Method for Operating a Steering System, Control Unit for a Steering System and Steering System

Abstract

The disclosure relates to a method for operating a steering system of a motor vehicle. A voltage reserve is determined as a function of a compensation trajectory for a second actuating voltage and as a function of a modulation limit. A first actuating voltage with a fundamental frequency is determined as a function of the voltage reserve. A compensation voltage with a sixth-order harmonic with respect to the fundamental frequency of the first actuating voltage is determined. The second actuating voltage is determined for an inverter as a function of the first actuating voltage and as a function of the compensation voltage.

Claims

1. A method for operating a steering system of a motor vehicle, the method comprising: determining a voltage reserve based on a compensation trajectory for a second actuating voltage for an inverter and based on a modulation limit; determining a first actuating voltage having a fundamental oscillation based on the voltage reserve; determining a compensation voltage having a sixth-order harmonic with respect to the fundamental oscillation of the first actuating voltage; and determining the second actuating voltage based on the first actuating voltage and based on the compensation voltage.

2. The method as claimed in claim 1, wherein the modulation limit extends along a circle in a voltage plane.

3. The method as claimed in claim 1, wherein the modulation limit extends along a hexagon in a voltage plane.

4. The method as claimed in claim 1, the determining the compensation voltage further comprising: determining the compensation voltage using a harmonic machine model.

5. The method as claimed in claim 1, the determining the compensation voltage further comprising: determining the compensation voltage based on an actual rotor position of a permanently excited synchronous machine and based on the first actuating voltage.

6. The method as claimed in claim 1, the determining the second actuating voltage further comprising: determining the second actuating voltage by adding the first actuating voltage and the compensation voltage {right arrow over (u)}.sub.dq,comp.

7. The method as claimed in claim 1, the determining the voltage reserve further comprising: determining the voltage reserve by subtracting a magnitude of the modulation limit from a magnitude of the compensation trajectory. wherein the voltage reserve is an angle-dependent voltage reserve and the compensation trajectory is an angle-dependent compensation trajectory.

8. A control device for a steering system of a motor vehicle, the control device comprising: at least one memory configured to store computer program code; and at least one processor configured to execute the computer program code to: determine a voltage reserve based on a compensation trajectory for a second actuating voltage for an inverter and based on a modulation limit; determine a first actuating voltage {right arrow over (u)}.sub.dq having a fundamental oscillation based on the voltage reserve; determine a compensation voltage {right arrow over (u)}.sub.dq,comp having a sixth-order harmonic with respect to the fundamental oscillation of the first actuating voltage; and determine the a second actuating voltage {right arrow over (u)}.sub.32 based on the first actuating voltage {right arrow over (u)}.sub.dq and based on the compensation voltage {right arrow over (u)}.sub.dq,comp.

9. A steering system of a motor vehicle, the steering system comprising: an inverter; a permanently excited synchronous machine; and a control device having (i) at least one memory configured to store computer program code and (ii) at least one processor configured to execute the computer program code to: determine a voltage reserve based on a compensation trajectory for a second actuating voltage for an inverter and based on a modulation limit; determine a first actuating voltage having a fundamental oscillation based on the voltage reserve; determine a compensation voltage having a sixth-order harmonic with respect to the fundamental oscillation of the first actuating voltage; and determine the second actuating voltage based on the first actuating voltage and based on the compensation voltage.

Description

[0016] Further features and advantages are to be found in the following description of exemplary embodiments. In the figures:

[0017] FIG. 1 shows a steering system for a motor vehicle in a schematic form;

[0018] FIG. 2a shows a schematic block diagram;

[0019] FIG. 2b shows a schematically illustrated control device;

[0020] FIGS. 3a, 4a each show a schematic voltage diagram in a dq system; and

[0021] FIGS. 3b, 4b each show a schematic voltage diagram in an αβ system.

[0022] FIG. 1 shows, in schematic form, a steering system 2 with power-assisted steering 4. The steering system 2 can, furthermore, as shown, also comprise a superimposed steering system 6. The steering system 2 comprises a steering gear 8 that is, for example, designed as a rack-and-pinion steering system. A rack-and-pinion steering system will predominantly be assumed in this description, in which the steering gear 24 comprises a sprocket 10 and a steering rack 12. The steering gear 8 is connected on each side of the vehicle via the sprocket 10 and the steering rack 12 to a steering linkage 14, each of which acts together with a wheel 16. Fundamentally, the steering system 2 represents one of a large number of possible forms of embodiment of devices suitable for carrying out the method according to the invention. Other forms of embodiment can thus be constructed by other steering gears or by a different arrangement of drives. In particular, the steering system 2 is a steer-by-wire steering system in one form of embodiment. Further sensors can, furthermore, be arranged in the steering system, whose arrangement and implementation will not be considered at this point.

[0023] A steering means 20 of the steering system, for example a steering wheel, is arranged at a torsion bar 18 of the steering system 2. The steering means angle applied by the vehicle driver can, in a normal operation of the steering system 2, be enlarged or reduced as far as the steering gear 8 by means of the superimposed steering system 6. This steering angle difference, which is introduced into the steering gear 8 by the superimposed steering system 6, is also referred to as the additional steering angle. Instead of a torsion bar 18, a steering column can of course also be arranged between the steering means 20 and the superimposed steering system 6. In this form of embodiment, the torsion bar 18 is arranged between the superimposed steering system 6 and the power-assisted steering 4.

[0024] The power assisted steering 4 of the steering system 2 comprises a permanently excited synchronous machine 22, an inverter 23 assigned to the drive unit 22, and a gear 24. The inverter 23 generates a modulated actuating voltage {right arrow over (u)}.sub.uvw for operating the permanently excited synchronous machine 22. A control device 26 of the steering system is assigned to the permanently excited synchronous machine 22. The permanently excited synchronous machine 22 acts on the steering rack 12 via the gear 24.

[0025] A torsion bar torque 34 ascertained by a sensor 32 of the steering system 2 is supplied to a block 102 of the control device 26. The steering system 2 comprises a position sensor 38 that ascertains an actual steering rack position 40 which is supplied to the block 102 of the control device 26. The motor vehicle furthermore comprises a speed sensor 42 that ascertains an actual vehicle speed 44 and supplies this to the control device 26. The actual vehicle speed 44 can, alternatively, also be supplied to the control device 26 by a further control device.

[0026] Depending on the supplied torsion bar torque 34, the supplied actual steering rack position 40 and the actual speed 44 of the motor vehicle, the control device 26 ascertains an auxiliary torque Mref that represents a setpoint value for an auxiliary torque to be introduced into the steering system 2 by means of the permanently excited synchronous machine 22, and is, for example, correspondingly converted as an actuating variable, supplied to the permanently excited synchronous machine 22 in the form of the modulated actuating voltage {right arrow over (u)}.sub.uvw.

[0027] A sensor 46 of the steering system 2 ascertains an actual stator current {right arrow over (i)}.sub.dq of the permanently excited synchronous machine 22. The actual stator current {right arrow over (i)}.sub.dq is, for example, a vectorial variable, and comprises the components id and iq in the iq system. A sensor 48 of the steering system 2 ascertains an actual rotor position ϑ of the permanently excited synchronous machine 22. A block 104 ascertains a modulation limit U.sub.mod. A block 106 transforms a compensation trajectory of a supplied compensation voltage {right arrow over (u)}.sub.dq,comp into a compensation trajectory {right arrow over (u)}.sub.αβ,comp. fixed with respect to the stator. A trajectory such as one of the compensation trajectories referred to above defines a path curve in a respective coordinate system along which the compensation voltage passes over time. A trajectory such as, for example, the compensation trajectory u.sub.αβ,comp, is consequently passed through by means of a vectorial variable such as, for example, a compensation voltage {right arrow over (u)}.sub.αβ,comp.

[0028] A block 108 ascertains a voltage reserve U.sub.res depending on the modulation limit U.sub.mod and depending on the compensation trajectory u.sub.αβ,comp. A block 110 ascertains the compensation voltage {right arrow over (u)}.sub.dq,comp depending on a first actuating voltage {right arrow over (u)}.sub.dq and depending on the actual rotor position ϑ. The block 110 comprises, for example, a harmonic machine model, and can be identified as such. The compensation voltage {right arrow over (u)}.sub.dq,comp emerging from the machine model is defined in the dq system in accordance with equations (1) and (2).

u.sub.d,comp=U.sub.d,6 sin(6θ.sub.el+φ.sub.d,6)   (1)

u.sub.q,comp=U.sub.q,6 sin(6θ.sub.el+φ.sub.q,6)   (2)

[0029] u.sub.d,comp is an angle-dependent compensation voltage in the d-direction. U.sub.d,6 is an amplitude of the compensation voltage {right arrow over (u)}.sub.dq,comp. Θ.sub.e1 is the electrical rotor position. Φd,6 is the phase position of the compensation voltage u.sub.d,comp. Similar considerations apply to u.sub.q,comp, although in the q-direction.

[0030] A block 112 ascertains a setpoint stator current {right arrow over (i)}.sub.dq,ref with components i.sub.d,ref and i.sub.q,ref depending on the predetermined auxiliary torque M.sub.ref, depending on the voltage reserve U.sub.res and depending on the actual rotor position ϑ. At an addition point, the control error d is ascertained depending on the setpoint stator current {right arrow over (i)}.sub.dq,ref and depending on the actual stator current {right arrow over (i)}.sub.dq. A block 116 represents a controller that ascertains the first actuating voltage {right arrow over (u)}.sub.dq depending on the control error d. At an addition point 118, a second actuating voltage {right arrow over (u)}.sub.23 is ascertained depending on the first actuating voltage {right arrow over (u)}.sub.dq and depending on the compensation voltage {right arrow over (u)}.sub.dq,comp. The inverter 23 modulates the adjustable voltages in the light of the modulated actuating voltage u.sub.uvw in such a way that the stator windings of the permanently excited synchronous machine 22 are adjusted for an effective voltage that corresponds to the second actuating voltage {right arrow over (u)}.sub.23. The first actuating voltage {right arrow over (u)}.sub.dq is calculated by the controller 116. The second actuating voltage {right arrow over (u)}.sub.23 is supplied to the inverter 32, so that the inverter 23 sets this actuating voltage {right arrow over (u)}.sub.23 at the permanently excited synchronous machine 22 by modulation. The control device 26 consequently provides the second voltage {right arrow over (u)}.sub.23 and passes it to the inverter 23, which drives the permanently excited synchronous machine 22 making use of the second actuating voltage.

[0031] A voltage U.sub.eff that is available for the development of torque is ascertained in accordance with equation (3), wherein U.sub.mod is the modulation limit, where Rs is the stator resistance, where Imax is the maximum current magnitude at a stator winding, and Ures is the voltage reserve.

U.sub.eff=U.sub.mod−R.sub.sI.sub.max−U.sub.res   (3)

[0032] The calculation of the setpoint stator current {right arrow over (i)}.sub.dq,ref is performed in accordance with equations (4) to (7), wherein Zp is a number of pole pairs, ψ.sub.pm,d is a permanent flux linkage in the d direction, L.sub.d, L.sub.q are respective inductances in the d and q directions, ω is an electrical angular velocity, and A is a Lagrange multiplier.

[00001]$\begin{array}{cc}f\left(i_{d,\mathrm{ref}},i_{q,\mathrm{ref}}\right)=-\frac{3}{2}{Z}_p\left({\psi }_{pm,d}{i}_{q,\mathrm{ref}}+\left(L_d-L_q\right)i_{d,\mathrm{ref}}{i}_{q,\mathrm{ref}}\right)& \left(4\right)\\ {\psi }_0=\frac{U_{\mathrm{eff}}}{\omega }=\sqrt{{\left({\psi }_{\mathrm{pm},d}+L_d{i}_{d,\mathrm{ref}}\right)}^2+L_q^2{i}_{q,\mathrm{ref}}^2}& \left(5\right)\\ c\left(i_{d,\mathrm{ref}},i_{q,\mathrm{ref}}\right)=\frac{U_{\mathrm{eff}}^2}{{\omega }^2}-{\left({\psi }_{\mathrm{pm},d}+L_d{i}_{d,\mathrm{ref}}\right)}^2-L_q^2{i}_{q,\mathrm{ref}}^2& \left(6\right)\\ L=-\frac{3}{2}{Z}_p({\psi }_{\mathrm{pm},d}{i}_{q,\mathrm{ref}}+\left(L_d-L_q\right)i_{d,\mathrm{ref}}{i}_{q,\mathrm{ref}}+\lambda \left(\frac{U_{\mathrm{eff}}^2}{{\omega }^2}-{\left({\psi }_{\mathrm{pm},d}+L_d{i}_{d,\mathrm{ref}}\right)}^2-L_q^2{i}_{q,\mathrm{ref}}^2\right)& \left(7\right)\end{array}$

[0033] The setpoint stator current {right arrow over (i)}.sub.dq,ref is calculated with the aid of the torque equation (4) and of the available voltage U.sub.eff. The voltage limit is described with the aid of the linked flux ψ.sub.0 by equation (5). An optimization problem results from this, with a torque that is to be maximized and the voltage limit as a secondary condition according to equation (6). With the aid of the negative torque equation and the secondary condition, the Lagrange function (7) that is to be minimized can be developed, from which the setpoint stator current {right arrow over (i)}.sub.dq,ref that is optimum for operation with the components i.sub.d,ref and i.sub.q,ref according to a respective d and q direction is calculated.

[0034] By means of the reference value calculation according to the setpoint stator current {right arrow over (i)}.sub.dq,ref, the fundamental oscillation amplitude udq of the second actuating voltage {right arrow over (u)}.sub.23 is limited in such a way that the addition of the compensation voltage {right arrow over (u)}.sub.dq,comp is always ensured. The compensation voltage {right arrow over (u)}.sub.dq,comp is transformed for this purpose according to equation (8) into the αβ system fixed with respect to the stator according to the compensation voltage {right arrow over (u)}.sub.αβ,comp.

{right arrow over (u)}.sub.αβ,comp={right arrow over (u)}.sub.dq,comp.sup.e.sup.jθ.sup.el   (8)

[0035] The compensation voltage {right arrow over (u)}.sub.dq,comp that is to be added is characterized by its d and q components. Depending on the amplitude and phase of the respective components, corresponding compensation trajectories u.sub.dq,comp result. In the general case, the compensation trajectory is described by an ellipse with a variable extent and orientation in the voltage plane. In the extreme case, the ellipse is reduced to a circle or to a straight line.

[0036] Through a manipulation in the calculation of the setpoint stator current {right arrow over (i)}.sub.dq,ref (MMPA/MMPV strategy) it is ensured that a suitable voltage reserve U.sub.res is maintained, which allows the required compensation trajectory u.sub.dq,comp to be added.

[0037] FIG. 2a shows a schematic block diagram. According to a block 202, the voltage reserve U.sub.res is ascertained depending on the compensation trajectory u.sub.αβ,comp for the second actuating voltage {right arrow over (u)}.sub.23 and depending on the modulation limit U.sub.mod. A block 204 ascertains the first actuating voltage {right arrow over (u)}.sub.dq with a fundamental oscillation depending on the voltage reserve U.sub.res. According to a block 206, the field-oriented compensation voltage {right arrow over (u)}.sub.dq,comp is ascertained with a sixth-order harmonic with respect to the fundamental oscillation of the first actuating voltage {right arrow over (u)}.sub.dq. According to a block 208, the second actuating voltage {right arrow over (u)}.sub.23 for the inverter is ascertained depending on the first actuating voltage {right arrow over (u)}.sub.dq and depending on the compensation voltage {right arrow over (u)}.sub.dq,comp.

[0038] FIG. 2b shows the schematically illustrated control device 26. The control device 26 comprises a processor P that is connected via a data cable to a storage element Mem. The processor P can also be referred to as a digital computing device on which the method described here can be carried out. The memory element Mem can also be referred to as a storage medium. A computer program that can be carried out on the processor P is stored as computer program code on the memory element Mem.

[0039] FIG. 3a is drawn in the field-oriented dq coordinate system. According to FIGS. 3a and 3b the inner circle of the vector plane is specified with a maximum diameter as the modulation limit U.sub.mod, which can also be referred to as the angle-independent voltage limit. This modulation limit U.sub.mod is defined by equation (9), which is achieved through the application of the vector modulation in the linear modulation range. U.sub.dc identifies the battery voltage or the intermediate circuit voltage. The modulation limit U.sub.mod in FIG. 3b (stator-oriented coordinate system) is the largest inner circle that can be drawn inside the hexagon.

[00002]$\begin{array}{cc}{U}_{\mathrm{mod}}=\frac{U_{\mathrm{dc}}}{\sqrt{3}}& \left(9\right)\end{array}$

[0040] The modulation voltage that can be set is reduced by the ohmic voltage drop at the stator windings. The compensation is, finally, ensured through the voltage reserve U.sub.res that is to be maintained.

[0041] The overlaying of a fundamental oscillation component and a compensation component in the form of the compensation voltage {right arrow over (u)}.sub.αβ,comp leads to the angle-dependent output trajectory u.sub.αβ for the second actuating voltage {right arrow over (u)}.sub.23, wherein the actuating voltage {right arrow over (u)}.sub.αβ that is fixed with respect to the stator extends along the angle-dependent output trajectory u.sub.αβ. The actuating voltage {right arrow over (u)}.sub.αβ that is fixed with respect to the stator corresponds in a similar manner to equation (8) to the second field-oriented actuating voltage {right arrow over (u)}.sub.23.

[0042] For reasons of symmetry it is sufficient in what follows to consider the segment of the vector plane extending from ϑ=0°-60° in FIG. 3b, where ϑ identifies the electrical angle of the actuating voltage {right arrow over (u)}.sub.αβ that is fixed with respect to the stator. In this region, the difference between the compensation trajectory u.sub.αβ and the modulation limit U.sub.mod is calculated in advance in accordance with equation (10) for a defined number of angle values. The electrical angle ϑ of the actuating voltage {right arrow over (u)}.sub.αβ that is fixed with respect to the stator differs from the electrical rotor position θ.sub.e1 by an offset.

u.sub.res(ϑ)=|U.sub.αβ(ϑ)|−|U.sub.mod|  (10)

[0043] The necessary voltage reserve U.sub.res that leads to a limitation of the amplitude of the fundamental oscillation finally emerges from the maximum voltage difference max(u.sub.res(ϑ)). The result of the limitation of the amplitude of the fundamental oscillation is that the output trajectory u.sub.αβ is always located inside the modulation limit U.sub.mod. With this, a requested output trajectory u.sub.αβ,an that is located outside the hexagon H is scaled into the settable voltage range, so that only the outer points of the output trajectory u.sub.αβ are located at the modulation limit U.sub.mod. The region inside the hexagon H corresponds to a region that can be set by the inverter 23.

[0044] FIGS. 4a and 4b show a further example in which the actuation range of the inverter 23 is fully utilized, and the torque yield thereby increased. By modulating the inverter 23 in the non-linear modulation range, the full, hexagonal voltage area can be set. This over-modulation range, as it is known, in the corners of the vector plane can be employed for the compensation of the sixth electrical order in the torque. The requested elliptical output trajectory u.sub.αβ,an can then be set in accordance with FIG. 4a beyond the linear actuation range. The modulation limit U.sub.mod is accordingly defined by an angle-dependent function according to equation (11), which extends along the hexagon.

[00003]$\begin{array}{cc}{U}_{\mathrm{mod}}\left({\vartheta }^{\prime }\right)=\frac{U_{\mathrm{dc}}}{\sqrt{3}\left(\sin \left(\frac{\pi }{3}-{\vartheta }^{\prime }\right)+\sin \left({\vartheta }^{\prime }\right)\right)},\mathrm{mit}{\vartheta }^{\prime }=\vartheta \mathrm{mod}\frac{\pi }{3}& \left(11\right)\end{array}$

[0045] The output trajectory u.sub.αβ for the second actuating voltage {right arrow over (u)}.sub.23, which is required for the compensation of the torque ripple, is now compared here with the angle-dependent modulation limit U.sub.mod at defined angular values over one sixth of the modulation area. The required voltage reserve U.sub.res is predicted or ascertained from the maximum magnitude difference according to equation (12).

U.sub.res=max(u.sub.res(ϑ))=max(|U.sub.αβ(ϑ)|−|U.sub.mod,max(ϑ)|)   (12)

[0046] As can be seen from FIG. 4b, the additional maintenance of a voltage reserve U.sub.res is only required when, depending on the angle of the harmonic compensation voltage {right arrow over (u)}.sub.dq,comp, the output trajectory u.sub.αβ lies outside a modulation surface that is defined by the modulation limit U.sub.mod. Otherwise, the sixth-order electrical harmonic in the torque can be compensated for without additional sacrifice of torque using this method. The proposed method makes it possible to compensate for torque ripple while utilizing the non-linear modulation ranges of the three-phase pulsed inverter (over-modulation).