 Original research
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Design of a robust PIDPSS for an uncertain power system with simplified stability conditions
Protection and Control of Modern Power Systems volume 5, Article number: 20 (2020)
Abstract
In a deregulated power system uncertainty exists and lack of sufficient damping can lead to Low Frequency Oscillations (LFO). The problem can be addressed using robust Power System Stabilizers (PSS). In this paper, an optimal procedure to design a robust PIDPSS using interval arithmetic for the Single Machine Infinite Bus (SMIB) power system is proposed. The interval modelling captures the wide variations of operating conditions in bounds of system coefficients. In the proposed design procedure, simple and new closed loop stability conditions for an SMIB interval system are developed and are used to design an optimum PIDPSS for improving the performance of an SMIB system. The optimum PIDPSS is attained by tuning the parameters using the FMINCON tool provided in MATLAB. The robustness of the proposed PIDPSS design is validated and compared to other notable methods in the literature when the system is subjected to different uncertainties. The simulation results and performance error values show the effectiveness of the proposed robust PIDPSS controller.
Introduction
Synchronous generators are equipped with high gain AVRs to enhance stability margins. However, although high gain AVRs improves the synchronizing torque they have a negative effect on the damping torque. This could result in low frequency oscillation. Transmission networks connected by weak lines are also susceptible to low frequency oscillation. To overcome these problems, synchronous generators are equipped with PSS to provide auxiliary signals to the excitation system [1,2,3,4,5,6,7]. The design of conventional PSS parameters is usually based on a fixed operating condition, and hence variation in the operating condition may cause poor performance of PSS and sometimes lead to system instability.
Much research has been carried out in PSS parameter tuning for a wide range of operating conditions that include application of modern tools like ANN and Fuzzy Logic, optimization techniques, FACTS, adaptive controllers and robust controllers etc. A power system is highly nonlinear and therefore PSS design using ANN [8, 9] assures good dynamic stability. However, it requires a good training data set covering all types of uncertainties in the system. This is difficult to realize in practice. On the other hand, extensive previous knowledge of system behavior is required for Fuzzy Logic application [10, 11]. Metaheuristic methods [12,13,14,15,16,17,18] like PSO, GA, Harmony Search, Firefly and Whale Optimization are also used for tuning PSS parameters. In [19] SVC provided with a supplementary damping controller (SDC) is developed for suppression of inter area oscillations, and a PI controller is designed using Kharitonov’s theorem by stabilizing sixteen transfer functions. Various techniques have been proposed for the coordination control of PSS and FACTS devices [20,21,22]. The MRACs proposed in [23] require continuous measurements to determine the error between system response and model reference, while a fuzzy observer and regulator are designed in [24, 25], and sufficient conditions are derived in terms of LMI inequalities. Methods such as pole placement [26] using state feedback require all the state variable information, whereas model uncertainties are presented as a linear fractional transformation in [27] and the controller is designed using a quadratic performance index resulting in a controller with the same order as the plant. Robust PSS design using H_{∞} & μ synthesis are described in [28,29,30,31], although finding the weighting factor is an additional task in the H_{∞} method. The LMI technique [32,33,34] locates all the closed loop poles in a prespecified bound. The problem of existing uncertainties in the controller gains is addressed in [35] using the socalled resilient control. Soliman et al., [36, 37] use Kharitonov’s theorem to design a leadlag compensator by stabilizing eight extreme polynomials using PSO. In [38] a multiobjective function is developed to minimize the overshoots to keep the control signal within limits. A different approach for robust PSS is developed in [39] using root locus analysis. Design of a robust threeterm PSS is given in [40], while necessary and sufficient conditions are derived by using the interval RouthHurwitz criterion in [41]. In [42], two controllers, one for excitation and the other for the governor, are proposed to enhance system stability in the case of controller failure. The PSS design for a multimachine system is developed using a whale optimization technique [43], while the effect of penetration of wind farms on small signal stability is studied in [44]. To cater for the multiple requirements of power systems, a wide area damping controller is designed in [45]. Stability conditions for fixed and interval polynomials are addressed in [46, 47], while the MFAC proposed in [48] damps the interarea LFO. A multiband fractional order PSS design is reported in [49], in which three different frequency bands instead of one are used to damp the LFO, and the advantages of FOPSS are exploited. In [50], a frequency response matching technique is used to find suitable PSS and TCSC controller parameters. The design of control devices for engineeering applications are explained in [51], whereas the practical data of the BarkaII power station in Oman is used and PSS is designed for one of the gas units in [52].
In most existing methods, control parameters are only tuned for a few operating points and therefore, the controller may fail or degrade its performance when significant deviation in the system operating state occurs. Furthermore, to deal with significant load variation, for each loading condition, e.g., light, nominal or heavy, a separate controller is proposed for the system to ensure the desired dynamic response. This would add additional cost to the system. Some of the proposed methods require extensive system variable information or exhaustive eigenvalue analysis. Therefore, as the system size increases, the complexity and computational efforts also increase. On the other hand, a controller design employing interval systems uses the following methods: 1) Eight extreme polynomials; 2) The Interval Routh Hurwitz criterion; and 3) Image set polynomials for 1024 operating conditions. Even though these methods exhibit robust stability, they require high computational effort. To overcome the above issues, this paper presents a systematic procedure to develop simple and new stability conditions for an interval system. The main advantage of the proposed method is that a single controller with fixed parameters can cope with the uncertainties in the system for a wide range of operating conditions without compromising the desired dynamic performance. Since the controller design formulation is based on system coefficients rather than system variables, the controller exhibits robust stability and performance for unmodelled dynamics like variations in transmission line reactance and machine inertia etc.
In order to eliminate the limitations and drawbacks of the existing methods, in this research work, an SMIB system with varying operating conditions over a specified range, i.e., P ϵ [0.2, 1.2] and Q ϵ [− 0.4, 0.4], is considered. This represents fourthorder 1024 linear models (transfer functions) and extreme values are taken as lower and upper coefficients of the interval system. A robust PIDPSS is designed for the SMIB interval system, one that provides sufficient damping for the entire 1024 operating states. The PIDPSS parameters are obtained using the newly developed stability conditions for interval systems, and to ensure the robust performance of the proposed PIDPSS, an objective function at a nominal operating point is defined. The parameters of the proposed controller are tuned by minimizing this objective function while satisfying the specified constraints. To test the efficacy of the proposed controller, the system is subjected to mechanical step disturbance under a wide range of operating states, and simulation results with the proposed controller are compared to the methods in the literature.
This paper is organized as follows. Section 2 describes the problem formulation and Section 3 develops the new stability conditions for robust stability of an SMIB interval system. Section 4 describes the proposed design procedure for tuning the PIDPSS parameters, and Section 5 presents the simulation results to validate the proposed controller. Finally, Section 6 draws the conclusion.
Problem formulation
Considering a power system consisting of a single machine connected to an infinite bus as shown in Fig. 1, the dynamic state of the system can be given by the following nonlinear equations:
where δ is the rotor angle, ω_{o} and ω are the synchronous speed and rotor angular speed, respectively. M is the inertia constant, T_{m} is the mechanical torque and T_{e} is the electrical torque. E_{q}^{'} is the field flux in transient state, T_{do}' is the daxis open circuit time constant, and X_{d}' and X_{q}' are the dand qaxis transient reactances respectively. E_{fd} is the field voltage, K_{E} and T_{E} are the respective gain and time constant of the exciter, i_{d} and i_{q} are the d and qaxis armature current components, respectively. V_{ref} and V_{t} are the reference and terminal voltages, respectively. These equations can be linearized around the operating point for small signal stability analysis. This is shown by the block diagram in Fig. 2, developed by Demello and Concordia [1] known as the HeffronPilliphs model.
Except k_{3}, the parameters of the model k_{1}k_{6} are load dependent and their analytical expressions are given in [37]. The transfer function of the plant without PSS can be obtained using Manson’s rule for Fig. 2 and is given as:
The coefficients of the transfer function are:
where \( T={k}_3{T}_{do}^{\hbox{'}} \)_{.}
The coefficients of the transfer function depend on the machine inertia constant, transmission line reactance, field time constant, machine loading conditions and exciter time constant. The load on the system varies continuously and hence the coefficients change for a given system. As the operating point is varied over a specified range, i.e., P ϵ [P_{min}, P_{max}] and Q ϵ [Q_{min}, Q_{max}], the coefficient upper and lower bounds can be determined. Then, the transfer function can be approximated by the following interval polynomial [53]:
where
for i = 1,2,3,4.
For some operating points, the open loop system is unstable. Hence, a controller needs to be designed to robustly stabilize the system for all operating conditions. Figure 3 shows the equivalent block diagram of the closed loop system, where G_{c}(s) is the transfer function of the controller and U(s) is the controller output.
This paper presents a systematic procedure to design a robust PIDPSS with fixed parameters while the operating point is varied over a specified range, i.e., P ϵ [P_{min}, P_{max}] and Q ϵ [Q_{min}, Q_{max}]. The stability of the interval polynomials is addressed in [46] using the Nie [47] conditions for a fixed polynomial. New necessary and sufficient conditions for SMIB system are then developed to design the controller parameters of the robust PIDPSS for a specified range of operating conditions.
Development of new stability conditions for robust stability of an SMIB system
A set of real interval polynomials of degree ‘n’ is considered to be in the form of:
where the real coefficient a_{i} varies within a range of lower and upper bounds, i.e.:
\( {a}_i=\left[{a}_i^{},{a}_i^{+}\right] \) for i = 1,2,3…..n.
It is assumed that the degree of the polynomial remains invariant over the family.
Such a set of polynomials is called a real interval family and is referred to as an interval polynomial. The set of polynomials given by (5) is stable if and only if each and every element of the set is a Hurwitz polynomial. The necessary and sufficient conditions for the robust stability of interval polynomial (5) are developed using the algebraic stability criterion for fixed polynomials due to Nie [47] and are described below.
Nie stability conditions for a fixed polynomial
Consider a real fixed polynomial of degree ‘n’ of the form:
Lemma 3.1.1:
A necessary condition so that the roots of Q(s) lie in the left half plane is:
Lemma 3.1.2:
A sufficient condition so that the roots of Q(s) lie in the left half plane is:
Stability conditions of the SMIB system with interval coefficients
The above stability conditions for a fixed polynomial due to Nie [47] are used to obtain the stability conditions for an SMIB system with interval polynomial. These are developed from [46].
Lemma 3.2.1:
The interval polynomial D(s, a) defined in (5) is Hurwitz for all \( {a}_i\in \left[{a}_i^{},{a}_i^{+}\right] \) where i = 0,1,2,3….. n, if the following necessary conditions are satisfied:
a_{i} > 0and a_{i}a_{i + 1} > a_{i − 1}a_{i + 2}.
These conditions in interval bounds are simplified into the following form:
Lemma 3.2.2:
The interval polynomial D(s, a) defined in (5) is Hurwitz for all \( {a}_i\in \left[{a}_i^{},{a}_i^{+}\right] \) where i = 0,1,2,3…..n, if the following sufficient conditions are satisfied:
a_{i} > 0and 0.4655a_{i}a_{i + 1} > a_{i − 1}a_{i + 2}.
These conditions in interval bound are simplified into the following form:
Therefore, for order n = 4 the stability conditions for the SMIB power system are given by:
Using these stability conditions the robust PIDPSS controller for the SMIB system under large uncertainty is developed in the following section.
Procedure for designing robust PIDPSS of a SMIB system
Power plants in the real world operate under large uncertainties and robust controllers that can stabilize the plants for all the disturbances under all operating conditions are required. This necessitates the development of a new design procedure for determining a robust PIDPSS for an SMIB power system under large uncertainties. The structure of the PIDPSS considered in this work is shown in Fig. 4. As shown, the function of the washout block is to make the PSS inactive under a steady state condition, sudden rejection of heavy loads or system islanding conditions. The gain of the washout block is almost unity and the phase shift is negligible. The addition of the block results in an increase in the number of constraints due to increase in the order of the system. Hence, in the proposed design procedure, the block is omitted, while it is included when validating the efficacy of the controller.
To accommodate the uncertainties of the plant, P and Q are considered in the present work to vary over a wide range, i.e., P ϵ [P_{min}, P_{max}] and Q ϵ [Q_{min}, Q_{max}] with a certain step size.
Step 1: Obtain the SMIB model in transfer function form. The coefficients of the transfer function (2) are computed using (3) for all the operating conditions to obtain the extreme values of the coefficients, given by:
Step 2: Substitute the above values of coefficients in (2) to obtain the open loop plant transfer function of the SMIB in the interval system given as:
Step 3: Consider the transfer function of the PIDPSS as:
where k_{p}, k_{i} and k_{d} are the proportional, integral and derivative constants of the PID controller, respectively.
Step 4: From Fig. 3, the closed loop transfer function is:
Substituting (13) and (14) into (15), the closed loop transfer function is:
Step 5: From (16), the characteristic equation is given by the following interval polynomial as:
Step 6: Determine the stability constraints by applying the new stability conditions given in (11) to (17) as:
Constraint 1:
Constraint 2:
Constraint 3:
Constraint 4:
Constraint 5:
Step 7: To find the controller parameters that exhibit robust performance over the entire range of operating conditions, an objective function is considered as:
where k_{po}, k_{io} and k_{do} are the PIDPSS controller parameters at the nominal operating point.
Step 8: The FMINCON function in MATLAB [54], which solves constraint nonlinear optimization problems, is used to obtain the robust PIDPSS parameters, i.e., k_{p}, k_{i} and k_{d}, by minimizing the objective function (23) while satisfying the developed five constraints (18)–(22). It starts with an initial guess value and finds the minimum of the defined objective function. An interior point algorithm is used in the present work to obtain the optimal controller parameters. The flow chart that represents the proposed design algorithm for obtaining the robust PIDPSS parameters is shown in Fig. 5.
Validation, simulation results and discussion
Case study I
The plant shown in Fig. 1 with the machine data given in [37] is considered, and P and Q vary within a wide range of operating conditions, i.e., P ϵ [0.2, 1.2] and Q ϵ [− 0.4, 0.4], with a suitable step size to have 1024 mesh points. The extreme values of the coefficients are as follows:
Substituting (24) into (13) obtains the open loop transfer function of the plant without PIDPSS controller as:
To determine the stability of the open loop system, the value of the constant k_{5} is computed for all 1024 operating states and is shown in Fig. 6 using a mesh plot. From Fig. 6, it is observed that the constant k_{5} is negative for some operating points, for example under high active power and leading power factor, the system is relatively more unstable compared to other operating conditions. To illustrate the damping characteristics of the open loop system, the ζ_{min} for all 1024 operating points are calculated and are shown in Fig. 7. For some operating points, ζ_{min} is negative, indicating poor damping characteristics, which can cause the system to become unstable under uncertainties. A robust PIDPSS controller that makes the closed loop system stable for all 1024 operating states is considered as given by (14). From (16), the resulting closed loop transfer function of the plant is:
From (26) the characteristic equation of the closed loop transfer function is:
Applying the new stability conditions in (18)–(22) to (27), the following inequality stability constraints are obtained:
Constraint 1:
Constraint 2:
Constraint 3:
Constraint 4:
Constraint 5:
From (30)–(32), the minimum limits for k_{p}, k_{i} and k_{d} for robust stability can be obtained as:
The newly proposed sufficient conditions given by (28) and (29) can be plotted in MATLAB using ezplot as shown in Fig. 8. The Constraint 1 is plotted for different values of k_{i}, and it can be seen that the stable region decreases with the increase of k_{i} from ‘145’.The minimum limits for gains are obtained using the new necessary conditions while the maximum limits are arbitrarily chosen. The plot shows the stable and unstable regions obtained from the newly developed stability conditions. Also note that there are a set of controller parameters that can stabilize the plant for all 1024 operating conditions.
The plant characteristic equation at the nominal operating point is given by:
From [51] the optimum coefficients of D(s) that minimize the Integral Time Absolute Error (ITAE) for a step input are given by:
Comparing (34) and (35), the controller parameters at the nominal operating point are:
Since the plant normally operates at the nominal operating point the error between the robust controller parameters and controller parameters at the nominal operating point is minimized. The objective function is obtained by substituting (36) into (23) as:
The optimal parameters of PIDPSS are obtained by minimizing (37) subject to satisfying the set of inequality constraints (28)–(32). The proposed method is simulated in MATLAB using FMINCON function to solve the set of nonlinear inequality constraints, and the obtained optimal controller parameters that robustly stabilize the plant for all 1024 operating conditions are:
Validation of relative stability (σ_{max}) and minimum damping ratio (ζ_{min})
The objective of the proposed work is to design a robust PIDPSS that meets the desired closed loop response for uncertainties present in the system. To achieve the desired response, it must have a minimum damping ratio of 0.25 and relative stability ‘σ’, i.e., the maximum real part of the roots, must be less than − 0.3, so that system oscillation would settle within 10–15 s. To illustrate the effectiveness of the proposed controller, the relative stability (σ_{max}) and minimum damping ratio (ζ_{min}) of the closed loop system for all 1024 operating points are computed and are shown in Figs. 9 and 10, respectively.
It is observed that all the closed loop poles lie in the left half of −0.3 and the maximum σ of all 1024 mesh points is σ_{max} = −0.5991. The minimum damping ratio is positive for all 1024 mesh points and ζ_{min} = 0.3438 is achieved with the proposed PIDPSS controller. Hence, the proposed controller exhibits robust stability and performance over the entire range of bounded operating conditions.
The relative stability and damping ratio of the closed loop system for some operating points over the range P ϵ [0.2,1.2] and Q ϵ [− 0.4,0.4] with a step size of 0.2 p.u. are listed in Table 1.
To further validate the robust performance of the proposed controller for other uncertainties such as changes in transmission line reactance due to line outage, machine inertia constant and field time constant, the relative stability σ_{max} and minimum damping ratio ζ_{min} are calculated and are listed in Tables 2, 3 and 4.
Assuming the generator is connected to the infinite bus by a doubleline circuit with equivalent x_{e} = 0.4 Ω, the effect of the transmission line outage can be investigated by considering x_{e} = 0.8 Ω and Table 2 shows the corresponding relative stability and minimum damping ratio.
It can be seen that with the proposed robust PIDPSS, σ_{max} = −0.9677 and ζ_{min} = 0.4150. Hence, the relative stability and minimum damping ratio for all the operating points considered are within the desired values. Therefore, the closed loop response for transmission line outage is satisfactory for P ϵ [0.2, 1.2] and Q ϵ [− 0.4, 0.4].
With ±30% changes in field time constant, Table 3 shows that the proposed robust PIDPSS has satisfactory closed loop response for all the operating states with σ_{max} = −0.5076 and ζ_{min} = 0.2939. From Table 4, it is observed that with ±30% changes in machine inertia constant, σ_{max} = − 0.5956 and ζ_{min} = 0.2873, indicating desired performance by the proposed robust PIDPSS.
Hence, we can conclude that the proposed PIDPSS exhibits robust stabilization and performance for the uncertainties presented in the system, since the proposed PIDPSS parameters are tuned for variations in system coefficients rather than system variables.
Simulation results and discussion
To further test the efficiency of the proposed PIDPSS comparing with the existing controllers in literature, the k constants, i.e., k_{1}k_{6} are calculated for light, nominal, full and overload conditions. Using the MATLABSIMULINK tool box, Fig. 2 is simulated for the above specified operating conditions with T_{W} = 5 and k_{p} = 98.8226, k_{i} = 30, k_{d} = 57.1044. The uncertainty in the system is provided by a small mechanical step disturbance.
Full load operating point
Figure 11 shows the simulation results when the system is operated at P = 1.0 p.u. and Q = 0.4 p.u., and is subjected to a mechanical disturbance of 0.1 p.u. at 0.5 s. It can be observed that without a controller, the plant is unstable to the given disturbance. With the proposed controller, the system is stable and the oscillation in speed deviation is less and reaches the steady state within a shorter time than the existing methods.
Table 5 shows that the proposed controller leads to better time domain specifications and has a better performance than the existing methods. The terminal voltage deviation during disturbance shown in Fig. 12 is within limits and the steadystate error is less than that of the other methods. Hence, the proposed controller exhibits robust performance even when the system is operating at full load and leading power factor at which the damping factor is poor.
Light load operating point
In this case the plant is operated at a light load condition at leading power factor i.e., P = 0.2 p.u. and Q = 0.4 p.u.. At 0.5 s a 0.1 p.u. step mechanical disturbance is applied to the plant. From Fig. 13 without a controller, the plant is stable for uncertainty in the load but the settling time is long and peak overshoot is high. With the PIDPSS in [41] shown in Fig. 14, the settling time and terminal voltage deviations are also very large, whereas with the proposed PIDPSS, the time domain specifications are within acceptable limits. In general, the settling time should be less than 10–15 s for satisfactory dynamic performance. Table 6 shows that the proposed robust PIDPSS has better overall performance than the other methods.
Nominal load operating point
The plant is operated at a lagging power factor and 10% mechanical step disturbance is induced. Figure 15 shows that the peak overshoot is low and the steadystate error in terminal voltage deviation shown in Fig. 16 is almost zero. Table 7 shows that the proposed robust PIDPSS has superior overall performance than the other controllers in literature. Therefore it can be concluded that the proposed controller gives the best performance at this operating point compared to other available controllers in the literature.
Over load operating point
The machine is operated at P = 1.2 p.u. and Q = 0.2 p.u. and is again exposed to a mechanical disturbance of 0.1 p.u.. From Fig. 17, it can be seen that without PSS the disturbance pushes the machine from stable mode to unstable mode. With the addition of PSS in the feedback loop the system regains its stability. With the proposed controller, the peak overshoot of speed deviation is less but the terminal voltage variation is higher when compared to other controllers, as seen from Fig. 18. However, the ΔV_{t} is within acceptable limits. Table 8 shows that the proposed robust PIDPSS has lesser time domain specifications and performance errors than the other notable controllers in literature. Hence, it can be concluded that the proposed PIDPSS gives robust performance over all operating points compared to the existing controllers.
Case study II
The system considered is a real plant, i.e., Barka II power station in Oman. It consists of three steam units each rated at 200MVA and two gas units each rated at 175MVA. The PSS is designed for one of the gas units, while the rest of the plant, i.e., the other 4 units and the Oman grid are represented by a Thevenin’s equivalent impedance and infinite bus. The data is taken from [48], and three operating conditions, i.e., light, nominal and heavy load covering the whole operating region, are considered for design purposes. From these three loading conditions, extreme values of the coefficients are obtained as:
The overall transfer function of the plant with PID –PSS in the closed loop is given by:
From (40) the characteristic equation of the closed loop transfer function is given by the following interval polynomial:
Applying the new stability conditions given by (18)–(22) to (41), the following inequality constraints are obtained:
Constraint 1:
Constraint 2:
Constraint 3:
Constraint 4:
Constraint 5:
The controller parameters are tuned by minimizing the objective function (23) subject to satisfying the above inequalities (42)–(46) using FMINCON in MATLAB to achieve desired damping and settling time at light, nominal and heavy loading conditions. The k_{po}, k_{io} and k_{do} are determined using the procedure described for Case study I. The obtained optimal PIDPSS controller values are:
The system is simulated in MATLABSIMULINK using the HeffronPhiliphs model shown in Fig. 2 for light, nominal and heavy loading conditions. The performance of the proposed PIDPSS is evaluated by subjecting the plant to a 0.1 p.u. mechanical step disturbance for all the three cases. The speed deviation responses of the plant are shown in Figs. 19, 20 and 21. It is observed that even without PSS the system is stable for a 10% mechanical step disturbance but it takes a long time to reach steady state and the peak overshoot is high. The dynamic stability of the plant is improved by the addition of PSS. The settling time is around 4 s with single lead PSS [52], 2.5 s with double lead PSS [52], and 1.3 s with the proposed PIDPSS for all the three operating conditions. Thus, the proposed PIDPSS well damps out system oscillation for the given disturbance under the different loading conditions. In addition, the peak overshoot with single lead PSS is higher than those of the proposed and double lead PSS controllers, while the latter two are similar. It can also be noted that the proposed PIDPSS produces less oscillation than the double lead PSS controller, hence creating fewer shaft fatigue effects. Hence, it is concluded that the proposed PIDPSS provides better dynamic performance for the uncertainties present in the system than the other controllers [52] under all operating conditions.
Conclusion
A simple robust PIDPSS design methodology is proposed to enhance the dynamic stability of an SMIB system for a wide range of operating conditions. The HeffronPilliphs model developed by DeMello and Concordia is used for small signal stability analysis, whereas the SMIB system is represented by a fourth order transfer function in an interval system. The extreme values of the coefficients are computed for a specified range of P and Q, and the computationally simple stability conditions with five inequality constraints are developed for the SMIB interval system. The robust PIDPSS parameters are tuned using FMINCON solver in MATLAB. The performance of the proposed robust PIDPSS is demonstrated with two case studies for different operating conditions. Simulation results show that the proposed robust PIDPSS has superior performance and provides better damping of low frequency oscillation when subjected to a small load disturbance for a wide range of operating conditions, when compared to the available methods in the literature.
Availability of data and materials
Please contact author for data material request.
Abbreviations
 V _{ t } :

Terminal voltage
 E _{ q } ^{’} :

Voltage proportional to direct axis flux linkages
 E _{ q } :

Induced emf proportional to field current
 E _{ fd } :

Generator field voltage
 δ :

Angle between quadrature axis and infinite bus
 M :

Inertia constant = 2H, seconds
 T _{ e } :

Electrical torque
 V :

Infinite bus voltage
 K _{ E } :

Exciter gain constant
 T _{ E } :

Exciter time constant
 \( {x}_d^{\prime } \) :

Generator direct axis transient reactance
 x _{ d. } ,x _{ q } :

Generator direct and quadratureaxis synchronous reactance respectively
 x _{ e } :

External (line) reactance
 ω :

Speed deviation
 T _{ do } ^{’} :

Open circuit direct axis transient time constant
 U :

Control signal (PSS) output
 P, Q :

Real and reactive power, respectively
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Acknowledgements
Dr. Vasu Ganji, Mr. Dasu Butti.
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This work is carried out without the support of any funding agency.
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MRR and ASV conceived the presented idea. MS & ASV formulate the methodology. ASV performed computations and simulate the results on a test system. MRR and MS supervised the findings of the work with constructive suggestions, verified the results and edited the manuscript. The authors read and approved the final manuscript.
Author’s information
A S V Vijaya Lakshmi: The author completed her B. Tech and M. Tech from JNTU Kakinada and pursuing her PhD in JNTU Kakinada. Her research interests include Control aspects of Power Systems and optimization techniques..
Manyala Ramalinga Raju received the Masters degree from REC Warangal and PhD degree from JNTU University, India. Presently working as ViceChancellor, JNT University Kakinada, Kakinada. He has presented many research papers in various national and international conferences and journals. His research interests include energy management, conservation and auditing, distribution generation and IT applications in power utility companies.
Mangipudi Siva Kumar: The author completed his M.E and PhD from Andhra University. He is presently working as Professor in EEE Department, Gudlavalleru Engineering College, Gudlavalleru. He has contributed more than 40 technical papers in various referred journals and conference. He is a life member of ISTE, member of IEEE and IAEng and Fellow of Institution of Engineers. His research interests include model order reduction, interval system analysis, design of PI/PID controllers for Interval systems, sliding mode control and Soft computing Techniques.
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A.S.V, V.L., Manyala, R.R. & Mangipudi, S.K. Design of a robust PIDPSS for an uncertain power system with simplified stability conditions. Prot Control Mod Power Syst 5, 20 (2020). https://doi.org/10.1186/s41601020001659
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DOI: https://doi.org/10.1186/s41601020001659
Keywords
 Low frequency oscillations
 Uncertainty
 Power system stabilizer
 Robust controller
 Interval systems