side of the system. In particular, the rotor has its own fast edge and zero crossing point detector 104a which supplies information like that described above for detector 104b to the demodulator controller 108. In the same fashion as described for the stator side, this allows the demodulator controller to adjust the predicted time of when to turn the rotor power switch on and off for a zero crossing point coincidence. As such, the synchronous demodulator 108 can synchronize the operation of the switch to the zero crossing points.

FIGS. 8a and 8b show an alternative implementation of the electric machine system that is similar to the embodiment shown in FIG. 7. The embodiment of FIGS. 8 and 8b differs from the embodiment of FIG. 7 in that it employs bypass capacitors 130, 132, 136 and 138 and switches 134a, 134b and 134c. These bypass capacitors 130, 132, 136 and 138 and switches 134a, 134b and 134c are not required components of the electric machine system of the present invention, but, rather, may be employed to improve performance of the system. FIG. 8a shows the use of the capacitors 130, 132, 136 and 138 for an arrangement in which the windings are series coupled. FIG. 8b, in contrast, shows the use of the bypass capacitors when a parallel coupled arrangement is employed in the electric machine system.

The bypass capacitors 130, 132, 136 and 138 provide utility line filtering and storage. The bypass capacitors 130, 132, 136 and 138 filter spikes and unwanted signals. The use of such bypass capacitors 130, 132, 136 and 138 in other applications is well known. These capacitors help to make the supply line low impedance voltage sources at high frequencies and prevent signal coupling between circuits. It should be noted that the capacitors may be conventional capacitors having suitable capacitances that are chosen to provide an impedance that is low relative to what is being bypassed. As suggested earlier, these capacitors may be selected to establish a resonating circuit that resonates at the frequencies of the A.C. utility power source.

In FIG. 8b, only bypass capacitors 130 and 132 are employed. Fewer bypass capacitors are required on this parallel coupled arrangement because there is not the direct coupling of the PGM and REG windings on the stator 12. These capacitors serve functions similar to those employed in FIG. 8a.

In general, additional bypass storage capacitors may be employed across the terminals of the PGM in the parallel connected arrangement, across the terminals of the REG in the series connected arrangement or across the terminals of both the PGM and REG in the series connected arrangement. In general, these bypass capacitors are more beneficial on the stator side rather than on the rotor side of the system.

The alternative embodiment of FIGS. 8a and 8b employs switches 134a, 134b and 134c. Each of these switches 134a, 134b and 134c is connected to a respective phase signal designated as PH1, PH2 and PH3, respectively, in FIGS. 8a and 8b. These switches serve as "reversing switches" like those commonly used in various commercial applications. The switches serve to interchange two of the three phase terminals of the electric motor system. These switches 134a, 134b and 134c may be either electromechanical switches or electronic switches. It should be noted that although a reversible switch is not essential for reversible operation of the electric machine system of the present invention, the use of the reversible switch allows for lower power ratings and reduce cost.

There may be as many switches are there are phases of the electric utility. For example, if there are six phases, six switches are employed. Similarly, there may be only two switches employed when two phases of the electric utility power are available. These switches serve to reverse the motion direction of three phase electric machine in the embodiments shown in FIGS. 8a and 8b exercised by the CPU module 10.

Another optional feature that may be incorporated into the present and is shown in FIGS. 8a and 8b is that the PGM rotor winding and the REG rotor winding may be connected to alternate phases (i.e., different ones of the phases PH1, PH2 and PH3). As an example, PGM rotor phase 1 may be connected to REG rotor phase 1 or, alternatively, PGM rotor phase 1 may be connected to REG rotor phase 2. This same idea may be applied equally to the stator phase windings.

FIG. 9 depicts yet another alternative embodiment of the present invention that is analogous to the embodiment shown in FIG. 7 but differs in that it employs bypass capacitors 130 and 132 and a direct current winding assembly (see 28 in FIG. 9). Thus, this winding may be an alternating current winding or a direct current winding. Further, this winding may be realized as a permanent magnet assembly.

While the present invention has been shown with respect to preferred embodiments thereof, those skilled in the art will know of other alternative embodiments which do not depart from the spirit and scope of the invention as defined in the appended claims.