DC modulation controller parameters tuning based on improved multisignal Prony algorithm
Hongsheng Su^{1} , Zongkong Zhu^{2}
^{1, 2}School of Automation and Electrical Engineering, Lanzhou Jiaotong University, Lanzhou 730070, P. R. China
^{1}Corresponding author
Journal of Vibroengineering, Vol. 17, Issue 6, 2015, p. 32993312.
Received 18 June 2015; received in revised form 23 August 2015; accepted 28 August 2015; published 30 September 2015
JVE Conferences
To aim at the puzzle of DC modulation controller parameters tuning in largescale AC/DC interconnected power systems, in this paper a multisignal Prony algorithm is proposed which can simultaneously extracts oscillation modes from multiple signals compared with traditional Prony analysis method. In the algorithm, current setting value increment at rectifier side serves as system input, and AC liaison transmission line active power increment acts as the resulting output under consideration of systems initialization state. Through the improved multisignal Prony identification on the output timedomain response data under specified input, an equivalent linear model with order reduced is obtained. Based on the identified results, the adjustments are then implemented on the controller parameters using the pole placement method. Through theoretical analysis and IEEE four generators system tests, the simulation results show that to add the DC modulation controller with parameters tuned by the improved Prony algorithm can significantly increase the oscillation damping of AC/DC interconnected systems, and improve the systems operation stability.
Keywords: interarea low frequency oscillation, DC modulation, Prony algorithm, identification, pole placement, parameters tuning.
1. Introduction
With the expansion of AC/DC power grids interconnection, the size of modern power systems is becoming larger and larger, and the structure of which is becoming more and more complex, which results in a higher requirement on the analysis and control of systems. The analysis and suppression of interarea low frequency oscillation in AC/DC interconnected power grids now has already become a more difficult and important puzzle [13]. The traditional methods such as eigenvalues and frequency domain analysis require a complete detailed precise mathematical model, but usually to do so is a difficult task. In another hand, the modern identification technology can identify the system model reduced not rely on the mathematical model of each component [4]. The Prony identification can estimate the system oscillation modes through analysis on the measured data, which include the oscillation frequency, damping, amplitude and phase, and etc. Further, the identification can directly obtain the characteristic roots of systems, and the residue of transfer function, and other information. And thus, it can avoid having to create an accurate model of the system and solve highorder matrix. Hence, it is particularly suitable for analysis on power systems response signal and the design of control systems [5, 6].
In recent years, with the development of high voltage direct current (HVDC) transmission technology in China, there would be more than 20 ultra HVDC lines to be put into operation by 2020 [7]. In view of its fast response, and flexible control on the HVDC transmission systems, and as well as strong modulation capacity, DC modulation controller can be used to modulate the power of DC transmission line. This is thought to be one of the most effective means to suppress the interarea low frequency oscillation of interconnect power grids [8]. The relative investigations have shown that the selection of DC modulation signal, and load model, and the modulator parameters are the key elements to influence modulation effects. In [9] trajectory sensitivity is applied to analyze the DC modulator parameters, and the results are verified using a fourgenerator system. But the method needs to calculate systems gradient information, and it is difficult for the largescale AC/DC hybrid systems. In [10] modulator parameters are optimized by genetic algorithm (GA). Due to its stronger randomness of optimization algorithm, there are some shortcomings existing of slow convergence. In [11] Prony method is proposed to identify the system transfer function very convenient, and possesses higher accuracy than the test signal method.
Prony analysis possesses many applications in AC systems such as the design of excitation regulator and PSS, but there have been little attentions in AC/DC hybrid transmission systems. In addition, Prony methods always assume that the system is single output, and each signal is analyzed, independently, which often results in estimates conflicting in frequency and damping due to noise effects [12]. And so it is difficult to determine which signal identification result is most reasonable and accurate. In [13], an extended Prony algebraic interpolation scheme is proposed to find the nearest analytic function of algebraic interpolant on an equispaced grid, and the interpolation errors of the method are much lower compared with the classic schemes on equispaced grids, which can be effectively exploited for analytic interpolation of noisy or defected signals. But the method based on the nearest algebraic interpolant does not suppress the Runge phenomenon, the calculation will increase and produce more serious error accumulation such that the stability can not be guaranteed. In [14] wide area measurement system (WAMS) can obtain the global oscillation information, and provide full support to suppress the interarea low frequency oscillation, which make the multisignal combined identification possible. In this paper, on the basis of WAMS, multisignal is firstly introduced into Prony algorithm for identification of low frequency oscillation in AC/DC hybrid systems, and wavelet transform is then applied to eliminate the signal noise. Secondly, multi signals sample function matrix is established and singular value decomposedtotal least square (SVDTLS) method is used to determine the order of signal. Thirdly, the improved multisignal Prony algorithm is proposed to identify the system output characteristics, and transfer function is then obtained, and then combining with the pole placement method to adjust the DC modulation controller parameters. Finally, the applicability and superiority of the proposed method are verified through the IEEE fourgenerator system.
2. System transfer function identification based on Prony algorithm
2.1. Traditional Prony algorithm
Prony algorithm can fit several exponential functions into a signal though linear combination, and which is shown by [15]:
where $\widehat{x}\left(n\right)$ expresses the estimated value of the $n$th sampling point, and $N$ takes integer, and $p$ expresses the number of exponential functions and takes integer, and ${A}_{i}$ is the amplitude of signal trace, and ${\theta}_{i}$ is the corresponding phase (unit: rad), and ${\alpha}_{i}$ represents the attenuation factor, and ${f}_{i}$ means the oscillation frequency, and $\u2206t$ is the sampling interval.
2.2. Improved Prony algorithm
Traditional Prony algorithm always assumes that the system is single output, which is not consistent with power systems of singleinput and multipleoutput. Due to disturbance from noise and other factors, the obtained outcome will lead to conflicting modality estimates. And so it is difficult to determine which modality estimates are accurate. In addition, since power system is a complex large system, and for large systems, the single signal analysis on system oscillation mode is limited. In order to identify system oscillation modes as much as possible, the multiple signals are introduced to extract oscillation characteristics, and fit into each output under same modality so as to improve identification accuracy, and then:
where ${\widehat{x}}_{k}\left(n\right)$ presents the model of measured data, ${b}_{ki}$ and ${z}_{i}$ are both complex, and expressed by:
where ${A}_{ki}$ is the amplitude of the $k$th signal trace, and ${\theta}_{ki}$ is its phase, ${\alpha}_{i}$_{}, ${f}_{i}$ and $\u2206t$ possess same implications with Eq. (1).
Now we consider the multisignal traces, and cost function is constructed by:
where $M$ is the total number of signal traces, and ${x}_{k}\left(n\right)$ is the actual value of the $k$th signal trace, and ${\widehat{x}}_{k}\left(n\right)$ is the corresponding estimated value.
Similar to single signal trace derivation process, multiple signal traces apply a set of same exponential signal to approximate multiple signals, simultaneously, and make mean squares sum of all curves minimum. According to least mean squares (LMS), we can obtain the parameters of ${A}_{ki}$, ${\theta}_{ki}$,${\alpha}_{i}$ and ${f}_{i}$ [16].
${\widehat{x}}_{k}\left(n\right)$ meets the recursive difference equation described by:
Let $e\left(n\right)$ be the error between the measured data and the estimated value, and thus we have:
Substituting Eq. (5) into Eq. (6), we obtain:
${a}_{0}=1,\mathrm{}\mathrm{}\mathrm{}n=0,\mathrm{}1,\dots ,N1.$
Define $\epsilon \left(n\right)=\sum _{i=0}^{p}{a}_{i}e(ni)$, and we then have:
Define the cost function as:
From Eq. (9), we have:
And then we obtain:
Improved multisignal Prony algorithm is then described as follows.
1) To define sample function matrix by:
where:
and $M$ expresses the number of signal traces, and ${p}_{e}$ is the order of prediction model, and ${x}_{k}\left(i\right)$ is the $i$th sample point of the $k$th signal.
2) To obtain $\mathbf{a}$ by:
The effective rank $p$ of matrix $\mathbf{R}$, and as well as the coefficients ${a}_{1}$, ${a}_{2}$,…, ${a}_{p}$ of corresponding oscillation pattern can be determined using SVDTLS algorithm
3) The eigenvalues of the polynomial $1+{a}_{1}{z}^{1}+{a}_{2}{z}^{2}+...+{a}_{p}{z}^{p}=$0 can be calculated based on the ${a}_{1}$, ${a}_{2}$..., ${a}_{p}$. And then we can obtain by the following recursive formula:
where ${\widehat{x}}_{k}\left(0\right)={x}_{k}\left(0\right)$.
4) To calculate the parameters ${b}_{ki}$ according to the following equation:
5) To calculate frequency, and the attenuation factor, and the amplitude and phase of each signal as follows:
where $k$ denotes the $k$th signal, and $i$ denotes the $i$th component.
2.3. System transfer function identification
System model is shown in Fig. 1, where $G\left(s\right)$ expresses system transfer function, and $u\left(t\right)$ is system excitation signal, and $y\left(t\right)$ is system output, and ${y}_{ex}\left(t\right)$ is system stimulusresponse, and ${y}_{0}\left(t\right)$ is the initial state of system.
Fig. 1. System model
Pole residue form of $G\left(s\right)$ and ${Y}_{0}\left(s\right)$ can be expressed by:
where $n$ is the order of transfer function, and ${\lambda}_{i}$ is the eigenvalues of system, and ${R}_{i}$ is the residue of transfer function, and ${A}_{i}$ is the residue of initial state.
The aim to identify transfer function and initial state of system is to find the estimate values of ${\lambda}_{i}$, ${R}_{i}$, ${A}_{i}$ and $n$, such that the model output as close as possible to the actual output [17].
Let us assume that $U\left(s\right)$ is composed of limited entry delay factor ${c}_{i}$ and eigenvalues ${D}_{j}$, and then:
Consider the effect of the input signal $U\left(s\right)$, the output $Y\left(s\right)$ should contain the modes caused by the input signal and system itself, which can be expressed by:
$\mathrm{}\mathrm{}\mathrm{}\mathrm{}\mathrm{}\mathrm{}=\left({c}_{0}+{c}_{1}{e}^{s{D}_{1}}+{c}_{2}{e}^{s{D}_{2}}+\cdots +{c}_{k}{e}^{s{D}_{k}}\right)\sum _{i=1}^{n}\frac{{R}_{i}}{\left(s{\lambda}_{n+1}\right)\left(s{\lambda}_{i}\right)}+\sum _{i=1}^{n}\frac{{A}_{i}}{s{\lambda}_{i}}.$
By partial fraction, the above formula can be expanded by:
where:
Since $t\ge {D}_{k}$, so that ${D}_{0}=0$, then $y\left(t\right)$ is:
$\mathrm{}\mathrm{}\mathrm{}\mathrm{}\mathrm{}\mathrm{}+\cdots \mathrm{}+{Q}_{n+1}\left(\sum _{i=0}^{k}\mathrm{\u200d}{c}_{i}{e}^{{\lambda}_{n+1}{D}_{i}}\right){e}^{{\lambda}_{n+1}t}.$
Since $t$ is bound to be greater than ${D}_{k}$, the above formula can not be directly analyzed by Prony method. Let $\tau =t{D}_{k}$, and $v\left(\tau \right)=y\left(\tau +{D}_{k}\right)$, the above equation then can be written by:
Consider the nonzero initial state conditions [18], and then have further Prony identification, we will obtain the residue of transfer function:
Substituting the above formula into Eq. (22), the transfer function residue then is:
${B}_{j}$ and ${\lambda}_{j}$ in Eq. (26) can be obtained from Eq. (24) using Prony analysis, ${c}_{i}$, ${D}_{j}$ and ${\lambda}_{n+1}$ are obtained based on the input. Therefore, the input in Eq. (19) will be applied into the real system, then through the results of improved multisignal Prony analysis and further calculation, system transfer function can be obtained.
3. AC/DC power system model and HVDC additional damping control
3.1. Principle of AC/DC power system interaction
In the AC/DC power system simulation, to reflect the impact of DC system on AC system stability more accurately, here we apply more accurate HVDC quasisteadystate model in [1]. The AC system and DC system are independently solved, and AC system and DC system interacts as shown in Fig. 2. The impact of DC system on AC system may be seen as a change of load or voltage source. HVDC quick adjustment feature is implemented by changing the power of the variable power branch [19].
Fig. 2. Diagram of interaction of AC/DC system
3.2. DC modulation controller model
DC modulation controller model is used in [1]. In this paper, it is generally believed that the current control is fast, and constant current control can prevent a substantial change in current, limiting the overcurrent and preventing from the converter overload. And constant extinction angle control can avoid commutation failure at inverter side, and maintain the DC voltage at a high level, so we adopt the operation mode of constant current in rectifier side, and constant extinction angle in inverter side. The constant current controller and DC modulation model are shown in Fig. 3.
Fig. 3. DC modulation controller model
In Fig. 3, ${I}_{d}$ and ${I}_{0}$ denote the input signal of constant current controller and the current setting value of rectifier, respectively. ${T}_{W}$ denotes the time constant of blocking part, ${T}_{1}$ and ${T}_{2}$ denote the time constant of leadlag parts, ${K}_{HVDC}$ denotes the gain coefficient, subscript max and min denote the upper and lower limits of the corresponding variable amplitude.
The active power increment $\mathrm{\Delta}{P}_{ac}$ of AC liaison transmission lines is set as the input signal of DC modulator, and through the measurement, blocking part and phase compensator composed by a series of leadlag parts and amplification part to synthesize, eventually outputs additional power control signal through clipper. While the signal is overlapped with the power control command signal, through the output of constant current regulator in pole control unit and changes the trigger angle $\alpha $ command of rectifier, which is sent to the valve control units to control the DC power output. By adjusting the transmission power of DC lines, which can rapidly absorb and compensate for excess power or shortfall power connected thereto AC system, so that the power can reach equilibrium, and reduce the transmission pressure of AC transmission system. Serving to strengthen the effect of AC system damping and improving AC/DC interconnected system stability [20].
3.3. DC modulation controller design
In parallel AC and DC power transmission systems, The DC current setting value increment $\mathrm{\Delta}{I}_{0}$ is selected as the control variable, and the active power increment $\mathrm{\Delta}{P}_{ac}$ of AC liaison lines is set as the controlled variable. Assuming that identified system transfer function is $G\left(s\right)$, the controller transfer function is $H\left(s\right)\text{.}$ And $\mathrm{\Delta}{P}_{ac}$ is introduced as a feedback variable, the closedloop system is shown in Fig. 4.
Fig. 4. System closedloop block diagram
From Fig. 4, the system transfer function can be obtained by:
Assuming that after adding the feedback compensation parts, the new dominant pole of closedloop system is ${s}_{d}$, and the eigenvalues of system is moved to the location ${\lambda}_{0}$. Then ${\lambda}_{0}$ must satisfy the characteristic equation $1G\left(s\right)H\left(s\right)=$0 of the closedloop system, so we can get $H\left({s}_{d}\right)=1/G\left({s}_{d}\right)$, which can be written in the form of amplitude and phase angle below:
Therefore, through the amplitude and phase angle values at $s={s}_{d}$ of the identified system transfer function, we can obtain the amplitude and phase angle of DC modulation controller at ${\lambda}_{0}$, so that the new pole location will be selected to meet the specific damping ratio, then take advantage of leadlag links to meet phase compensation. Finally, we can select the gain to meet the amplitude equation.
3.4. Stability analysis with DC modulation controller
According to linear control theory [21], the characteristic polynomial of the $G\left(s\right)$ can be described as:
And then the poles of $G\left(s\right)$ is denoted as the roots of the characteristic equation ${\alpha}_{G}\left(s\right)=$0. If all the ploes is located on the left side of the imaginary axis in the complex plane, namely, they are the negative real numbers or possess the negative real parts, and then the system characterized by $G\left(s\right)$ can be said stable, and instable if there is a ploe located in imaginary axis or the right side of the imaginary axis in the complex plane otherwise.
The introduction of state feedback $H\left(s\right)$ changes the system transfer function, namely, $G\left(s\right)$ is converted to ${G}_{c}\left(s\right)$, and characteristic eauation ${\alpha}_{G}\left(s\right)$ to ${\alpha}_{Gc}\left(s\right)$, correspondingly, the roots of the characteristic eauation is changed. In other words, in system synthesis, to obtain desired properties we can apply diverse feedback matrix $H\left(s\right)$ to change the location of the zeros and ploes, since they possess significant inflence on system behavior. In this paper, from Fig. 3, we can select suitable $H\left(s\right)$ to change the location of the poles, such that the expected dynamical properties can be acquired.
4. Examples
Fig. 5 shows the structure of IEEE fourgenerator system, and system parameters can be found in [1], where the rated power of DC line is 1000 MW, and the rated voltage of AC line is 230 KV, the rated capacity of each generator is 900 MWA, rated voltage is 20 KV, and generator model includes the excitation system and the speed control system, and the load uses constant resistance, and as well as two terminals HVDC systems adopts quasisteadystate model, wherein the left side is the rectifier station, and the right one is the inverter station. The control system adopts the operation mode of constant current in rectifier side and constant extinction angle in inverter side. DC modulation controller is attached to the side of the rectifier side of the verification system. DC modulation controller is as shown in Fig. 3.
Fig. 5. IEEE fourgenerator test system
4.1. Modal identification based on improved multisignal algorithm
In this example, threephase short circuit fault occurs in the bus 7side starting at the 1.0 s, and is cleared at five cycle later. Each generator power angle curve closely related to the electromechanical oscillations is selected, and the Prony modal identification is adopted mentioned in Section 2.1. In this paper, the relative power angle of each generator and AC liaison line active power are set as the identification signals, and the generator G1 is considered as reference machine. Table 1 and Table 2 are respectively single signal and improved multisignal algorithm for each generator relative power angle identification results.
Seen from Table 1, when adopts the signals of different units each time can identify the dominant mode of system accurately, namely, the interarea oscillation mode. However, for the identification of local oscillation modes, the identification results are quite different. In model model 2, and model 3, and as well as model 4, applying the signals of same area can get different estimate results even contradictory results, which makes the choice of frequency and damping ratio of local oscillation modes become very difficult, and it is not conducive to have further identification. However, in Table 2, when using multiple signals can identify all oscillation modes, and the results are more accurate than the ones of single signal.
Table 1. Each generator power angle identification results based on single signal Prony algorithm
Identification signals and parameters

Mode 1

Mode 2

Mode 3

Mode 4


${\delta}_{21}$

$f$/ Hz

0.575

1.107

1.253

0.837

Damping ratio

0.016

0.062

–0.001

0.300


${\delta}_{31}$

$f$/ Hz

0.577

0.976

1.285

1.767

Damping ratio

0.016

0.135

0.035

0.046


${\delta}_{41}$

$f$ / Hz

0.575

0.866

1.110

1.110

Damping ratio

0.016

0.036

0.120

0.120


Comprehensive
analysis

$f$/ Hz

0.575

0.913

1.110

–

Damping ratio

0.016

0.175

0.120

–

Table 2. Generator power angle identification results based on improved multisignal Prony algorithm
Identification signals and parameters

Mode 1

Mode 2

Mode 3

Mode 4

$f$ / Hz

0.575

0.983

1.167

1.643

Damping ratio

0.016

0.054

0.125

0.084

4.2. System transfer function identification
The input signal of DC modulation controller is active power increment of AC liaison line between the two regions, and system transfer function is identified in accordance with Section 2.2. The current setting of DC side adds an excitation $\mathrm{\Delta}u$, and carries on the Prony analysis, we then obtain the transfer function from DC line at rectifier side current setting to AC liaison line active power. Table 3 shows the system initial state and reduced order transfer function based on improved multisignal Prony algorithm identification. System output curves fitting results are shown in Fig. 6.
Table 3. Order transfer function and initial state of $\mathrm{\Delta}u\to \mathrm{\Delta}{P}_{ac}$
$n$

${\lambda}_{i}$

${A}_{i}$

${R}_{i}$

1

–9.158

0.0030

1.2328j0.0001

2

–0.0561+j3.5101

–0.0046+j0.0162

2.1245+j3.1360

3

–0.0561j3.5101

–0.0046j0.0162

2.1245j3.1360

4

–0.1815+j5.6490

–0.0015+j0.0031

0.8405+j1.3267

5

–0.1815j5.6490

–0.0015j0.0031

0.8405j1.3267

6

–0.5865+j6.1839

0.0001+j0.0205

0.2175+j0.5033

7

–0.5865j6.1839

0.0001j0.0205

0.2175j0.5033

8

–0.4812+j7.0375

–0.0037+j0.0007

0.2096+j0.1741

9

–0.4812j7.0375

–0.0037j0.0007

0.2096j0.1741

10

–1.2486+j10.2399

0.0012+j0.0046

0.3876+j2.9004

11

–1.2486j10.2399

0.0012j0.0046

0.3876j2.9004

From the analysis of Table 3, eigenvalues (–0.0561±j3.5101) and (–0.1815±j5.6490) show the mode of the system interarea low frequency oscillation, damping ratio is small, so attenuation is slow, while the former residue is larger than that of the latter, therefore the former is system dominant oscillation mode. Additional DC modulation controller to form a closedloop system, using the pole placement method and the damping ratio of system dominant mode will be increased to 0.15, the dominant eigenvalues is selected as 0.485±j3.20. The corresponding oscillation frequency is 0.51 Hz, and then obtain amplitude and phase of controller, which are respectively 6.28 and 113.04 deg.
According to DC modulation controller model in Fig. 3, the transfer function of DC modulation controller is shown by:
where ${T}_{w}$ is blocking time constant, which has no relation with the damping property of the controller, and generally takes for 10 s, in order to meet the requirement of improving dynamic stability, power modulation amplitude can achieve 3 % to 10 % of the DC power, so the power limiting link is ±30 MW.Through the phase requirements we can calculate ${T}_{1}$ and ${T}_{2}$, then according to the amplitude can obtain gain $K$, the final transfer function of DC modulation controller is obtain by:
Fig. 6. Identified model output data versus actual data
4.3. Simulation results
Under the condition of above fault, these three cases are simulated in time domain without DC modulation, adds the DC modulator of traditional Prony design and DC modulator designed based on improved multisignal Prony algorithm. The power angle of generator and AC liaison line active power steadystate simulation results are shown in Figs. 7 and 8.
Fig. 7. Angle swing curves of G4 refer to G1
Fig. 910 are respectively by changing the operating mode and fault mode to verify the robustness of DC modulation controller whose parameters has been tuned. In Fig. 9, failure mode changes for the threephase short circuit occurs in the bus 8 side, after 5 cycles fault is cleared. In Fig. 10, the L78 AC liaison line active power is transmitted by increased from 210 MW to 306 MW, the fault pattern is unchanged.
Fig. 8. Active power oscillation curves of the intertie 78
Fig. 9. Active power oscillation curves of the intertie 78 as system failure mode changing
Fig. 10. Active power oscillation curves of the intertie 78 as system operating mode changing
The simulation results show that the additional DC modulation controllers can indeed play a role in suppressing the interarea low frequency oscillation, and the modulation controller parameters is the key to affecting the modulation effect. Controller designed based on the traditional single machine infinite theoretical analysis and combination of engineering practical experience can achieve a certain damping effect on power oscillation. The controller designed based on improved multisignal Prony algorithm, then adopts pole placement and combines with the identification results to adjust controller parameters, since the identified transfer function contains information between generators and DC modulation controller, which more comprehensively consider the interaction of the whole system. The simulation shows that to add controller designed by improved algorithm makes the system can restore stability less than 10 s after a disturbance, however, the system need longer time to restore without DC modulation controller, which is not conducive to make the system have a stable operation.
Therefore system adds the controller designed by improved multisignal Prony algorithm can improve the system damping effect greatly. It not only suppress interarea low frequency oscillation, but also improve the stability of interconnected AC/DC system, which is consistent with the former theoretical analysis.
5. Conclusions
This paper analyzes low frequency oscillation modes of the AC/DC power transmission systems, and aims at the flaws of traditional Prony algorithm in applications, and proposes analysis method based on multiple signals Prony algorithm, and gives out the calculating process and experiment verification. The applications shows that the proposed method improves the identification accuracy and control effects and does not depend on the accurate mathematical model and parameters tuning, which can lay the foundation for the coordination optimization between controllers. DC modulation controller designed by improved multisignal Prony algorithm can effectively improve the damping effect of the systems, and suppress interarea low frequency oscillation so as to increase the stability of the overall system operation.
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