VOLTAGE SOURCE CONVERTER (VSC) CONTROL SYSTEM WITH ACTIVE DAMPING

Abstract

A Voltage Source Converter control system for active damping of a resonance oscillation in the VSC includes a regular Phase-Locked Loop 2, and a slow PLL 3. The control system is arranged such that an imaginary part of the AD is obtainable from the slow PLL. The slow PLL is configured for having a closed-loop bandwidth which is less than a frequency, in a synchronous dq frame, of the resonance oscillation to be dampened.

Claims

1.-9. (canceled)

10. A Voltage Source Converter, VSC, control system for active damping, AD, of a resonance oscillation in the VSC, the resonance oscillation having a frequency which is above the synchronous frequency but less than two times said synchronous frequency, the control system comprising: a first Phase-Locked Loop, PLL, having a first PLL controller; and a second PLL having a second PLL controller, the second PLL controller having a gain which is lower than the gain of the first PLL controller, wherein the control system is arranged such that an imaginary part of the AD signal is obtainable from the second PLL; and wherein the second PLL is configured for having a closed-loop bandwidth which is less than the frequency, in a synchronous dq frame, of the resonance oscillation to be dampened.

11. The control system of claim 10, wherein the second PLL is configured for having a closed-loop bandwidth which is less than 100, such as less than 50, radians per second, e.g. in the range of 5 to 40 or 5 to 20 radians per second.

12. The control system of claim 10, wherein the second PLL is configured for having a closed-loop bandwidth which is a fraction of the closed-loop bandwidth of the first PLL, e.g. in the range of to 1/20 of the closed-loop bandwidth of the first PLL.

13. The control system of claim 10, wherein the control system is arranged such that a real part of the AD is obtainable via a High-Pass Filter, HPF, of the control system.

14. The control system of claim 10, wherein the control system is arranged such that a real part of the AD is obtainable by tapping an input signal to an Alternating Current Voltage Control, ACVC, of the control system.

15. The control system of claim 10, wherein the resonance oscillation has a frequency within the range of 1.3 to 2 times the synchronous frequency.

16. The control system of claim 10, wherein the resonance oscillation has a frequency of 1.3 times the synchronous frequency.

17. The control system of claim 10, wherein the resonance oscillation has a frequency of 1.5 times the synchronous frequency.

18. A method of active damping, AD, of a resonance oscillation in a Voltage Source Converter, VSC, by means of a VSC control system, the resonance oscillation having a frequency which is above the synchronous frequency but less than two times said synchronous frequency, wherein the control system comprises: a first Phase-Locked Loop, PLL, having a first PLL controller, and a second PLL having a second PLL controller, the second PLL controller having a gain which is lower than the gain of the first PLL controller, wherein the control system obtains an imaginary part of the AD signal from the second PLL; and wherein the second PLL has a closed-loop bandwidth which is less than the frequency, in a synchronous dq frame, of the resonance oscillation being dampened.

19. The control system of claim 11, wherein the second PLL is configured for having a closed-loop bandwidth which is a fraction of the closed-loop bandwidth of the first PLL, e.g. in the range of to 1/20 of the closed-loop bandwidth of the first PLL.

20. The control system of claim 11, wherein the control system is arranged such that a real part of the AD is obtainable via a High-Pass Filter, HPF, of the control system.

21. The control system of claim 12, wherein the control system is arranged such that a real part of the AD is obtainable via a High-Pass Filter, HPF, of the control system.

22. The control system of claim 11, wherein the control system is arranged such that a real part of the AD is obtainable by tapping an input signal to an Alternating Current Voltage Control, ACVC, of the control system.

23. The control system of claim 12, wherein the control system is arranged such that a real part of the AD is obtainable by tapping an input signal to an Alternating Current Voltage Control, ACVC, of the control system.

24. The control system of claim 11, wherein the resonance oscillation has a frequency within the range of 1.3 to 2 times the synchronous frequency.

25. The control system of claim 12, wherein the resonance oscillation has a frequency within the range of 1.3 to 2 times the synchronous frequency.

26. The control system of claim 13, wherein the resonance oscillation has a frequency within the range of 1.3 to 2 times the synchronous frequency.

27. The control system of claim 14, wherein the resonance oscillation has a frequency within the range of 1.3 to 2 times the synchronous frequency.

28. The control system of claim 11, wherein the resonance oscillation has a frequency of 1.3 times the synchronous frequency.

29. The control system of claim 12, wherein the resonance oscillation has a frequency of 1.3 times the synchronous frequency.

Description

BRIEF DESCRIPTION OF THE DRAWINGS

[0009] Embodiments will be described, by way of example, with reference to the accompanying drawings, in which:

[0010] FIG. 1 is a schematic circuit diagram of a standard VSC control system.

[0011] FIG. 2 is a schematic illustration of a main-circuit model.

[0012] FIG. 3 is a schematic circuit diagram of a VSC control system with AD according to prior art.

[0013] FIG. 4 is a schematic circuit diagram of an embodiment of a VSC control system with AD according to the present invention.

[0014] FIG. 5 is a schematic circuit diagram of another embodiment of a VSC control system with AD according to the present invention.

DETAILED DESCRIPTION

[0015] Embodiments will now be described more fully hereinafter with reference to the accompanying drawings, in which certain embodiments are shown. However, other embodiments in many different forms are possible within the scope of the present disclosure. Rather, the following embodiments are provided by way of example so that this disclosure will be thorough and complete, and will fully convey the scope of the disclosure to those skilled in the art. Like numbers refer to like elements throughout the description.

[0016] The cause of resonance destabilization is negative-resistance behaviour resulting from the various cascaded and parallel controllers that make up the VSC control system. A typical control system is depicted in FIG. 1, where the PLL is illustrated within the dashed line, boldface letters denote complex space vectors and the superscript s denotes the stationary reference frame. The controllers work as follows:

[0017] The Direct Current (DC or dc) voltage controller (DCVC) operates on the error between the dc-voltage reference u.sub.dc.sup.ref and the actual dc voltage u.sub.dc. Its output is the active-power-producing current reference i.sub.d.sup.ref. Reference u.sub.dc.sup.ref may be adjusted by an outer active-power controller in a cascaded fashion.

[0018] The ac-voltage controller (ACVC) operates on the error between the point-of-common-coupling (PCC)-voltage reference u.sub.pcc.sup.ref and the actual PCC-voltage modulus u.sub.pcc=|u.sub.pcc.sup.s|. Its output is the reactive-power-producing current reference i.sub.q. Reference up, may be adjusted by an outer reactive-power controller in a cascaded fashion.

[0019] Both current references are fed to the ac-current controller (ACCC), whose outputs are the VSC phase-voltage references u.sub.a,b,c.sup.ref, which form the input to the pulse width modulator. The ACCC may be implemented in the frame or in the synchronous dq frame. The ACCC has as input signals also the converter input current i.sup.s and the transformation angle (or the exponential factors e.sup.j thereof).

[0020] The transformation angle is computed by the phase-locked loop (PLL), whose input u.sub.pccq is the imaginary part of the dq-transformed PCC voltage u.sub.pcc=e.sup.ju.sub.pcc.sup.s. Input u.sub.pccq is fed to the PLL controller (PLLC), to whose output the nominal angular synchronous frequency .sub.nom is added, forming the instantaneous angular frequency co. This is then integrated into the transformation angle (modulo 271).

[0021] All the mentioned controllers are normally of proportionalintegral (PI) type.

[0022] To test the damping scheme proposed by Alawasa et al., a test system is implemented in Matlab, using a per-unit (pu) system. The base frequency is set to the synchronous frequency 50 Hz, but all other base values are unspecified. The main circuit is as shown in FIG. 2. An LC series resonance (comprising an inductor L and a capacitor C), with resonant frequency f.sub.res=1/(2{square root over (L.sub.bC.sub.b)}), is inserted as a branch at the PCC. L is the phase-reactor-plus-transformer inductance and Lg is the grid inductance in front of the stiff grid voltage .sub.g. The inductances are selected as L=Lg=0.1 pu and Lb=1 pu. The closed-loop bandwidths of the respective control loops are chosen as ACCC: 4 pu, PLL: 1 pu, and DCVC: 0.5 pu. The ACVC proportional gain it set to 1 pu. Integral action is added to all controllers. The ACCC is implemented in the frame, implying that a generalized integrator (i.e., a resonator at the synchronous frequency) is used.

[0023] Three cases are evaluated, all for inverter operation at 0.9 pu active power, but with different LC resonant frequencies. Relatively well-damped operation is obtained for f.sub.res=2f.sub.1, poorly damped operation for f.sub.res=1.5 f.sub.1, and unstable operation for f.sub.res=1.3f.sub.1.

[0024] As mentioned above, to mitigate subsynchronous torsional interaction, damping controllers can be added to the VSC control system. Two interesting damping schemes (and their combination) are proposed by Alawasa et al.

[0025] The rationale behind the first scheme is to inject a contribution to the current reference vector i.sub.ref=i.sub.d.sup.refji.sub.g.sup.ref, where j is the square root of 1, as

i.sub.ref.sup.modified=i.sub.ref+B(s)u.sub.pcc(1)

[0026] where B(s) (s=d/dt) is a bandpass filter. The scheme can be generalized (enhanced) as shown in FIG. 3, where the active damper (AD) operates on the difference between u.sub.pcc and its reference as

i.sub.ref.sup.modified=i.sub.ref+AD(u.sub.pccu.sub.pcc.sup.ref).(2)

[0027] The AD can now, theoretically, be a proportional gain G.sub.a, which acts as an active conductance

i.sub.ref.sup.modified=i.sub.ref+G.sub.a(u.sub.pccu.sub.pcc.sup.ref).(3)

[0028] In practice, however, a low-pass filter may be added to suppress disturbances of higher frequencies. A hard limiter may also be added to avoid large transient injections.

[0029] The scheme proposed by Alawasa et al. in accordance with FIG. 3 is shown to give improved damping at subsynchronous frequencies. However, it often fails to stabilize a resonance close to, but above, the synchronous frequency, as will now be shown. We set G.sub.a=4 pu and obtain results in which the amplitudes of the oscillations in response to a step change no longer appear to grow over time for f.sub.res=1.3 f.sub.1, but the system is only marginally stable. Increasing G.sub.a does not give improved stability.

[0030] The proposed scheme of Alawasa et al. manages to add damping that compensates negative impact of the ACVC and the DCVC, but negative impact of the PLL actually increases. This can be understood as follows. Let us consider a scenario when the system is in the steady state, but oscillations of small amplitudes start to occur. These are modelled as incremental variables, denoted with the prefix A. For the PCC voltage, we thus have

u.sub.pcc.sup.s=e.sup.j.sup.1.sup.t(u.sub.pcc.sup.ref+u.sub.pccd+ju.sub.pccq).(4)

[0031] and for the transformation angle

=.sub.1t+.(5)

[0032] Now, the dq transformation of the PCC voltage is given by

u.sub.pcc=e.sup.ju.sub.pcc.sup.s=e.sup.j(.sup.1.sup.t+)e.sup.j.sup.1.sup.t(u.sub.pcc.sup.ref+u.sub.pccd+ju.sub.pccq).(6)

[0033] Since is small, e.sup.j1j, giving

u.sub.pcc(1j)(u.sub.pcc.sup.ref+u.sub.pccd+ju.sub.pccq).(7)

[0034] Neglecting cross products of quantities yields

u.sub.pccu.sub.pcc.sup.ref+u.sub.pccd+j(u.sub.pccqu.sub.pcc.sup.ref)(8)

and

u.sub.pccu.sub.pcc.sup.ref=u.sub.pccd+j(u.sub.pccqu.sub.pcc.sup.ref).(9)

[0035] This shows that the correct d component, u.sub.pccd, of the error u.sub.pccu.sub.pcc.sup.ref is obtained, whereas in the q component a parasitic contribution is added: the term proportional to . This term is the reason for negative impact of the PLL in the scheme shown in FIG. 3.

[0036] The negative PLL impact found in (9) can be reduced to a minimum by modifying the control scheme to the schemes 1 shown in FIGS. 4 and 5. According to FIG. 5, the d part of the active damping (ADO) is obtained by tapping the input signal to the ACVC. This gives the correct signal (after a sign change), because the modulus of (4) with u.sub.pcc.sup.ref subtracted is given by

[00001]$\begin{array}{cc}.Math.u_{\mathrm{pcc}}^s.Math.-u_{\mathrm{pcc}}^{\mathrm{ref}}=.Math.u_{\mathrm{pcc}}^{\mathrm{ref}}+.Math..Math.u_{\mathrm{pccd}}+j.Math..Math..Math..Math.u_{\mathrm{pccq}}.Math.-u_{\mathrm{pcc}}^{\mathrm{ref}}=\sqrt{{\left(u_{\mathrm{pcc}}^{\mathrm{ref}}+.Math..Math.u_{\mathrm{pccd}}\right)}^2+.Math..Math.u_{\mathrm{pccq}}^2}-u_{\mathrm{pcc}}^{\mathrm{ref}}=u_{\mathrm{pcc}}^{\mathrm{ref}}.Math.\sqrt{1+\frac{2.Math..Math..Math.u_{\mathrm{pccd}}}{u_{\mathrm{pcc}}^{\mathrm{ref}}}+{\left(\frac{.Math..Math.u_{\mathrm{pccd}}}{u_{\mathrm{pcc}}^{\mathrm{ref}}}\right)}^2+{\left(\frac{.Math..Math.u_{\mathrm{pccq}}}{u_{\mathrm{pcc}}^{\mathrm{ref}}}\right)}^2}-u_{\mathrm{pcc}}^{\mathrm{ref}}{u}_{\mathrm{pcc}}^{\mathrm{ref}}.Math.\sqrt{1+\frac{2.Math..Math..Math.u_{\mathrm{pccd}}}{u_{\mathrm{pcc}}^{\mathrm{ref}}}}-u_{\mathrm{pcc}}^{\mathrm{ref}}.Math..Math.u_{\mathrm{pccd}}.& \left(10\right)\end{array}$

[0037] The q part of the active damping (AD.sub.q) is obtained by tapping the input signal u.sub.pccq.sup.s to an added slow PLL 3 (denoted with the sub- or superscript s). The gain of the slow PLL controller (PLLC.sub.s) shall be significantly lower than that of the regular PLL 2 (PLLC).

[0038] The slow PLL 3 should have a bandwidth which is less than the frequency, as referred to the synchronous dq frame, of the oscillations to be dampened. Thus, the slow PLL 3 is slower, is running at a lower frequency, than the oscillations to be dampened such that Os (the angle tracking u.sub.pcc.sup.s) does not include said oscillations.

[0039] For example, in some embodiments, the slow PLL 3 may be configured for having a closed-loop bandwidth which is a fraction of the closed-loop bandwidth of the regular PLL 2, e.g. in the range of to 1/20 of the closed-loop bandwidth of the regular PLL.

[0040] In some embodiments, the slow PLL 3 may be configured for having a closed-loop bandwidth which is less than 100, such as less than 50, radians per second, e.g. in the range of 5 to 40 or 5 to 20 radians per second.

[0041] PLLC.sub.s shall preferably not have an integral part. AD.sub.d and AD.sub.q may be low-pass filters with equal or different gains, possibly with hard limiters added.

[0042] It is not a necessity to include ac- and dc-voltage controllers, DCVC and ACVC in FIG. 5. As long as the regular (fast) PLL 2 is used, the active damping contribution in the q direction may be added without modification. For the d direction contribution, a substitute for the reference u.sub.pcc.sup.ref, may be found, e.g. by means of a high-pass filter (HPF) |.sub.pcc.sup.s|, as shown in FIG. 4. Consider (4) with u.sub.pcc.sup.ref=U.sub.pcc, we get

[00002]$\begin{array}{cc}.Math.u_{\mathrm{pcc}}^s.Math.=.Math.U_{\mathrm{pcc}}+.Math..Math.u_{\mathrm{pccd}}+j.Math..Math..Math..Math.u_{\mathrm{pccq}}.Math.=\sqrt{{\left(U_{\mathrm{pcc}}+.Math..Math.u_{\mathrm{pccd}}\right)}^2+.Math..Math.u_{\mathrm{pccq}}^2}=U_{\mathrm{pcc}}.Math.\sqrt{1+\frac{2.Math.U_{\mathrm{pcc}}.Math..Math..Math.u_{\mathrm{pccd}}+.Math..Math.u_{\mathrm{pccd}}^2+.Math..Math.u_{\mathrm{pccq}}^2}{U_{\mathrm{pcc}}^2}}{U}_{\mathrm{pcc}}\left(1+\frac{1}{2}.Math.\frac{2.Math.U_{\mathrm{pcc}}.Math..Math..Math.u_{\mathrm{pccd}}+.Math..Math.u_{\mathrm{pccd}}^2+.Math..Math.u_{\mathrm{pccq}}^2}{U_{\mathrm{pcc}}^2}\right)U_{\mathrm{pcc}}+.Math..Math.u_{\mathrm{pccd}}.& \left(11\right)\end{array}$

[0043] If the cut-off frequency of the high-pass filter is set lower than the frequency (as referred to the dq frame) of the oscillation that is to be damped, then the oscillating component u.sub.pccd passes through, whereas the mean value U.sub.pcc is rejected:

HPF(|u.sub.pcc.sup.s|)HPF(U.sub.pcc+u.sub.pccd)=u.sub.pccd.(12)

[0044] The regular PLL 2 is still used to translate to the dq coordinate system. It may form its input signal as follows. Suppose that u.sub.pcc.sup.s=U.sub.pcce.sup.j1. Then

u.sub.pccq=Im{e.sup.ju.sub.pcc.sup.s}=U.sub.pccIm{e.sup.j(.sup.1.sup.)}=U.sub.pcc sin(.sub.1).(13)

[0045] The closed loop formed around the PLL controller forces to converge to 1, such that u.sub.pccq=0 in the steady state. This is why active damping with u.sub.pccq tapped from the regular PLL 2 may fail. The oscillations that are to be damped are suppressed in u.sub.pccq, since the regular PLL 2 may have too fast tracking in relation to the oscillation frequency. Slowing down the regular PLL would degrade the dynamic properties of the control system (such as the response in the ac- and dc-voltage control) and is not an option. This is why the slow PLL 3 has been added. The closed-loop bandwidth of the slow PLL 3 should be lower than the frequency (as referred to the dq frame) of the oscillation that is to be damped.

[0046] If the bandwidth of the slow PLL 3 is set to 0.02 pu and the same active conductance G.sub.a=.sub.4 pu is used in both AD.sub.d and AD.sub.q. The new active damping scheme is evaluated for f.sub.res=1.3 f.sub.1, giving a significantly improved damping compared with the scheme of Alawasa et al.

[0047] The damping method of the present invention may be straight-forward to implement in existing e.g. HVDC control systems. It offers the potential of resistance to detrimental subsynchronous torsional interaction, regardless of the torsional frequencies. It may also be conjectured that stable operation using current control mode may be possible even for very weak grids.

[0048] The present disclosure has mainly been described above with reference to a few embodiments. However, as is readily appreciated by a person skilled in the art, other embodiments than the ones disclosed above are equally possible within the scope of the present disclosure, as defined by the appended claims.