Feedforward parameter estimation for electric machines

Abstract

A method and system for estimating a parameter of an electric machine, including a controller and a switching device, the controller responsive to at least one of: a current sensor, and a temperature sensor. Where the controller executes a parameter estimation process, which is responsive to at least one of: a current value and a temperature estimate and the resultant of the parameter estimation process representing an estimated parameter of the electric machine. The parameter estimation includes a method for estimating a temperature of the electric machine comprising: the temperature sensor operatively connected to and transmitting a temperature signal corresponding to a measured temperature to a controller, which executes the temperature estimation process responsive to a temperature signal from the temperature sensor.

Description

BACKGROUND

Electric machines, for example, permanent magnet (PM) motors as may be employed in electric power steering system (EPS) are affected by parameter variations, which impact the overall system performance as a function of temperature, build and changes over life. The motor circuit resistance, R; inductance, L; and the motor torque/voltage constant, K_e; are the three primary parameters, which affect motor control and performance. Over normal operating temperature, the motor circuit resistance, R changes by up to 60 to 70%: the motor inductance, L varies a modest amount; and the motor constant, K_e varies by as much as +/−7%. In addition, both the motor circuit resistance, R and motor constant, K_e exhibit variations of about +/−5% for build and a degradation of approximately 10% over the life of the system. The motor resistance, R increases with life and the motor constant, K_e decreases over life. On the other hand, build variations of the motor parameters tend to be randomly distributed. Therefore, without some form of temperature, build, or duration/life dependent compensation, the variations in motor output torque and system damping will result in decreased performance of the power steering system.

To account for variations in the resistance R only, a resistance estimation methodology was conceived of and described in pending commonly assigned U.S. Patent application Ser. No. 60/154,692, by Sayeed Mir et al. While able to correct for variations in resistance R due to temperature, build, and life, and well suited for its intended purposes, the correction scheme disclosed in that invention was not always capable of addressing varied motor operating conditions. For example, such conditions may include, when the motor is at stall, in quandrant II of the torque vs. velocity plane, at low currents, or at high motor velocities. In a vehicle employing an electronic steering system significant time may be spent at stall and low motor currents (highway driving for example), and large change in temperature may occur during these periods. Most correction schemes are configured to make corrections very slowly, this, it may require significant time to eliminate such an error. Of further significance, existing design schemes may not account for variation in other motor parameters, such as motor constant, which may vary significantly over temperature, build, and life.

Steering systems currently exist which employ the use of current controlled motors. In order to maintain the desired current levels as the temperature in the system varies, these current controlled motors are typically equipped with current sensors as part of a hardware current loop. However, there are also other motor designs in existence that, for cost purposes, require the use of a voltage mode controlled system. In such a situation, the same methods described above compensate for temperature in the current controlled motor cannot be applied to the voltage-controlled motor in a cost effective manner. Without the benefit of numerous expensive sensors, it becomes necessary to obtain accurate estimations of motor resistance R, motor constant Ke, and temperature readings for voltage control, which accurately controls motor torque.

SUMMARY OF THE INVENTION

A steering for estimating a parameter of an electric machine, comprising: a controller operatively connected to a switching device, which is operatively connected between the electric machine and a power source, the switching device being responsive to the controller; and at least one of: a current sensor operatively connected to and transmitting a current value indicative of a current in the electric machine, and a temperature sensor operatively connected to and transmitting a temperature signal corresponding to a measured temperature to the controller. Where the controller executes a parameter estimation process, which is responsive to at least one of, a current value indicative of a current in the electric machine, the temperature value, and a resultant of the parameter estimation process representing an estimated parameter of the electric machine.

A method for estimating a parameter of an electric machine, comprising: receiving at least one of: a current value; and a temperature value. The parameter estimating is a resultant of a parameter estimation process responsive to one or more of the current value, and the temperature value responsive to a temperature estimation process.

A storage medium encoded with a machine-readable computer program code for estimating a parameter of an electric machine. The storage medium including instructions for causing controller to implement the method for estimating a parameter of an electric machine as described above.

A computer data signal embodied in a carrier wave for estimating a parameter of an electric machine. The computer data signal comprising code configured to cause a controller to implement the method for estimating a parameter of an electric machine as described above.

BRIEF DESCRIPTION OF THE DRAWINGS

Referring now to the drawings wherein like elements are numbered alike in the several figures:

FIG. 1 is a block diagram depicting a motor control system;

FIG. 2 is a block diagram of an exemplary temperature estimation system;

FIG. 3 is a block diagram depicting a model of the thermal characteristics for a motor, a motor controller, and a temperature estimation filter;

FIG. 4 is an illustrative graphical depiction of the unit step response of the block diagram models in FIG. 3;

FIG. 5 is a block diagram of an exemplary embodiment of a temperature estimation filter;

FIG. 6 is a table of the characteristics of the filters shown in FIG. 5;

FIG. 7 is a schematic of a filter initialization implementation;

FIG. 8 is a block diagram depicting an alternative temperature estimation implementation;

FIG. 9 is a block diagram depicting an alternative embodiment for temperature estimation with ambient temperature estimation;

FIG. 10 is a block diagram representing the use of the temperature estimates in parameter calculations;

FIG. 11 is a block diagram depicting the combined feedforward/feedback estimation process; and

FIG. 12 depicts a K_e estimator error signal gain as a function of motor velocity.

DETAILED DESCRIPTION OF AN EXEMPLARY EMBODIMENT

In many practical applications of motor control, such as electronic power steering systems, it is often the case that cost and design considerations prohibit the use of temperature sensors placed directly on the motor windings or the magnets. However, such data is used to maintain motor torque accuracy over temperature, build, and life variations of the key parameters in a voltage mode controlled system. To insure adequate torque control and operation of a motor in an electronic power steering system it has become desirable to compensate the control of the motor for variations in motor parameters such as, but not limited to, motor resistance R, and motor constant K_e as a function of temperature, build, and life. In a motor control system, a motor employing voltage mode control is controlled via an applied motor voltage, not the motor current. However the torque produced by the motor is proportional to the motor current. Therefore, variations of the motor parameters such as those described directly impart inaccuracies in the control system. The motor parameter variations generate direct torque variations and accuracy errors as a function of build, life, and temperature variations. Therefore, a system that compensates for motor parameter variations as function of temperature, build, and life may exhibit improved response and more accurate control. As such, a motor parameter estimation/compensation scheme that accounts for such variations is disclosed. Generally, build and life deviations may be compensated for by means of long-term compensation of modeled motor parameters. This is usually the case because such deviations vary slowly over the operational life of a motor. However, the temperature variations induced become much more evident as a result of the repeated operational cycling of the electric motor. Therefore, emphasis on temperature estimation addresses the evident temperature dependent characteristics of the motor parameters being estimated. Thus, a detailed analysis supporting the estimation of various temperatures within the system is provided to facilitate the motor parameter estimation.

Disclosed herein in the several embodiments are methods and systems for estimating the temperature and parameters of an electric machine. More particularly, the disclosed embodiments identify models to simulate the variation of the motor parameters as a function of temperature, build and life. Particular to this variation is identification of the coefficients that characterize the change in the motor parameters with temperature, and predictions for build, and life variations. For example, for the temperature variation, the models simulate the effects of three coefficients: first, the thermal coefficient of restivity of the substrate silicon in the switching devices employed to control the motor; second, the thermal coefficient of resistivity of the copper utilized in the motor; second, the thermal coefficient of magnetic field strength of the magnets employed in the motor. Likewise, selected estimates define and characterize the variations in the motor control system components as a function of build and life.

The disclosed methodologies include, but are not limited to, feedback methodologies and predictive or feedforward methodologies. In addition, combined methodologies utilizing both feedback and feedforward parameters estimation are disclosed. An exemplary embodiment of the invention, by way of illustration, is described herein and may be applied to an electric motor in a vehicle steering system. While a preferred embodiment is shown and described, it will be appreciated by those skilled in the art that the control system employing an electric machine where parameters and temperature estimates are desired.

Referring now to the drawings in detail, FIG. 1 depicts a PM electric machine system where numeral 10 generally indicates a system for controlling the torque of a PM electric machine (e.g. a motor), hereinafter referred to as a motor 12. The torque control system hereafter system 10 includes, but is not limited to, a motor rotor position encoder 14, a velocity measuring circuit 16, a current measurement device (not shown), a controller 18, power circuit or inverter 20 and power source 22. Controller 18 is configured to develop the necessary voltage(s) out of inverter 20 such that, when applied to the motor 12, the desired torque is generated. Because these voltages are related to the position and velocity of the motor 12, the position and velocity of the rotor are determined. The rotor position encoder 14 is connected to the motor 12 to detect the angular position of the rotor denoted θ. The encoder 14 may sense the rotary position based on optical detection, magnetic field variations, or other methodologies. Typical position sensors include potentiometers, resolvers, synchros, encoders, and the like, as well as combinations comprising at least one of the forgoing. The position encoder 14 outputs a position signal 24 indicating the angular position of the rotor. The current measurement device, detects the current provided to the motor 12 and transmits a signal to the controller 18 indicative of the current value. In an exemplary embodiment, the current is measured at the inventer 20, however, it is evident that the current could be measured at any location convenient to a particular implementation. Moreover, it should also be evident that other equivalent means of ascertaining the value of the current are possible.

In an exemplary embodiment and referring also to FIG. 2, the temperature of the motor 12 is measured utilizing one or more temperature measuring device(s) of sensor(s) 13 located at the substrate of the switching device which controls the application of excitation voltage to the motor 12. It should be understood that while an exemplary embodiment decloses placing a temperature sensor 13 at the switching device substrate, various other locations are possible. Alternative locations may include placement in or in proximity to: the motor 12, the controller 18, and the like. The temperature sensor 13 transmits a temperature signal 23 to the controller 18 to facilitate the processing prescribed herein. Typical temperature sensors include, but are not limited to, thermocouples, thermistors, resistive thermal devices (RTD), semiconductors, and the like as well as combinations comprising at least one of the foregoing, which when appropriately placed provide a calibratable signal proportional to the particular temperature.

The positional signal 24, velocity signal 26, temperature signal 23, current value, and a torque command signal 28 are applied to the controller 18. The torque command signal 28 is represented of the desired motor torque value. The controller 18 processes all input signals to generate values corresponding to each of the signals resulting in a rotor position value, a motor velocity value, a temperature value and a torque command value being available for the processing in the algorithms as prescribed herein. It should be noted that while a velocity signal 26 is disclosed as derived from other measured parameters, e.g., motor position, in an exemplary embodiment, such as signal may also be a measured signal. For example, motor velocity may be approximated and derived as the change of the position signal 24 over a selected duration of time or measured directly with a tachometer or similar device.

Measurement signals, such as the abovementioned are also commonly linearized, compensated, and filtered as desired or necessary to enhance the characteristics or eliminate undesirable characteristics of the acquired signal. For example, the signals may be linearized to improving processing velocity, or to address a large dynamic range of the signal. In addition, frequency or time based compensation and filtering may be employed to eliminate noise or avoid undesirable spectral characteristics.

The controller 18 determines the voltage amplitude V_ref 31 required to develop the desired torque by using the position signal 24, velocity signal 26, and torque command signal 28, and other motor parameter values. The controller 18 transforms the voltage amplitude signal V_ref 31 into three phases by determining phase voltage command signals V_a, V_b, V_c from the voltage amplitude signal 31 and the position signal 24. Phase voltage command signals V_a, V_b, and V_c are used to generate the motor duty cycle signal D_a, D_b, D_c 32 using an appropriate pulse width modulation (PWM) technique. Motor duty cycle signals 32 of the controller 18 are applied to a power circuit or inverter 20, which is coupled with a power source 22 to apply phase voltages 34 to the stator windings of the motor in response to the motor voltages command signals. The inverter 20 may include one or more switching devices for directing and controlling the application of voltage to the motor. The switching devices may include, but need lot be limited to, switches, transmission gates, transistors, silicon controlled rectifiers, triacs and the like, as well as combinations of the foregoing. In this instance, for example, silicon power transistors, often MOSFETs, are employed.

In order to perform the prescribed functions and desired processing, as well as the computations therefore (e.g., the execution of voltage mode control algorithm(s), the estimation prescribed herein, and the like), controller 18 may include, but not limited to, a processor(s), computer(s), memory, storage, register(s), timing, interrupt(s), communication interfaces, and input/output signal interfaces, as well as combinations comprising at least one of the foregoing. For example, controller 18 may include signal input signal filtering to enable accurate sampling and conversion or acquisitions of such signals from communications interfaces. Additional features of controller 18 and certain processes therein are thoroughly discussed at a later point herein.

Temperature Estimation

Identified herein as exemplary embodiments are methodologies for estimating motor parameters from the components of the temperature as measured from the power transistor substate. Understanding the origin of these temperature components helps to identify and quantify the relationship between the power transistors and motor. Therefore, it is important to appreciate and understand the principles of conversation of energy (first law of thermodynamics) particularly as applied to the disclosed embodiments. Equation (1) states the first law of thermodynamics:E_in+E_g−E_out=E_st  (1)where E_in is the energy added or transferred to a system; E_g is the energy converted to thermal energy manifested as heat; E_out is the energy transferred out of a system or released to the ambient; and E_st is the energy stored in the system.

A system 10 as depicted in FIG. 1 may include, but is not necessarily limited to, three primary components to affect control, in this instance of a vehicle: a motor, a controller and an assist mechanism. Within the system mechanical, electrical, and electromagnetic energy are converted to thermal energy (E_g). Electrical energy is converted to thermal energy in the controller from various components. For example, a voltage regulator, shunt resistor, bus capacitors, power relay, power transistors, and the like as well as other various electronic components. The motor 12 also converts electrical energy into thermal energy in the copper windings. The core losses in the motor 12 are minimal and therefore electromagnetic heating is neglected with respect to thermodynamic considerations. The assist mechanism provides mechanical force multiplication and converts mechanical energy into thermal energy in the form of heat generated from fiction. Some of these energies are stored within components (E_st), while others are released to the ambient environment within the system by convection (E_out). In addition, the energy transferred to the ambient may also enter other components (E_in). Finally, energy may be supplied from outside the system 10. The vehicle heating system, for example, in automobile applications could potentially cause an 80° C. temperature rise under certain conditions.

To facilitate effective temperature estimation the relationship between the measured temperature and the transistor silicon, motor copper windings, and motor magnet temperatures is determined. Temperature estimation may be complicated, in that the measured temperature to be utilized may include multiple coupled components. Therefore, separating these components from a single measured temperature is desirable to enhance the accuracy of a temperature estimate. Identified herein in the exemplary embodiments are components of the power transistor substrate temperature and a methodology for performing the temperature estimation.

For the purpose of this analysis, consideration will be given to four components of the measured temperature: convection from the motor; conduction and convention from the power transistors; convection from the controller 18 electronics; and the convection from the vehicle. To illustrate the temperature estimation, equations are derived for the motor copper winding and the transistor silicon temperatures. Therefore, the additional components are identified. Finally, a temperature estimation algorithm will be identified that includes all the components.

A description of the time differential of energy (i.e., power) relates the temperature the copper windings of the motor 12 to the silicon temperature of the power transistor. The power generated from electrical energy is the product of the motor current I squared and electrical resistance R. The electrical resistance R is a function of geometry I/A, conductivity σ and temperature T.

$\begin{array}{cc}\begin{array}{c}{\stackrel{.}{E}}_x=I^{2}R,R\\ =\frac{l}{\sigma A}\left(1+\mathrm{a\Delta }T\right)\end{array}& \left(2\right),\left(3\right)\end{array}$

When the power transistors are activated current conducts through the transistors' silicon and the motor copper windings. The power stored is a function of volume V, density ρ, specific heat c, and temperature T.

$\begin{array}{cc}{\stackrel{.}{E}}_x=\rho \mathrm{Vc}\frac{dT}{dt}& \left(4\right)\end{array}$

Convection is a function of the coefficient of convection h, surface area A_s, and the difference in surface temperature T_s and a boundary layer temperature defined here as ambient temperature T_a. In the instance of the exemplary embodiment disclosed herein, for simplicity, the power transistors and motor windings share the same ambient temperature within a few degrees of each other.E_out=hA_s(T_s−T_a)   (5)

Therefore, when equations (2), (4), and (5) are substituted into equation (1) to sum the associated energy in the system, the relationship in thermal power output between the silicon and copper becomes a function of geometry (I,A,A_s,V), mass, material properties (σ, ρ, c, h) and temperature.

$\begin{array}{cc}{I}^{2}R-{\mathrm{hA}}_E\left(T_a-T_e\right)=\rho \mathrm{Vc}\frac{dT}{dt}& \left(6\right)\end{array}$

Equation (6) may be solved for the surface temperature T_s, thereby yielding in equation (7) two seperate temperatures: an ambient temperature T_a, and a surface temperature T_s representing the substrate temperature value 25 (or motor temperature). The ambient temperature T_a includes the convection from the vehicle and controller electronics. The surface temperature T_s includes convection from the power transistors of the inverter 20 or motor 12. The measured substrate temperature value 25 (as linearized) is separated from the power transistors by a conduction path. This conduction path is considered when assigning values to h, A, ρ, V and c for the substrate. Moreover, the I²R loss in the silicon is transferred across a thermal conduction path characterized by k·A/L where k is the coefficient of thermal conductivity of the silicon substrate. Consideration of this k·A/L conduction path is not represented in equation (7) for the representation of the substrate temperature value 25 (or motor temperature).

$\begin{array}{cc}{T}_a=T_e+\frac{I^{2}R}{{\mathrm{hA}}_E}\left(1-\exp \left(-t\frac{{\mathrm{hA}}_E}{\rho \mathrm{Vc}}\right)\right)& \left(7\right)\end{array}$

It is noteworthy to recognize that because the current is shared between the silicon and copper, equation (7) indicates that the difference in a change in temperature above ambient between the copper and the silicon is characterized by material properties (h, σ) and geometry of both the copper and the silicon. Recall the limit of exponentials as time goes to infinity.

$\underset{l=\infty }{\lim }\exp \left(-\tau \frac{{\mathrm{hA}}_s}{\rho \mathrm{Vc}}\right)=0$

The steady-state temperature rise above ambient for the substrate and motor now becomes more apparent.

$\begin{array}{c}\Delta T_g=\frac{I^2{R}_{\mathrm{cg}}}{h_{\mathrm{si}}{A}_{g,\mathrm{si}}},\\ \Delta T_{\mathrm{cg}}=\frac{I^2{R}_{\mathrm{cg}}}{h_{\mathrm{si}}{A}_{s,\mathrm{cg}}}\end{array}$

To find the difference in the total change in temperature above ambient between the copper and the silicon find the ratio of the steady-state temperature rise. Notice how the current term cancels out.

$\begin{array}{cc}\frac{\Delta T_{\mathrm{cg}}}{\Delta T_{\mathrm{si}}}=\frac{R_{\mathrm{cx}}{h}_{\mathrm{si}}{A}_{x,\mathrm{si}}}{R_{\mathrm{si},}{h}_g{A}_{x,\mathrm{cx}}}& \left(8\right)\end{array}$

Equations (7) and (8) illustrate a principle that may be employed to implement the temperature estimation. Under close examination it may be demonstrated that a filter (in this instance, first order) and gain may be implemented to have a response to a measured temperature, which would duplicate these results when the ambient temperature T_a is treated as a separate component. The time constant in equation (7) is

$\frac{\rho \mathrm{Vc}}{h{A}_s}$ When equation (7) is applied to the measured silicon, this time constant is used to calibrate the lead portion of all three filters since it is the silicon that is actually being measured. In other words, the dynamics of the measured substrate temperature is cancelled out. When equation (7) is applied to the motor copper windings, magnet and power transistors these time constants are used to calibrate the lag portion of all three filters. In other words, the dynamics of the motor copper winding, magnet and power transistors are estimated. The frequency of the filters is determined from the time constants in the following equation.

$\begin{array}{c}f=\frac{1}{2\pi \tau }\\ =\frac{{\mathrm{hA}}_g}{2\pi \rho \mathrm{Vc}}\end{array}$ The gains are determined by the ration of the steady-state delta-temperatures described in equation (8).

An exemplary embodiment includes a method and system for temperature estimation of the power transistor silicon, motor copper windings and rotor magnets of a motor 12 in accordance with the abovementioned disclosure and analysis. This is achieved by measuring at least one temperature, in this instance, on the power transistor substrate. This measured temperature is then processed to estimate all three temperatures utilizing the abovementioned filter estimation.

Feedforward Parameter Estimation and Temperature Estimation

An expemplary embodiment includes a motor control method and system employing a process for temperature estimation of the power transistor silicon, motor copper windings and rotor magnets is accordance with the abovementioned disclosed and analysis to facilitate motor parameter estimation. This is achieved by measuring at least one temperature, in this instance, on the power transistor substrate. This measured temperature is then processed to estimate all three temperatures utilizing filter estimation, the abovementioned analysis, which is provided above.

An exemplary embodiment includes a feedforward parameter estimation method and system by which actual operating motor temperatures and parameters may be estimated. FIG. 2 depicts a block diagram for practicing an exemplary embodiment. The requisite processing for performing the method disclosed may, but need not be performed in controller 18. Such processing may also be distributed to or across a variety devices provided in the system 10 as desired and necessary for practicing the invention. Referring also to FIG. 1, a temperature sensor 13, is used to directly measure the temperature of motor controller 18 for an electric motor 12. The temperature sensor 13 is preferably affixed to a power transistor substrate (not shown), which is a component of the motor controller 18 or inverter 20. It should be noted that the temperature sensor 13 as described may also be placed in other locations as practical considerations permit. Moreover, placement may also be internal to the motor 12, controller 18, or inverter 20 or external. In either instance appropriate consideration of the thermodynamic considerations is preferred to ensure generation of an accurate thermal model. In an exemplary embodiment, motor parameters are estimated and compensated as a function of temperature. To further enhance the compensation and estimation, and yet address the cost ramifications of additional sensors, the application of multiple sensors is reduced by further estimation of temperatures in the motor controller 18 and electric motor 12. Therefore, multiple embodiments are disclosed herein disclosing various means for temperature determination and ultimately motor parameter estimation.

Referring once again to FIG. 2, to determine a temperature estimate, the output of a temperature sensor 13, temperature signal 23 is transmitted through a linearization function mechanism 15 to compensate for non-linearities in the measurement. Linearization function mechanisms are well known in the art and may comprise either hardware or software embodiments, or a combination of both. Thereafter the linearized temperature signal denoted the substrate temperature value 25 is directed to a temperature estimation process 100, the output of which represents the temperature estimate 70.

One example of a temperature estimation process 100 as depicted in FIG. 2, may comprise a simple low pass filter having a cut off frequency designed to estimate the thermal time constant of the motor. However, it has been found that even with careful adjustment of the time constant of such a temperature estimation process 100, the transient response may still show error between the actual temperature of the motor and the temperature estimate 70, especially under dynamic conditions. Therefore, in order to improve the transient accuracy of the filter estimate, a filter structure such as the one shown in FIG. 3 also employing lag, lead-lag, and/or lag-lead filters may be used. FIG. 4 illustrates a unit step response of an exemplary lead-lag filter estimate as compared with the both the actual motor and motor controller temperature. An error in the filter parameters has been introduced to illustrate how the estimate response closely resembles the desired response even with variation of the filter parameters.

In an exemplary embodiment as depicted in FIG. 5, multiple temperature estimation filters are employed to facilitate the temperature estimation and thereby, the motor parameters estimation. Depicted in the figure, are actually three separate estimation filters, which serve to estimate three operating temperatures in an exemplary embodiment: the temperature of the motor controller silicon, the temperature of the motor magnet and the temperature of the copper winding of the motor. Hereinafter, the three temperature estimation filters shall be referred to as the silicon temperatures estimate filter 40, the magnet temperature estimation filter 50, and the copper winding temperature estimate filter 60. It is important to appreciate that while the disclosed exemplary embodiment identifies three filters and three estimated temperatures, this should not be considered limiting. It will be apparent that the temperature estimation may be applied to as many temperature estimates or parameter estimates as desired and practical for estimation or to enhance the accuracy or response characteristics of the estimation.

FIG. 5 depicts the block diagram, which illustrates the processing of the substrate temperature value 25 (FIG. 2 as well). As can be seen, the substrate temperature value 25 is transmitted to the silicon temperature estimate filter 40, the magnet temperature estimation filter 50, and the copper winding temperature estimate filter 60. In this manner, multiple temperature estimate(s) 70, comprising; 70a for silicon, 70b for magnet, and 70c for copper temperature estimates respectively, are generated using a single temperature signal 23 from the temperature sensor 13.

Referring to FIG. 5, in an embodiment, the silicon, magnet, and copper winding temperature estimate filters 40, 50, and 60 are implemented as first order filters. Once again, first order lead-lag and lag-lead filters are selected because equation 7 indicates such a filter implementation will provide an accurate estimate with the expected response characteristics. The range of the lead and lag filters and gain amplifiers is intended to cover multiple levels of controller and motor thermal coupling, placement within vehicle, convection schemes, power distribution and heat sink capability. Depending on the above mentioned thermal characteristics between the motor and controller the gain amplifier could be less than unity, unity or greater than unity. As shown in FIG. 6, in an exemplary embodiment, the lag frequency range of the silicon temperature estimate filter 40 is between about 53 μHz (microhertz) and about 320 μHz and the lead frequency range is between about 53 μHz and about 160 μHz. The lag frequency range of the magnet temperature estimate filter 50 is between about 35 μHz and about 80 μHz and the lead frequency range is between about 53 μHz and about 160 μHz. The lag frequency range of the copper winding temperature estimate filter 60 is between about 35 μHz (microhertz) and about 80 μHz and the lead frequency range is between about 53 μHz and about 160 μHz. The temperature estimate filters (e.g., 40, 50, and 60) respectively include an option to disable the zero or the combination of the zero and the pole yielding a low pass filter or a unity gain respectively. It will be appreciated that the temperature estimate filters 40, 50, and 60 respectively may be implemented employing a variety of methods including but not limited to passive, active, discrete, digital, and the like, as well as combinations thereof. In an exemplary embodiment, for example, each of the temperature estimation filters 40, 50, and 60 is digitally implemented and operates at the rate of about 128 milliseconds. Moreover, it should also be noted that the gain amplifiers depicted in the figures are included for clarity and completeness. It is well known that such gain amplifiers depicted with each of the temperature estimate filters 40, 50, and 60 may, like the filters be implemented employing numerous variations, configurations, and topologies for flexibility.

It is noteworthy to recognize and appreciate that because the thermal time constant of a motor winding is relatively long (over 20 minutes), it takes a long time for the temperatures of the motor 12 and the substrate to equalize after a system shutdown if the motor and substrate temperatures were significantly different upon shutdown. When the system is subsequently “powered on” again such a difference may cause an introduction of an error in the temperature estimates. To address this anomaly, an initialization scheme is employed at power application, which reduces the impact of the abovementioned temperature differences. In an embodiment, an initialization signal 80 is provided for initialization of the silicon, magnet, and copper temperature estimate filters 40, 50, and 60 respectively to the substrate temperature value 25 following linearization of the temperature signal 23 as measured by temperature sensor 13. It is also noteworthy to appreciate that such an initialization may introduce an offset error into the motor temperature estimate, which could require a relatively long time to be significantly reduced or eliminated. As a result, the system 10 may experience decreased torque accuracy until the error is sufficiently reduced. Such an offset error may be acceptable in some applications and yet be objectable in others and therefore more sophisticated initialization schemes may prove beneficial.

According, an alternative embodiment may include an additional initialization process whereby the temperature estimation process 100 (e.g., comprising filters 40, 50, and 60) continues to execute after the system 10 is shut off, until such time as the temperature estimate 27 from temperature estimation process 100 approaches a steady state value. If the temperature estimation process 100 is still running when the system is activated, then no initialization to the temperature estimation process 100 would be necessitated.

Yet another exemplary embodiment addresses the estimation filter initialization error by initializing the digital temperature estimation filter(s) (e.g., 40, 50, and 60) with reduced error using information from another sensor should it be available. In such an exemplary embodiment, an engine coolant temperature, for instance, may be available and utilized. For example, if τ_e is the time for the engine to cool by 63%, thenT_e=T_a+(T_e0−T_a)e^−t/τe   (9)

where T_e is the engine coolant temperature, T_a is the ambient temperature, and T_e0 is the hot engine coolant temperature when the ignition is first turned off. To approximate the length of time the ignition has been off equation (9) can be rewritten as

$\begin{array}{cc}t=-{\tau }_e\ln \left(\frac{T_e-T_a}{T_{e0}-T_a}\right)& \left(10\right)\end{array}$

If τ_cu and τ_m are the times for the motor windings and magnets to cool by 63% respectively, thenT_cu=T_a+(T_cu0−T_a)e^−i/τe  (11)andT_m=T_a+(T_m0−T_a)e^−i/τe  (12)

where T_cu and T_m are the motor winding and magnet temperatures and T_cu0 and T_m0 are the hot motor winding and magnet temperatures when the ignition is first turned off. Substituting equation (10) into equations (11) and (12) the motor winding and magnet temperatures can be initialized in terms of calibration time constants, recorded shut-down temperatures and the initial engine coolant temperatures:

$\begin{array}{cc}{T}_{\mathrm{cu}}=T_a+\left(T_{\mathrm{cu}0}-T_a\right){\left(\frac{T_e-T_a}{T_{e0}-T_a}\right)}^{\frac{{\tau }_e}{{\tau }_{\mathrm{cu}}}}& \left(13\right)\\ T_m=T_a+\underset{\underset{\mathrm{Filter}\mathrm{intial}\mathrm{value}}{⎵}}{\left(T_{m0}-T_0\right){\left(\frac{T_e-T_a}{T_{e0}-T_a}\right)}^{\frac{{\tau }_e}{{\tau }_m}}}& \left(14\right)\end{array}$

It is noteworthy to appreciate that the multiplication term with the present and last engine coolant temperatures T_e and T_e0 is a fraction between zero and one indicating the change in the final recorded temperatures T_cu0 and T_m0 since the system was last shut down. The product of these two terms (from equations (13) and (14)) is then employed to initialize the digital temperature filters. When the fraction term is zero the digital filter is likewise initialized to zero and the motor winding and magnet temperatures become equal to the ambient temperature as initialized before. It should be noted that many of the equations are presented as material specific. However, these equations may be generalized to apply to any material of interest by substituting the appropriate subscripts in the equations. For example, with equation (14) which is specific to the magnetic material could be generalized by substituting as follows:

$\begin{array}{cc}{T}_x=T_a+\underset{\underset{\mathrm{Filter}\mathrm{initial}\mathrm{value}}{⎵}}{\left(T_{x0}-T_e\right){\left(\frac{T_e-T_a}{T_{e0}-T_a}\right)}^{\frac{{\tau }_e}{{\tau }_x}}}& \left({14}^{\prime }\right)\end{array}$ where the m subscripts are replaced by an x to indicate a generalized application to another material.

The embodiment as disclosed may be implemented utilizing tow 2-dimensional look-up tables for each digital filter initial value. FIG. 7 depicts an implementation of equations (1) and (14) for generating the filter initialization signal 80 for the magnet and copper winding filters 80a and 80b respectively. Look-up tables 86 and 88 respectively may employ linear interpolation, quanitzation, and the like to reduce the size of, or number of entries in the tables. It should be appreciated that while an exemplary embodiment is disclosed identifying an initialization for the magnet and copper filters (e.g., 50, and 60), such an embodiment is equally applicable to any estimation filter utilized.

In yet another exemplary embodiment, the disclosure outlined above is supplemented once again with additional filtering and estimation. The scheme outlined above provides a method for enhancing the initialization of the estimation filters 40, 50, and 60 (FIG. 5) under particular operating conditions. Each of the estimation filters 40, 50, and 60 (FIG. 5) employs the ambient temperature T_a as one of the terms in the initialization equation(s) (e.g., equations (13) and (14)) to formulate the initialization signal 80. It is noted that under particular operating condition where the ambient temperature T_a varies significantly, errors may be introduced after the initial ambient temperature is recorded. For example, if the estimation process 100 are initialized under extreme cold conditions, and then heating causes the ambient temperature to rise significantly. Under close examination of equations (7) and (8) it should also be evident that once again a simple filter and gain may be employed to accurately estimate the delta-temperature (e.g., the change in temperature above ambient) from a measured current and resistance when the ambient temperature is treated as a separate component. In an embodiment, a first order low-pass filter is utilized to simulate the desired response. FIG. 8 depicts a block diagram of a motor temperature estimation filter 150 employing this methodology. An alternative motor delta-temperature estimate signal 27a is generated by the motor temperature estimation filter 150. By using this alternative means of motor delta-temperature estimation as a reference, the ambient temperature recorded at initialization can be adjusted where appropriate. This alternate motor delta-temperature estimation can be processed from a current estimation and the motor resistance estimation features disclosed herein. The change in motor temperature with no other contributing factors, addressing only convection, can be simplified in the following equation:ΔT_m=I²R_mR_therm(1−e^−t/τ)  (15)where I represents a peak phase current of the motor (e.g., the total heat producing current), R_m represents the resistance of the motor as may be estimated by the embodiments disclosed herein and R_therm represents the thermal resistance associated with convection, represents the thermal time constant related to the heat transfer through the motor 12, the system 10 and the temperature control system. In an embodiment, a calibratable filter 152 provides the time element and a gain 154 provides for the thermal resistance R_therm and other system variables. These other variables include convection and heat transfer from the controller. In an embodiment, the calibratable filter 152 may be a first order low pass filter. Although the time constant of the heat transferred from the controller may vary from the motor, it contributes as little as 10-15° C. It should be noted that this delta-temperature estimate is implemented as a motor delta-temperature estimate. It therefore follows that a silicon or magnet delta-temperature estimate may be implemented in a similar manner as well.

Referring now to FIG. 9, a block diagram depicting the combined ambient temperature estimation/initialization scheme integrated with the estimation process 100. These two approaches provide two methods of estimating the change in surface temperature from equation (7) without an estimation of the ambient temperature T_a. While the first method requires that a measured ambient temperature T_a be known before filtering, the second method does not. Therefore, when these two methodologies are combined an estimation of the ambient temperature T_a is the result. This is illustrated in FIG. 9 for the copper temperature estimation filter 60 as it may be implemented. It should be noted that the motor temperature estimation filter 150 as depicted in FIG. 8 may be further simplified to facilitate ease of implementation and processing burden for controller 18 by once again employing a lookup table 156.

It may be the standard condition or operation to use the initial substrate temperature 25 at start-up as the initial ambient temperature T_a. An accuracy range check may be employed to determine whether the ambient temperature estimation disclosed is needed and used to compensate the initial ambient temperature. Similar to the previous estimation methodologies, another filter (not shown), may be used to provide a slow and smooth transition from an initial ambient temperature to a new ambient temperature estimate. An offset term for trim adjustment is also included to account for constant heat transfer, known errors, and unanticipated errors and biases. When this delta motor temperature estimate 27 is substrated from the estimate temperature (in this instance the winding copper temperature estimate 70c) the result is an estimation of the ambient temperature T_a. The estimated ambient temperature may thereafter be employed to compensate the respective temperature estimates e.g., 70a, 70b, and 70c as depicted at ambient temperature compensator 158.

It should be noted that this exemplary embodiment only utilizes one filter with estimate of ambient temperature T_a (e.g., depicted with the copper estimation filter 60) as depicted in FIG. 9. The same ambient temperature estimate may, but need not be, utilized for additional parameter temperature estimation filters. For example, for the magnet temperature estimate, the same scheme may be employed, however, for the silicon estimation filter, to account for the previously mentioned difference in the ambient temperature for the controller 18 and the motor 12, an additional offset calibration should be added to the ambient temperature estimate. Additionally, it should be noted that the initial value of the measured substrate temperature value 25 may be adequate as the ambient temperature T_a over the duration of the system operation within a required threshold. Then, if or when the ambient estimation crosses such a threshold as may occur during excessive controller or vehicle heating the initial value is compensated by an additional ambient temperature estimation process following the (copper) estimation filter 60. It should also be noted that the compensated ambient temperature estimate may further require adjusted sealing in response to the gain now applied within the copper estimation filter 60.

Turning now to FIG. 10, a block diagram depicting a feedforward parameter estimation process 110 employing the abovementioned temperature estimation process(es) 100 is depicted. Deriving accurate temperature estimates of the various motor and system components facilitates the estimation and calculation of motor parameter value and therefrom, determination of the correct operating voltage to command the motor 12 (ses also FIG. 11). Once again, in an embodiment, the calculations may be accomplished either by using lookup tables to simplify and expedite processing or by solving the equations. FIG. 10, as well as FIG. 11 illustrate an example of how such temperature estimation data may be processed to calculate the total motor circuit resistance and motor constant and thereafter, the correct motor operating voltage in response to temperature changes. Nominal parameter value 82 (in this instance, for the transistor silicon resistance as well as the motor copper resistance and motor constant K_e) are used as inputs, along with the temperature estimates 70, into the corresponding parameter calculation blocks 90, 92, and 94. The equation of all three parameter calculation blocks 90, 92, 94 are the following form:Actual Parameter Value=(Nominal Value @T_nom)*(1+Thermal Coeficient*(T_act−T_nom))   (16)where T_nom is the temperature at which the nomincal parameter value is defined, Thermal Coefficient is the thermal coefficient of the thermally sensitive material of the parameter being calculated (such as the temperature coefficient of resistivity of copper for the motor resistance), and T_act is the actual temperature of the material.

It should, however, be noted that the diagram in FIG. 10 depicts three temperature estimates 70a, 70b, 70c (e.g., silicon, copper, and magnet) used in the parameter calculation, are employed. However, it should be evident that the same technique shown in FIG. 10 may logically be applied using any number of temperature estimates.

Enhanced Feedback Parameter Estimation

Feedforward parameter estimation provides as open loop means of approximating the variations in the motor parameters with temperature. Even with such estimation, because the models are not exactly correct, there will still be an error in the temperature estimates. Moreover, life degradation of the machine parameter values cannot be accounted for and compensated. Finally, the parameter changes due to build variation may only be addressed utilizing 100% part evaluation and calibration, which would require additional time and cost to manufacturing. A closed loop (feedback) approach utilizing error integrators allows for compensation of the slowly changing build and life variations. Errors in temperature estimates in resulting parameter estimation errors may also be compensated.

An exemplary embodiment includes one or more conditional integrators for accumulating and correcting both motor circuit resistance R errors and motor constant K_e errors. The integration conditions are determined by the accuracy of the error signal for each integrator. In addition, error integration for R estimation occurs in the low velocity/high torque command region of motor operation and error integration for K_e occurs in a high velocity/low torque command region. This is due to the fact that at low velocities, the resistance error signal equation is more accurate, while at high velocities the K_e error signal equation is more accurate.

Referring now to FIG. 11 depicting combined feedforward methodology 120 and feedback methodology 130 for parameter estimation as may be implemented and executed by the controller 18. Generally, in a voltage control scheme, a torque command signal T_CMD 28, which identifies the desired torque command, is utilized along with the current motor velocity ω to generate voltage and phase advance angle δ commands to the motor. Moreover, the torque command signal T_CMD 28 may include envelope and magnitude limiting, or other such processing and the like, to control the signal characteristics. Controller 18 may also include such processing, the motor control and estimation processing as may be present in an inverse motor model 112 may also take advantage of estimates of motor parameters such as resistance R, inductance L, and motor constant K_e.

The embodiment also includes conditional integrators 104 and 106 (e.g., they integrate their inputs only under predefined conditions) for correcting both motor circuit resistance R (104) and motor constant K_e (106). The conditional integrators 104 and 106 are responsive to a torque error signal 204 generated via the comparison of an estimated torque 206 generated at 108 and a time shifted version of the T_CMD 28 denoted the delayed torque command 202. It will be appreciated, that by noting that the torque producing current I_q is directly proportional to the torque, either of the two analogous quantities may be employed in this approach. Hereafter, the torque and torque current will be treated equivalently.

This process, estimate torque 108 utilizes a measurement representing the torque producing current or I_q, of the motor (also referred to as the “real”, “quadrature”, or “torque” component of the motor current vector) and the motor velocity ω as inputs. Appropriate scaling is applied to facilitate comparison of the measured torque producing current I_q to the expected value determined from the torque command T_CMD 28. An appropriate delay depicted at 114 between the T_CMD 28 and the comparison operation is applied to ensure that the measured I_q is time coherent with the T_CMD 28 to which it is being compared thereby generating a delayed torque command 202. The most recent estimated value of the combined feedforward and feedback motor constant estimate K_eEST is employed used in the scaling process. Since toque is equal to K_e, I_q either the delayed torque command 202 may be divided by K_eEST to create a commanded torque current variable to compare to the computed I_q, conversely, I_q may be multiplied by K_eEST to create a computed torque estimate T_EST 206 and compared to the delayed torque command 202. The latter is depicted in FIG. 11. The torque error signal 204 generated by the comparison is range checked at limiting process 122 and ignored if the torque error signal 204 exceeds a selected limit. Otherwise, the torque error signal 204 is supplied to the resistance conditional integrator 104. Similarly, the torque error signal 204 is supplied to the motor constant K_e conditional integrator 106.

An additional output of the estimate torque process 108 is a signal which represents that the measured value of I_q is valid, or within selected error bounds. The operation of the conditional integrators may be interlocked as a function of the validity condition to ensure that the integrators only operate under selected conditions. For instance, the I_q measurement input to the estimate torque process 108 may be unavailable or of lesser accuracy. The conditional integrators 104 and 106 are employed to generate feedback corrections for resistance R and motor constant K_e responsive to the torque error signal 204. The integration conditions are determined by the accuracy of the torque error signal 204 applied to each integrator. In addition, error integration for resistance estimation occurs in the low velocity/high torque command region of motor operation, while the error integration for motor constant K_e occurs in a high velocity/low torque command region. It will be appreciated that at low velocities, the resistance error signal equation (e.g., equation 23) is more accurate; while at high velocities the K_e error signal equation (e.g., equation 25) is more accurate.

The conditional integrators 104 and 105 themselves also operate as a function of numerous input signals to establish the selected integrating conditions. In an exemplary embodiment, motor velocity ω, motor torque command T_CMD 28, a rate flag 208, and the estimate good flag as discussed earlier are employed to further define the desired integration envelopes. It is noteworthy to appreciate that motor velocity ω is utilized to enhance the accuracy of the error equations being used for the estimation. As described herein above, the feedback compensation equations, exhibit enhanced accuracy in different velocity ranges for the numerous motor parameters. On the other hand, as stated earlier, the resistance estimate in equation (23) approaches infinity at I_q=0. Therefore, low torque commands need to be excluded from the integration component of the estimation for resistance. Similarly, the K_e in equation (25) approaches infinity at ω=0, and thus the motor stall and/or low velocity condition should be excluded from the K_e integration. In addition, it is noteworthy to recognize that the resistance error estimate is more accurate for low velocities and the motor constant estimate is more accurate for low torques.

The estimate good flag provides an interlock on the estimate computation for those operating conditions when the torque estimate from the estimate torque process 108 may not be valid. For example, under certain operating conditions the algorithm employed to ascertain the torque current may experience degradation in accuracy or may not be deterministic. One such condition employed to invalidate the torque estimate is when the motor 12 is operating in quadrant II or IV, that is, when the torque command and velocity ω are in opposite directions. Such conditions occur when there are torque and direction reversals.

In yet another embodiment, the conditional integrators may also be a function of additional conditions and criteria. For example, additional constrains may be employed upon the integrations. In this embodiment, a rate flag us also employed to identify conditions when the spectral content of the torque command is undesirable and thus the integration should be disabled. In this instance, a rate flag 208 is employed by each of the conditional integrators 104 and 106 as an interlock on the feedback estimate computation under transient conditions. The rate flag 208 indicates that the spectral content of the torque command T_CMD 28 is below a selected frequency threshold. An interlock of this nature is desirable to avoid including in the estimate computation contributions to the torque error which are resultant from sudden but short duration torque commands by the operator.

Continuing with FIG. 11, it is noteworthy to appreciate that the integration envelope boundaries may be implemented with a variety of boundary conditions. For example, “hard” boundaries, which are exemplified by the conditional integrator(s) 104 and 106 being either “on” and running or “off” when on either side of the boundary respectively. Conversely, “soft” boundaries, where the integrator gain is gradually reduced when crossing the boundary from the “on” or active side of the “off” or inactive side and gradually increased back to its nominal value when crossing the boundary from the “off” side to the “on” side. A “hard” boundary may be easier to implement but a “soft” boundary may allow the integration window to grow slightly. In an embodiment, a “hard” boundary may be employed to simplify implementation requirements.

Having reviewed the interfaces to, and operation of, the conditional integrator 104 and 106, attention may now be given to some details of operation of the remainder of the feedback parameter estimation as depicted in FIG. 11. It may be noted that the parameters of interest usually vary relatively slowly over time. For example, the temperature dependent variation and the life variation of the parameters may exhibit time constants on the order of minutes, days if not even years. Therefore, the conditional integrators 104 and 106 may be configured as desired to exhibit relatively slow response times, or low gains. Setting the gains too high or the response too fast, for example, may inadvertently cause the conditional integrators 104 and 106 to initiate correction of parameters during high frequency commanded torques as might be experienced under rapid or aggressive steering maneuvers. Because the normal delay between commanded torque T_CMD 28 and actual torque (as supplied from the process estimate torque 108) becomes less predictable in this case, the delayed T_CMD 202 and T_EST 206 may not be time coherent (matched in time). However, by maintaining the conditional integrator gains lower and the response characteristics of the conditional integrator slower, overall response to erroneous torque error signals, if any, are limited and unable to adversely affect the outputs of the conditional integrators 104 and 106, or the motor parameters estimates. Once again, this may be accomplished by disabling the conditional integrators 104 and 106 under selected conditions to ensure that the effect on the parameter estimates will be minimized. The rate flag disclosed in the above mentioned embodiment may be employed to address this requirement in a manner similar to that described earlier.

Another important consideration for the practical implementation employing the conditional integrators 104 and 106 is initialization. It is well understood that because of the nature of an integrating function, controlling the initial conditions is very important. This is the case because any error in the initial conditions may only be elimnated via the gain and at the integrating rate specified. Therefore, in the instant case where the desired response is purposefully maintained slow to accommodate system characteristics, the initial error may take significant time to be completely eradicated.

Like the estimation filters 40, 50, and 60 discussed earlier, initialization of the conditional integrators 104 and 106 presents unique circumstances for consideration. In another embodiment, the conditional integration 104 and 106 may be initialized to a nominal parameter value with each initialization or vehicle starting condition (e.g., with each ignition cycle or power on cycle in an automobile). However, employing this approach once again means that at key on (initial power turn on) the parameter estimate applied to the inverse motor model 112 will now start at the nominal parameter value, and therefore once again not include any information about the parameter estimates “learned” during previous operational cycles. Considering, as state earlier, the conditional integrators 104 and 106 are interlocked at motor stall (e.g., ω=0), this again means that for the first steering maneuver (first commanded torque T_CMD 28) the operator performs, a significant, albeit smaller than the abovementioned embodiment, error may be present.

In yet another embodiment, the output of each conditional integrator 104 and 106 may be saved in a storage location at the end of each ignition/operational cycle. It is noteworthy to recognize that at the end of each ignition cycle, the output conditional integrator 104 and 106 represents the parameter estimate correction needed to overcome the build and life errors and variations. Furthermore, it should be noted and apparent that from one operational cycle to the next, the parameter variation dependent upon build variations will not have changed significantly and therefore, the build variation error correction required is zero. Likewise, the life variation correction from one operational cycle (e.g., each power application to the motor control system 10) to the next is minimal if not negligible. Therefore, in an embodiment, the output of the conditional integrators 104 and 106 may be compared with values from previous operational cycles and saved as a correction only if they differ from the saved values by some selected margin. As such, only significant differences in the response of the conditional integrators 104 and 106 between operational cycles will be saved, thereby reducing processing effort and impact on storage utilization.

To appreciate and understand the accuracy ranges for the estimates, and the operation of the feedback motor parameter estimates, it is helpful to review the theoretical equations for each of their generation. The motor resistance R and motor constant K_e estimates are based upon a simplification of the motor torque and voltage equations.

The equation for calculating the actual motor circuit resistance is derived from the motor torque and voltage equations in the following manner. The motor torque T_m is equal to:

$\begin{array}{cc}{T}_m=\frac{K_e}{R}\frac{V\left(\cos \left(\delta \right)+\left(\frac{{\omega }_{e}L}{R}\right)\sin \left(\delta \right)\right)-K_e{\omega }_e\frac{2}{N_p}}{1+{\left(\frac{{\omega }_{e}L}{R}\right)}^2}& \left(17\right)\end{array}$ where R, K_e, and L are all the actual motor circuit parameters of resistance, motor constant and inductance respectively, ω_c is the electrical motor velocity (i.e. the rotational velocity times the number of poles divided by 2, ω_mN_p/2), N_p is the number of motor poles and δ is the actual motor phase advance angle. V is the applied motor voltage, which is derived using estimate of the parameters.

The concept is as follows: Equation (17) for the motor torque is divided by the actual value of the motor constant K_e which gives an equation for the torque producing component of the total motor current, I_q as shown in equation (18).

$\begin{array}{cc}{I}_q=\frac{V·\left[\cos \left(\delta \right)+\left({\omega }_e·\frac{L}{R}\right)·\sin \left(\delta \right)\right]-2·{\omega }_e·\frac{K_e}{N_p}}{R·\left[1+{\left({\omega }_e·\frac{L}{R}\right)}^2\right]}& \left(18\right)\end{array}$

Equation (18) is then solved for the actual resistance R, with the exception that the L/R terms are still on the right hand side of the equation yielding equation (19).

$\begin{array}{cc}R=\frac{V·\left[\cos \left(\delta \right)+\left({\omega }_e·\frac{L}{R}\right)·\sin \left(\delta \right)\right]-2·{\omega }_e·\frac{K_e}{N_p}}{I_q\left[1+{\left({\omega }_e·\frac{L}{R}\right)}^2\right]}& \left(19\right)\end{array}$

The equation for commanded motor voltage V is derived from equation (17) and using estimated motor parameters yields equation (20), which is subsequently substituted into equation (19), thereby resulting in a new equation for the resistance R, equation (21).

$\begin{array}{cc}V=\frac{\frac{2·{\omega }_e{K}_{\mathrm{eEST}}}{N_p}+T_{\mathrm{cmd}}·\frac{R_{\mathrm{EST}}}{K_{\mathrm{eEST}}}\left[1+{\left({\omega }_e·\frac{L_{\mathrm{EST}}}{R_{\mathrm{EST}}}\right)}^2\right]}{\cos \left(\delta \right)+\left({\omega }_e·\frac{L_{\mathrm{EST}}}{R_{\mathrm{EST}}}\right)·\sin \left(\delta \right)}& \left(20\right)\\ R=\frac{\begin{array}{c}\frac{\frac{2{\omega }_e{K}_{\mathrm{eEST}}}{N_p}+T_{\mathrm{cmd}}\frac{R_{\mathrm{EST}}}{K_{\mathrm{eEST}}}\left[1+{\left({\omega }_e\frac{L_{\mathrm{EST}}}{R_{\mathrm{EST}}}\right)}^2\right]}{\cos \left(\delta \right)+\left({\omega }_e·\frac{L_{\mathrm{EST}}}{R_{\mathrm{EST}}}\right)·\sin \left(\delta \right)}\\ \left[\cos \left(\delta \right)+\left({\omega }_e\frac{L}{R}\right)·\sin \left(\delta \right)\right]-2{\omega }_e\frac{K_e}{N_p}\end{array}}{I_q·\left[1+{\left({\omega }_e·\frac{L}{R}\right)}^2\right]}& \left(21\right)\end{array}$

Hereafter, certain assumption are applied to aid simplification of equation (21). First, it is noteworthy that if the error between the estimated values R_EST and L_EST and the actual values for R and L is small, and further, if the motor velocity ω_m low (such that phase advance angle δ is also small), then, the phase advance terms (terms of the form cos (δ)+ω_eL/R* sin (δ)) of equation (21) may be ignored and canceled. The resultant is equation (22) as shown. Second, assuming that the error between the estimated value K_eEST and K_e is small and again that the motor velocity ω_m is low allows the first term in the numerator to be neglected and cancelled.

$\begin{array}{cc}R=\frac{\begin{array}{c}2·{\omega }_e·\frac{K_{\mathrm{eEST}}-K_e}{N_p}+\\ T_{\mathrm{cmd}}·\frac{R_{\mathrm{EST}}}{K_{\mathrm{eEST}}}·\left[1-{({\omega }_e·\frac{L_{\mathrm{EST}}}{R_{\mathrm{EST}}})}^2\right]\end{array}}{I_q·\left[1+{\left({\omega }_e·\frac{L}{R}\right)}^2\right]}& \left(22\right)\end{array}$

Finally, the numerator and denominator terms of the form 1+(ω_eL_EST/R_EST)² may be cancelled based on the first assumption that the errors between the estimated values R_EST and L_EST and the actual values for R and L is small. This results in a relatively simple equation for the actual value of R as follows:

$\begin{array}{cc}R=T_{\mathrm{CMD}}\frac{R_{\mathrm{EST}}}{K{e}_{\mathrm{EST}}{I}_q}& \left(23\right)\end{array}$

To determine a “measured” value of K_e from the available signals, the following vector equation for motor current can be used. V represents the applied motor voltage, E represents the motor BEMF, or back electro-motive force, I represents the motor current, ω_m is the motor mechanical velocity, and Z represents the motor circuit impedance.

$\begin{array}{cc}\hat{I}=\frac{\hat{V}-\hat{E}}{\hat{Z}}\hat{E}=\hat{V}-\hat{I}\hat{Z}\hat{E}=K_e{\omega }_m{K}_e=\frac{\hat{V}-\hat{I}\hat{Z}}{{\omega }_m}& \left(24\right)\end{array}$

Since the left side of the equation (24) is real, the right side using well known principles can be written in terms of its real part only.

$\begin{array}{cc}{K}_e=\frac{V\cos \left(\delta \right)-I_{q}R}{{\omega }_m}& \left(25\right)\end{array}$

It should be noted that all of the values on the right side of the equation are available either as software parameter or software inputs. By subtracting this “measured” value of K_e from the K_e estimate, a K_e error signal can be developed and used for gradually integrating out the error in the estimate. Also noteworthy is to recognize that as motor velocities approach zero velocity, this equation becomes undefined and should not be used. Moreover, under conditions where the imaginary part of the motor current is nonzero the equation is not as accurate.

It may seem as though equation (23) could be solved directly for R since all the parameters on the right hand side of the equation are readily available. However, it is noteworthy to realize that I_q may realistically not always be available or accurate, especially at start up. Further, the assumptions used to derive the equations initially, were characterized as valid primarily at low velocities, thus dictating that equation (23) is only valid at low velocities. Therefore, the approach disclosed in this embodiment should preferably, by employed under conditions where the resultant of the integration can either be combined with a constant nominal value for the resistance R, or more substantially, as in an exemplary embodiment disclosed later herein, an estimate for R derived from the feedforward compensation as described in previous embodiments.

An alternative approach to computing an equation for K_e estimation may be employed. Employing the same technique utilized above to develop an equation for the estimate for R, an equation to estimate K_e may be developed. Referring once again to equation (18), the equation can be solved for K_e to yield equation (26).

$\begin{array}{cc}{K}_e=\frac{V·\left[\cos \left(\delta \right)+\left({\omega }_e·\frac{L}{R}\right)\sin \left(\delta \right)\right]-I_q·R·\left[1+{\left({\omega }_e·\frac{L}{R}\right)}^2\right]}{2·\frac{{\omega }_e}{N_p}}& \left(26\right)\end{array}$

Again in a similar fashion, utilizing equation (20) for the voltage and then substituting into equation (26), equation (27) for K_e is generated.

$\begin{array}{cc}\mathrm{Ke}=\frac{\frac{2{\omega }_e\frac{K_{\mathrm{eEST}}}{\mathrm{Np}}+T_{\mathrm{cmd}}\frac{R_{\mathrm{EST}}}{K_{\mathrm{eEST}}}\left[1+{\left({\omega }_e\frac{L_{\mathrm{EST}}}{R_{\mathrm{EST}}}\right)}^2\right]}{\cos \left(\delta \right)+\left({\omega }_e\frac{L_{\mathrm{EST}}}{R_{\mathrm{EST}}}\right)\sin \left(\delta \right)}[\cos \left(\delta \right)+\left({\omega }_e\frac{L}{R}\right)\sin \left(\delta \right)]-I_{q}R\left[1+{\left({\omega }_e\frac{L}{R}\right)}^2\right]}{2\frac{{\omega }_e}{\mathrm{Np}}}& \left(27\right)\end{array}$

Once again, applying the assumptions and simplifications employed above to solve for R, a simplified equation for K_e may be developed in terms of known parameters. That is, because the errors in R and L are small, allows the phase advance terms to cancel. Additional simplification of the remaining terms yields equation (28) shown below.

$\begin{array}{cc}{K}_e=K_{\mathrm{eEST}}+\frac{N_p{R}_{\mathrm{EST}}}{2·{\omega }_e}·\left(\frac{T_{\mathrm{cmd}}}{K_{\mathrm{eEST}}}-I_q\right)·\left[1+{\left({\omega }_e\frac{L_{\mathrm{EST}}}{R_{\mathrm{EST}}}\right)}^2\right]& \left(28\right)\end{array}$

Although not as simple as the estimation equation for R (equation 23), the error between K_e and K_eEST is still a function of the different equation T_cmd/K_eEST minus I_q. Two other velocity dependent terms act as a “gain” term for the difference equation. Observation indicates that this “gain” term approaches infinity at zero velocity (e.g., ω_e=0), then the “gain” term reduces to a minimum at motor operation mid-range velocities, and then increases again at high velocities. An example of the “gain” term versus velocity in shown in FIG. 12. Therefore, it may be apparent then that the difference equation of equation (28) provides an indeterminate estimate for K_e at low or zero velocity as state earlier, and yet an improved indication of the K_e estimate error at high velocities where the “gain” term is larger. Therefore the best range to estimate K_e would be at high velocities.

It is easy to see from equation (23) for R that if T_CMD is equal to K_eEST I_q then R will be equal to R_EST. If T_CMD is larger then K_eEST I_q, then R_EST is too small, and vice versa. Therefore, the error signal for the conditional integrators 104 and 106 may readily be computed by subtracting K_eEST I_q from T_CMD (or equivalently T_CMD/K_eEST minus I_q). Integration should then take place only at low motor velocities where δ is small and at values of I_q greater than zero, since at I_q=0 the above equation for R goes to infinity and is not valid.

Returning to equation (25) and the computation of K_e, in this instance, the error between K_e and K_eEST is also a function of the difference equation T_CMD/K_eEST minus I_q. The two other velocity dependent terms provide scaling for the difference equation. It is noteworthy to recognize that these scaling terms approach infinity at zero velocity, then reduce to a minimum for mid-range velocities of motor operation, and then increase again at high velocities. Therefore, the difference equation will then be a better indicator of the K_e estimate error at high velocities where the gain is larger. Therefore, the best range to integrate for K_e would be at high velocities and avoiding the anomaly at low or zero velocity. FIG. 12 depicts a K_e estimator error signal gain as a function of motor velocity.

Therefore, by starting with the explicit equations for the parameters and applying several educated assumptions and constraints, simple equations for estimating the parameters may be derived. The resultant parameter estimates are proportional to the error between the commanded motor torque and the actual or measured motor torque. This approach facilitates employing a simple error integration technique to compute corrections for the motor parameters. Once again, it is noteworthy to appreciate that the integration process should be constrained to the motor operational regions where the simplified equations are valid due to the abovementioned assumptions and constraints.

Yet another embodiment, employs another enhancement to feedback parameters estimation by establishing conditions under which the parameter estimation should be halted and not performed. Such conditions may exist for a variety of reasons particularly those associated with conditions under which the assumptions employed to establish the parameters estimation equations may no longer be valid. One such condition may be dynamic operating conditions for the motor 12, for example, dynamic torque and current as may be induced by more aggressive operator inputs. Under such dynamic conditions, for example, high torque or current or high rate motor commands, the parameter estimation algorithms disclosed above may update existing estimations for motor parameters with estimates which are consequently inaccurate as a result of the dynamic conditions. Therefore, an exemplary embodiment provides a means of selectively enabling the motor parameter estimation as a function of the commanded motor dynamic conditions. Such selective enablement of the estimation process yields a more accurate estimate by avoiding parameter estimation responses to conditions that produce undesirable results.

The inverse motor model depicted at 112 in FIG. 11 employed for motor control is effectively a steady state inverse of the motor equation of operation providing voltage to be applied to the motor 12 as a function of motor velocity and desired output torque. It will be appreciated that utilizing this steady state model, for example, in motor control applications for vehicle steering, produces acceptable results while avoiding undesirable driver feel anomalies associated with the dynamic characteristics of the system 10. This has been the case because the motor time constant and dynamic responses are negligible when compared to the mechanical time constant of the vehicle steering mechanisms. In other words and more particularly, the lag and dynamics between the commanded current in the steady-state inverse motor model and the torque produced by the motor are not felt by the driver and are thus, transparent to the driver.

In an exemplary embodiment and referring once again to FIG. 11, to facilitate motor parameter estimation a comparison and error computation between commanded torque and motor torque is employed, thereby, generating a torque error. Even when ideal motor parameters are considered, such an error will persist, particularly under dynamic conditions. Moreover, because the torque error is utilized to correct and compensate the motor parameters as disclosed herein, such a torque error will effectively “correct” the motor parameters from more accurate or ideal values to less accurate, non-ideal values under certain conditions. This “correction” away from more accurate values is characteristic of the parameter estimation process, which is preferably avoided. Therefore, it will be evident that one way to prevent “improper” correction is to disable the parameter estimation of the conditional integrators 104 and 106 during selected dynamic conditions. The rate flag 208 discussed in earlier embodiments is an implementation, which addresses this disabling of the conditional integrators 104 and 106 under selected conditions. It will be appreciated that while the disclosed embodiment pertains an enhancement for parameter estimation employing a determination of a torque error resultant from a difference between commanded and actual torque, analogous comparisons may be employed utilizing current. In fact, under certain conditions it may be advantageous in implementation to employ current rather than torque as the subject compared parameter.

An exemplary embodiment presents method and system for preventing undesirable correction of motor parameters estimation under dynamic operating conditions. In the system 10 motor 12 operates under true steady state conditions (no dynamics) if all orders of the motor torque and motor velocity derivatives are zero. It will be appreciated that over a short duration of time and neglecting highly dynamic conditions, the motor velocity ω_m exhibits little change due to physical constraints and properties (e.g., mass, inertia, and the like). Hence, it may be assumed that all orders of derivatives of motor velocity are zero during one sample period. Moreover, the velocity of the motor remains relatively constant under operating conditions where the torque is not rapidly changing as well. Therefore, the characteristics of the motor torque often provide a good indication of the characteristics of the velocity of the motor. However, significant dynamics may exist when the commanded torque exhibits rapid changes. In addition, the greater the rate of changes of the commanded torque, the greater the resulting motor dynamics. The first derivative of the motor torque may be approximated by the change of commanded torque over a fixed period of time, for example, one sample periods, or a specified motor torque change divided by the associated duration of time for that torque change. It will be appreciated that there are numerous methodologies for ascertaining the rate of change of motor torque or motor current. The two given here are exemplary and illustrative and are not necessarily inclusive of other potential means of determining a derivative. It will also be appreciated that, in practice, it is often difficult to obtain a true measurement or estimate of higher order derivatives utilizing the abovementioned or similar methods. Because of noise amplification difficulties and mathematical anomalies, such methodologies are limited to certain characteristics of data and applications. Ideally, it would be preferred to include all the higher order derivatives of the motor current to facilitate the determination and characteristics of the motor dynamics, but nonetheless, the rate of the change of commanded torque and therefore the current presents a useful estimate of the motor dynamics.

Referring once again to FIG. 11, it will be appreciated that the rate of change of commanded current may be calculated as the difference between current commands over a period of time. For instance, the difference between current commands over two consecutive or a selected number of controller cycles. If the rate of change of current command exceeds a selected threshold value, the parameter estimation may be disabled (no integration by the conditional integrators 104 and 106 (FIG. 11) during that time period). If this rate is less than the threshold, parameters estimation is allowed to integrate the error. In an exemplary embodiment, a threshold value of 2 Ampreses (A) over a 2 millisecond duration was employed and found to provide more efficient conditional integrators.

It should be noted that the maximum gains of the conditional integrators 104 and 106 may therefore be determined by the maximum acceptable wandering fluctuations of the estimated parameters R and K_e. It is further noteworthy to appreciate that by restricting the parameter estimation to operate under the threshold as disclosed herein, to a finite extent, an increase in the gain of the conditional integrators 104 and 106 may be achieved thereby improving the response characteristics of the conditional integrators 104 and 106 for the parameter estimation.

Combination Feedback and Feedforward Parameters Estimation

Another exemplary embodiment contemplates an enhancement of the processes of the feedback methodology 130 for parameter estimation embodiments discussed earlier combined with the processes of the feedforward methodology 120 for parameters estimation also discussed earlier. Such a combination of feedback methodology 130 combined with feedforward methodology 120 for parameter estimation captures the advantages of both methodologies while minimizing the disadvantages and limitations of either methodology when implemented alone. FIG. 11 depicts a diagram outlining the process employed. It is noted that feedback methodologies are generally closed loop and provide accurate control of a parameter or system at the expense of mandating an accurate sensing method or apparatus and poor transient response or stability. Moreover, feedback systems often require additional processing time to compute the desired corrections. Conversely, feedforward methodologies are generally open loop and do not require a sensor measurement of the parameter of interest. Additionally, a feedforward methodology exhibits excellent transient response characteristics usually at the expense of accuracy of response. Therefore, a combination of the feedback methodology with the feedforward methodology provides the increased accuracy attributable to feedback with the dynamic response attributable to feedforward.

A description of the processes employed to facilitate the feedback methodology 130 and the feedforward methodology 120 has been provided earlier and will not be repeated here to avoid redundancy. Therefore, it should be understood that a reference to feedback includes the full description and disclosure of the abovementioned feedback parameter estimation methodology. Furthermore, reference to feedforward includes the full description and disclosure of the abovementioned temperature estimation and feedforward parameter estimation methodology. Further descriptions provided herein are intended to expound the capabilities either the feedback or feedforward parameter estimation or the combination thereof.

Having reviewed the interfaces to, and operation of, the conditional integrators 104 and 106, attention may now be given to some details of operation of the remainder of the combined feedforward and feedback parameter estimation as depicted in FIG. 11. Turing now to the feedback methodology 130, it may be noted that the parameters of interest usually vary relatively slowly over time. For example, the life variation of the parameters may exhibit time constants on the order of minutes, days if not ever years. Moreover, the build variations tend to be more random in nature from one unit to another. Therefore, the conditional integrators 104 and 106 may be configured as desired to exhibit relatively slow response times, or low gains. Setting the gains too high or the response too fast, for example, may inadvertently cause the conditional integrators 104 and 106 to initiate correction of parameters during higher frequency commanded torques as might be experienced under rapid or aggressive steering maneuvers. Because the normal delay between commanded torque T_CMD 28 and actual torque (as supplied from the process estimate torque 108) becomes less predictable in this case, the delayed T_CMD 202 and T_EST may not be time coherent (matched in time) possibly resulting in the generation of erroneous error signal, albeit briefly. However, by maintaining the conditional integrator gains lower and the response slower any erroneous signals generated are limited and unable to adversely affect the outputs of the conditional integrators 104 and 106, or the motor parameter estimates. Once again, this may be accomplished by disabling the conditional integrators 104 and 106 under selected conditions to ensure that the effect on the parameter estimates will be minimized. The rate flag disclosed in the above mentioned embodiment may be employed to address this requirement in a manner similar to that described earlier.

Returning once again FIG. 11, the feedforward methodology 130 comprising the feedforward parameter estimation 110 as well as the component temperatures estimation process 100 has been disclosed earlier, and together, computes a temperature dependent feedforward parameter estimate for both the resistance R and the motor constant K_e. The feedback methodology 130 compute long term slowly varying corrections to the parameter estimates to address build and life variations. In an embodiment, the output of the conditional integrators 104 and 106 respectively, is combined at summers 116 and 118 respectively with the output of the feedforward parameter estimation for resistance estimate 210 and motor constant estimate 212 described yielding combined parameter estimates 214 and 216 for resistance and motor constant respectively. The combined parameter estimates 214 and 216 update continuously with temperature (feedforward), and as needed to correct for build or life variations (feedback). The result of these combinations is the final motor parameter (R, K_e) estimate, which is applied to the inverse motor model 112 and used to calculate the appropriate voltage and phase commands for the motor to achieve the desired torque.

In an embodiment of the combined feedback methodology 130 and feedforward methodology 120, once again initialization is paramount. The combined approach yields significant advantages not readily achieved with either the feedback methodology 130 or feedforward methodology 120 alone. Turning to the initialization of the conditional integrators, in an exemplary embodiments of the combined processes, the conditional integrators 104 and 106 could simply be initialized to a zero output with each vehicle starting condition as disclosed earlier. However, employing this approach means that at key on (initial power turn on) the combined parameter estimate applied to the inverse motor model 112 will equal the feedforward estimate only from the feedforward parameter estimate process 110. While this approach may be adequate for some applications, once again, it does not take advantage of the information “learned” about the build and life variations of the parameters.

In yet another embodiment, similar to that disclosed earlier, the output of each conditional integrator 104 and 106 may be saved in storage location at the end of each ignition/operational cycle. It is noteworthy to recognize that at the end of each ignition cycle, the output of each conditional integrator 104 and 106 represents the parameter estimate correction needed to overcome the build, life, and feedforward correction error variations. Furthermore, it should be noted and apparent that from one operational cycle to the next, the parameter variation dependent upon build variations will not have changed significantly and therefore, the build variation error correction required is zero. Likewise, the life variation correction from one operational cycle (e.g., each power application to the motor control system 10) to the next is minimal if not negligible. Therefore, once again, the contribution to the output of the conditional integrators 104 and 106 due to these variations may be assumed to be constant. As such, the only significant difference in the response of the conditional integrators 104 and 106 between operational cycles may be attributed to errors in the feedforward estimation as a function of temperature.

Fortunately, these types of errors have been previously addressed in an embodiment disclosed, which minimizes their impact. Therefore, the feedforward estimation errors most likely, will be smaller than the build and life variations carried forward. Moreover, employing this approach, the overall initialization errors will still be much smaller that if the conditional integrators 104 and 106 were initialized to a zero as the assumed initial output. Employing this technique will reduce the errors due to parameter errors at initialization with the application of power, and will reduce the amount of time for the integrators to approach their final value.

Once again, it is significant to recall and recognize that the feedforward estimation contribution to the motor parameter estimates primarily addresses temperature related changes, while the feedback contribution to the motor parameter estimation primarily addresses long-term variations. Therefore, once the outputs of the conditional integrators 104 and 106 approach final values they should not change significantly until the end of the ignition cycle.

Moreover, looking to the conditions for initialization of the conditional integrator 106 associated with the estimation of K_e, it should be recognized that K_e feedback compensation errors only under certain operational conditions, for example, in disclosed embodiment, high motor/hand wheel velocities. Significantly, some operating conditions are less probable and occur less frequently, for example in an instance employing a vehicle, some drivers may very rarely derive in a manner in which they use high hand wheel velocities. Thus, from a practical position, it would be fruitless to discard the information learned and accumulated about the actual value of K_e from each operational cycle to the next. Thus, to avoid errors in the K_e estimate, which may result in substantial changes in torque output and damping, and possibly stability degradation, the last output values of the conditional integrator (in this instance 106) may be stored, and saved for later use at the end of each operational cycle. More appropriately, at the end of an operational cycle, the last value of the parameter estimate may be compared with a stored value from previous operations and saved only if there has been a significant change in that parameter estimate since the last cycle.

However, the shortcomings described above, due, mainly to the large periods of time where the integrators 104 and 106 are set inactive would remain therefore combining the feedback estimation with the feedforward estimation yields more accurate results. Another advantage of the combining approach described herein is that the accuracy requirements of the feedforward methodology 120 could potentially be relaxed slightly due to the presence of the feedback process. Thereby, allowing the feedback contribution to the parameter estimates to make up the difference without impacting overall system performance. For example, lower cost temperature sensors may be employed or less complex initialization utilized for the estimation process 100 than may be desired with feedforward parameter estimation alone. It will be further appreciated the while an embodiment disclosing the operation of a pair of conditional integrators responsive to a torque error signal had been described, it will be understood as being exemplary and illustrative only. Other implementations of the same concepts are conceivable. For example, the integrators as described are effectively error accumulators or counters, which accumulate errors at a predetermined rate. Other implementations employing accumulators, counters or other summation methods may readily be employed.

The disclosed method may be embodiment in the form of computer-implemented process and apparatuses for practicing those processes. The method can also be embodied in the form of computer program code containing instructions embodied in tangible media, such as floppy diskettes, CD-ROMs, hard drives, or any other computer-readable storage medium, wherein, when the computer program code is loaded into and executed by a computer, the computer becomes an apparatus capable of executing the method. The present method can also be embodied in the form of computer program code, for example, whether stored in a storage medium, loaded into and/or executed by a computer, or as data signal transmitted whether a modulated carrier wave or not, over some transmission medium, such as over electrical wiring or cabling, through fiber optics, or via electromagnetic radiation, wherein, when the computer program code is loaded into and executed by a computer, the computer becomes an apparatus capable of executing the method. When implemented on a general-purpose microprocessor, the computer program code segments configure the microprocessor to create specific logic circuits.

While the invention has been described with reference to an exemplary embodiment, it will be understood by those skilled in the art that various changes may be made and equivalents may be substituted for elements thereof without departing from the scope of the invention. In addition, many modifications may be made to adapt a particular situation or material to the teachings of the invention without departing from the essential scope thereof. Therefore, it is intended that the invention not be limited to the particular embodiment disclosed as the best mode contemplated for carrying out this invention, but that the invention will include all embodiments falling within the scope of the appended claims.

Claims

1. A method for estimating at least one parameter associated with an electric machine, the electric machine operably coupled to a controller, the controller controlling operation of the electric machine, the method comprising: measuring a temperature of the controller to obtain a measured temperature, utilizing a temperature sensor;estimating a temperature of the electric machine to obtain a first estimated temperature, utilizing a first temperature estimation filter associated with the electric machine, based on the measured temperature; andestimating at least one parameter associated with the electric machine based on the estimated temperature of the electric machine.

2. The method of claim 1, wherein the first temperature estimation filter associated with the electric machine comprises a magnet temperature estimation filter, and the step of estimating the temperature of the electric machine comprises: estimating a temperature of a magnet in the electric machine, utilizing the magnet temperature estimation filter, based on the measured temperature of the controller.

3. The method of claim 1, wherein the first temperature estimation filter associated with the electric machine comprises a copper winding temperature estimation filter, and the step of estimating the temperature of the electric machine comprises: estimating a temperature of a copper winding in the electric machine, utilizing the copper winding temperature estimation filter, based on the measured temperature of the controller.

4. The method of claim 1, wherein the at least one parameter associated with the electric machine comprises at least one of a motor winding resistance and a motor voltage constant.

5. The method of claim 1, further comprising estimating a temperature of a switching device in the controller to obtain a second estimated temperature utilizing a second temperature estimation filter associated with the controller, based on the measured temperature of the controller; andestimating at least one parameter associated with the controller, utilizing the second temperature estimation filter, based on the second estimated temperature of the controller.

6. The method of claim 5, wherein the second temperature estimation filter comprises a silicon temperature estimation filter.

7. The method of claim 5, wherein the at least one parameter associated with the controller is a FET resistance.

8. A system for estimating at least one parameter associated with an electric machine, comprising: a controller configured to be operably coupled to the electric machine;a temperature sensor configured to generate a signal indicative of a temperature of the controller; andthe controller configured to determine a measured temperature associated with the controller based on the signal, the controller further configured to estimate a temperature of the electric machine to obtain a first estimated temperature, utilizing a first temperature estimation filter associated with the electric machine, based on the measured temperature, the controller further configured to estimate at least one parameter associated with the electric machine based on the estimated temperature of the clectric machine.

9. The system of claim 8, wherein the first temperature estimation filter associated with the electric machine comprises a magnet temperature estimation filter, the controller further configured to estimate the temperature of the electric machine by estimating a temperature of a magnet in the electric machine, utilizing the magnet temperature estimation filter, based on the measured temperature of the controller.

10. The system of claim 8, wherein the first temperature estimation filter associated with the electric machine comprises a copper winding temperature estimation filter, the controller further configured to estimate the temperature of the electric machine by estimating a temperature of a copper winding in the electric machine, utilizing the copper winding temperature estimation filter, based on the measured temperature of the controller.

11. The method of claim 8, wherein the at least one parameter associated with the electric machine comprises at least one of a motor winding resistance and a motor voltage constant.

12. The system of claim 8, wherein the controller is further configured to estimate a temperature of a switching device in the controller to obtain a second estimated temperature utilizing a second temperature estimation filter associated with the controller, based on the measured temperature of the controller, the controller further configured to estimate at least one parameter associated with the controller, utilizing the second temperature estimation filter, based on the second estimated temperature of the controller.

13. The system of claim 12, wherein the second temperature estimation filter comprises a silicon temperature estimation filter.

14. The system of claim 12, wherein the at least one parameter associated with the controller is a FET resistance.