A Generalized Approach for Harmonics and Unbalanced Current Compensation through Inverter Interfaced Distributed Generator Jing Wang, Dalia D. Konikkara, A. Monti Institute for Automation of Complex Power Systems E. ON Energy Research Centre Aachen, Germany jwang, dkonikkara, amonti@eonerc.rwth-aachen.de Abstract—Harmonics and unbalanced current compensation in the distribution grid has become a major concern due to connections of nonlinear and unbalanced loads and high penetration of renewable energy sources. To tackle this problem, the increasing integration of inverter interfaced distributed generation (DG) may actually be considered able to provide ancillary service for power quality support, if controlled and regulated properly. The challenging part consists of precisely extracting the current to be compensated in a fast dynamics and accurately tracking the compensation reference as close and as fast as possible. Most of the existing control methods are developed for selected harmonics compensation, thus not appropriate for the scenarios with wide range of harmonics due to the increasing implementation complexity. Therefore, this work proposes an approach to compensate harmonics and unbalance in a generalized way aiming to correctly compensate wide range of harmonics with less complexity and computation effort. Simulation and hardware-in-the-loop (HIL) experiment results are provided to validate the proposed approach. extracted and then parallel P+Resonant (PR) controllers are adopted to track the harmonic components. Although desirable results are achieved with this compensation approach, it only suits for selected harmonics and unbalance component thus not suited for compensation of wide band of harmonic frequencies [11]. Therefore, complete compensation techniques are developed in [9][10], which extract the compensation reference current in a generalized way and thus track the reference current in a universal manner. However, some of them, e.g methods based on Current´s Physical Component (CPC) [9], Conservative Power Theory (CPT) [10] have drawbacks, such as long time delay, complex implementation, and large computation effort. Thus, as an alternative reference generation solution of the second group, this work utilizes an advanced PLL which can rapidly and accurately extract the fundamental current component and therefore the compensation reference current. A deadbeat type controller is customized to track the compensation reference current. Keywords—Harmonics and Unbalanced Current Compensation; Distributed Generation (DG); power quality support The main contributions of the paper can be summarized as follows: I. INTRODUCTION Harmonics and unbalanced current compensation in the distribution grid has become a major concern due to connections of nonlinear and unbalanced loads and high penetration of renewable energy sources. To tackle this problem, the increasing integration of inverter interfaced distributed generation (DG) may actually be considered able to provide ancillary service for power quality support, if controlled and regulated properly [1]. The idea of using the inverter interfaced DG to improve the grid current quality is to control the DG unit as a shunt Active Power Filter (APF), where the DG absorbs the harmonic and unbalance current of the nonlinear loads, improving the current quality in the grid with lower total harmonic distortion (THD) [1]. To achieve this goal, the harmonic and unbalance current in the load side must be accurately extracted as current reference and then precisely tracked by a current controller of inverter interfaced DG unit. The challenging part consists of precisely extracting the current to be compensated in a fast dynamics and accurately tracking the compensation reference as close and as fast as possible. Control techniques for grid harmonics and unbalance current compensation may be classified into two groups selective and complete compensation techniques [1][2]. Compensation methods using selective scheme are reported in [1][4], in which the harmonic components are selectively • Proposal of a new control strategy for harmonics and unbalance current compensation, which is more flexible and effective than the selective approach. • Use of an advanced PLL to accurately extract the current reference of harmonic and unbalance components in a general way and with fast dynamics. • Design of a novel current control algorithm for a VSI interfaced DG. First, a digital deadbeat current controller with delay compensation has been designed to achieve high bandwidth current control characteristics. Secondly, the evaluations of the closed-loop performance indicate good tracking performance and robustness against parameter variations with the proposed deadbeat controller. • Implementation, testing of the proposed harmonic and unbalanced current compensation algorithm in hardware-in-the-loop with the OPAL-RT platform, thus proving the practical feasibility. '978-1-4799-5115-4/14/$31.00 ©2014 IEEE' II. CONTROL SCHEME FOR HARMONICS AND UNBALANCED CURRENT COMPENSATION A. Compensation Schemes The basic structure for harmonics and unbalanced current compensation includes two parts: generation of the compensation reference current and current controller for tracking the compensation reference current. In the literature, if a compensation reference current is generated in a selective way, the multiple parallel P+Resonant controller is adopted to selectively track the compensation reference current [1][3][4][5].While a deadbeat type of controller is developed in [9][10] to track the reference in a general way when the complete approach is adopted to generate the compensation reference current. The first scheme (selective reference extraction + selective reference tracking) is developed for selected harmonics and unbalanced compensation, thus not appropriate for the scenarios with wide range of harmonics due to the increasing implementation complexity [1]. Therefore, this work proposes an approach (second scheme) to compensate harmonics and unbalance current in a generalized way aiming to correctly compensate wide range of harmonics with less complexity and computation effort compared to the existing complete compensation techniques. B. Proposed Current Compensation Method The inverter interfaced DG compensates the power quality besides the primary function of fundamental current injection, assuming that the available power rating of the DG is sufficient. DG are distributed generators such as wind turbine, PV, Fuel Cell and battery which forms the DC power supply for the inverter system. When the DG is not operating in full power conditions, the inverter may also operate as an APF to be controlled for power quality support and fundamental current injection. The basic structure of the power quality compensation scheme using Current Control is shown in Fig. 1. The figure includes an inverter interfaced DG unit symbolized using a DG source, a voltage source inverter and an LCL filter. The Grid is represented using grid voltage, grid impedance and signifies the load harmonic and unbalanced loads where current and the PCC voltage. As depicted, the fundamental three phase reference current is obtained from the power control loop in the dq frame and the compensation reference current for complete compensation is generated from the advanced PLL. vs Zg iL io vo io vo i * c i vg vs θ i u* + h i*af i*a * b iL i * bf i * cf i*df i*qf vsf P* Q* Fig. 1. Basic structure of the proposed control scheme. A model-based deadbeat current controller, with predictive compensation is designed to allow the output current of the with accuracy and filter to track the reference current high bandwidth. The filtered fundamental voltage angle information of PCC voltage θ is provided to guarantee the injected fundamental current to synchronize with the grid fundamental voltage. Fig. 4 depicts the information of the LCL filter variables used for control purpose such as and . The following two sections discuss the advanced PLL used and the proposed deadbeat control algorithm. III. ALGORITHM OF THE ADVANCED PLL A. An Overview of Detection Techniques for Extracting the Compensation Harmonic and Unbalance Current Detection techniques for extracting the needed compensation harmonic and unbalance in the existing literature may be classified into two groups: selective detection and complete detection [2]. The first group is only valid for selected harmonics compensation, thus not appropriate for the scenarios with wide range of harmonics due to implementation complexity caused by parallelization of multiple Phase-Lock-Loops (PLL) such as multiple complex-coefficient-filter PLL (MCCF-PLL), secondorder generalized integrator PLL (SOGI-PLL) and decoupled synchronous reference frame PLL (DSRF-PLL) [3][4][5]. Moreover, both MCCF and SOGI-PLL essentially perform resonant filtering which implies possible problems of sensitivity in the magnitude and the phase responses around the resonance points [1]. As explained in [1], the DSRF-PLL uses multiple feedback loops to separate the positive- and negativesequence components thus not appropriate for input harmonics. Resonant filters are used as well to selectively extract the harmonics; however, they introduce a large change of phase angle around the resonance frequencies which results in substantial phase errors in the extracted signals [1]. Adaptive notch filter (ANF) is reported to isolate the selected harmonics [7]; however, the drawbacks such as phase error around the notch frequencies, and the large computational effort for continuously tuning the coefficients of the notch filters limit its application for the purpose of this work. The second group performs complete harmonic extraction and uses various methods based on either time domain or frequency domain or a combination, to generate the compensation reference current from a power theory perspective [6]. Comparison of applicability of these methods depending on goals of compensation as well as on expected system conditions are summarized in [6] which shows to offer very effective and a high degree of flexibility in compensation applications [2]. However, some of them, e.g based on Current´s Physical Component (CPC) [9], Conservative Power Theory (CPT) [10] have drawbacks, such as complex implementation, large computation effort and longtime delay. Thus, as an alternative reference generation solution, the second group utilizes an advanced PLL which can rapidly and accurately extract the fundamental current component and therefore the compensation reference current. The advanced PLL is called Cascaded Delayed Signal Cancellation (CDSC) PLL [8], and is used for fast selective harmonic detection. However, the fundamental component is harmonic in a broad sense, thus the fundamental component can be extracted with CDSC PLL by choosing proper parameters. B. Applied Advanced PLL The CDSC-PLL discussed in [8] is adopted in this paper due to its advantages over the previously mentioned methods. The parameters of CDSC-PLL are properly designed here to extract the fundamental current component and thereafter obtain the reference current containing harmonics and unbalance currents. The method uses a cascaded connection of Delayed Signal Cancellation (DSC) subsystems as shown in Fig. 2. The key idea behind it is the fact that different frequencies in the same portion of time can be separated through delay operation. Let us assume / is the vector delayed by / and lagging by : 2 1 where represents the fundamental period at the fundamental frequency , and represents 2 , and signifies harmonic order and targeted harmonic order which in this case is +1 for fundamental component of current. When we multiply the delayed vector by a chosen rotation angle , it results in a rotated vector which along with the original vector is used to construct the DSC operator as follows. 1 2 e θ 2 1 3 2 2 4 represents the harmonic gain. Using trigonometric identities and equating real and imaginary parts of (3) the following equations can be obtained. |cos /2| Fig. 2. Basic structure of CDSC-PLL. Using this method, unwanted harmonics can be eliminated, thus obtaining the fundamental component. Though it sounds as a selective harmonic elimination method, studies show that the PLL leads to automatic elimination of harmonics other than the selected ones when appropriate parameters (h=+3,+5,+9 and h*=1) are chosen. The rules to choose the parameters are summarized as follows: 1) fix the targeted order harmonic, and then to choose the first unwanted harmonic and obtain the magnitude representation diagram of the first DSC operator as the top one shown in Fig. 3; 2) choose the second unwanted harmonic (gain equals to 1 in the first DSC operator) and get the magnitude representation diagram, and then pick the third unwanted harmonic (gain equals to 1 in the first and the second DSC operators); 3) make the cascaded CDS operators and get the complete magnitude representation diagram and check if the unwanted harmonics are cancelled; 4) if not, repeat the step 3. It is worth pointing out that the advantage of this method is that the number of CDSC subsystems equals to the number of harmonics to be detected. Whereas in SOGI-PLL or DSRF-PLL, the number of SOGI/DSRF subsystems equals the number of harmonics present. Therefore to extract only the fundamental components, SOGI/DSRF needs multiple subsystems, while only one CDSC subsystem is required. A single CDSC-PLL module is enough to extract the fundamental component and thus significantly reduces the implementation complexity and computation effort. 5 (6) In order to eliminate unwanted harmonics , the gain must be zero for all cases other than for which the gain is unity. Substituting 0 in (5), 2 can be obtained. 3, 5, 9 and 1, then 4, 8 and 16 Consider respectively. Fig. 3 shows the magnitude representation of the DSC operators and the CDSC-PLL. The first three plots show the DSC operators for 4, 8 and 16 respectively. The last part in the plot shows the cascaded operation of the three DSC operators for fundamental current component extraction. For the first DSC operator, harmonics such as +1, 3, +5 (gain equal to 1) are retained and harmonics such as +3, +7 (gain equal to 0) are eliminated. The same principle holds for the second and third DSC operators. The highlight in this approach is, by trying to get rid of +3, +5 and +9 harmonics, we can get rid of ±3, ±5, ±7, ±9, ±11and other higher order harmonics (-1, -12, 13…). Even the magnitudes at the even order and interharmonics (e.g 2.5th harmonic) may not be zero; they are attenuated to a negligible amount [8]. Thus by properly choosing h and h*, wide band of harmonics can be eliminated. Fig. 2 shows the basic structure of a CDSC-PLL with three DSC operators corresponding to n=4, 8 and 16. The extracted fundamental component is then used to obtain the as shown in the unbalance and harmonic component Figure 2. Fig. 3. Diagrammatical magnitude representation of DSC and CDSC. As seen in Fig. 2, the extracted fundamental component is located by locking the zero-crossing point of the fundamental component of the current , which indicates that there is no phase shift (error) in the extracted fundamental component. Therefore, using CDSC-PLL will not cause phase error to the extracted harmonics and unbalance component like resonance filter or notch filter does. IV. AN OVERVIEW OF THE CONTROL ALGORITHM FOR POWER QUALITY IMPROVEMENT A. Types of Current Controller The main aim of a current controller of an inverterinterfaced DG is to provide accurate current tracking for the reference current as fast and as close as possible. There are different types of current controllers which have one advantage over the other. The comparisons among them are summarized in Table I. TABLE I. TYPES OF CONTROLLERS Type of control Stationary PR control Advantages Zero phase error Synchronous PR/PI control No phase lag Hysteresis control Fast transient response Fast transient response Deadbeat control Disadvantages Slow transient response; poor compensation of high order harmonics; complex tuning process Slow transient response; nondefined robustness; poor compensation of high order harmonics Unpredictable low order harmonics Delay limits the bandwidth of controller; sensitivities to plant uncertainty As the compensating reference current contains harmonics at frequencies much higher than the fundamental one, conventional current approaches (PR or PI controller) fail to reach control goals such as minimization of the phase and amplitude errors of reference tracking and fast dynamic response [11]. Harmonics control by using parallel PR controller is limited to the selected harmonics reference in the chosen number and order, which is not appropriate for tracking a reference with wide band of frequencies and without knowing the number and order of the harmonics. In addition, higherorder harmonic tracking should be avoided with the multiresonance controller due to the limited bandwidth (higher than 13th) [1]. Hysteresis current controller has non-constant switching frequency as main drawback. Due to this fact, the spectrum of controlled current may contain various harmonics that are hardly predictable. To overcome all these limitations, a deadbeat type of controller featuring accurate refined tracking, high bandwidth and less complexity is proposed for harmonic compensation control. B. Proposed Deadbeat Control The basic idea of the proposed deadbeat controller is to use the desired output to generate the desired control input based on the controlled plant (inverter and LCL filter) shown in Fig. 4. implementation complexity without losing the accuracy of the controlled plant. Meanwhile, it involves less plant parameters which results in less sensitivity to plant parameter variations. The well-known two-step delay caused by the computation of the control algorithm and the PWM modulation are included, thus the plant equations can be given as follows: 1 represents the two-step delay. Using Euler where Backward integration method, the discretized system can be described as: 8 where 1 9 is the discretization time. Based on the above equation, the control law can be formulated as follows: 2 1 2 10 If only one-step-ahead prediction is carried out to test the proposed control scheme and the compensation effect, the one1 and voltage 1 are step-ahead reference current obtained using linear prediction as described in [11]. 1 3 3 1 1 2 2 11 1 12 Two-step-ahead prediction of the reference current and the voltage , and one-step-ahead prediction of the output current are needed to compute the desired control input . A prediction algorithm which estimates future variables such as reference current and the measured current and voltage has to be developed. Taking into account the different characteristics of the estimated variables, specific prediction method should be applied to predict or estimate each of the future variables [11][13]. The output voltage is a slow and periodic varying signal therefore the prediction of the voltage at the next time step 1 can be done by using first-order linear extrapolation method. The prediction is based on available measured voltage value at the time step k and the history sampling values, and it can be formulated as in (12). The voltage at the time step 2 can be derived directly based on (12): 2 3 2 1 13 1 affects not only the The prediction algorithm of accuracy of prediction but also the stability of the entire system. The estimation of the measured current is calculated based on the system model due to the fact that the output current has faster dynamic features compared to the voltage and it is determined mainly by the system model. Therefore, 1 is the prediction law for the current at the time step proposed based on the real plant shown in (7). The prediction law can be characterized as follows. Fig. 4. Structure of one phase of the LCL filter. In this work, the desired control input is generated is the based on LC filter rather than LCL. In this case, control input and is the disturbance input, and is the output. As we have , substituting this equation into (7), we can observe that generating the control input using LC filter model is equivalent as using LCL filter model. To put it another way, the LC model still contains the information of the LCL filter model. Essentially, this way of modeling reduces the system to second order thus reducing the 7 1 where 1 , , 2 , 1 14 . The reference current is stochastic and unknown, and depends on the characteristics of the nonlinear load in the utility grid. This feature makes the prediction of the reference current difficult and more sophisticated algorithm should be developed to accurately estimate the current especially when there is a sudden change in the reference current. However, more sophisticated prediction/estimation algorithm may need large computation effort which gives problem of undesirable delay [11]. The polynomial extrapolation method is reported in [11][13] and has been proven to be an effective solution considering accuracy and computation burden. Therefore, this method is adopted in this work and a fourth-order two-stepahead extrapolation method is applied to guarantee the estimation accuracy and not much computation effort, therefore resulting in the following prediction formula: 2 1 2 Z −2 i* (k + 2) ∑ The optimization of the coefficients is part of the training of the ANN, and the forecasted two-step-ahead reference current will be the output. The whole training process must be much faster than the control step (sampling step). This can be satisfied due to the memory function of ANN during training, then the optimized coefficients will be the same as long as no sudden change in the reference current. If the output error is over a tolerance then it is detected as a sudden reference is used for change, therefore, the reference current value 2 . The results of the estimated the predicted value reference current and the estimation error are presented in Fig. 6, which shows the forecasted current is exactly two steps ahead the present value and the estimation error is small. Current (A) 2 ⁄ 17 where estimated io*(k+2) present io*(k) 10 2 sampling steps 1.005 1.01 1.015 1.02 1 1.005 1.01 Time (s) 1.015 1.02 20 1 21 ⁄ 22 For good steady-state performance, that is, response in finite settling time, the poles must be moved to the origin and the final value theorem should be fulfilled for step response [12]. Thus, |G(z)|z=1=1 has to be fulfilled. Further deriving the shows that the poles are in the origin transfer function zero steady-state error. This condition is verified by the fact that the magnitude of the transfer function is zero by 1. substituting 10 0 -10 -20 -30 -40 -50 -60 -70 -80 1 10 2 10 Frequency (Hz) 3 10 Fig. 7. Bode diagram of the gain of the disturbance input (io(k)/vo(k)) The disturbance term results in an instantaneous tracking error which is caused by the prediction errors of the voltage 1 , 2 and 1 . For a sampling frequency of 5 kHz and for an operating frequency of 50 Hz, the error of 1 is 0.394% and linear prediction for one-step-ahead 2 is 1.18%. The gain of the lumped for two-step-ahead 0 1 19 1 the magnitude of the transfer function is 1. and at is a disturbance for the closed-loop system, the As transfer function should be zero for accurate tracking and e(k ) Fig. 5. The proposed current reference predictor using ANN. Estimation error (A) ⁄ Magnitude (dB) Z0 Z −1 Z −1 Z −1 Z −1 0.2 0 tracking error is indicated by the transfer function -0.2 ANALYSIS OF THE PROPOSED DEADBEAT CONTROL A. Control Performance Analysis Based on the prediction methods, the following control law is obtained: 2 1 (16) 2 , 2 3 . The bode diagram is shown in Fig. 7 which denotes that the tracking error is small considering the possible harmonic components in the capacitance voltage. Fig. 6. Results of the estimated two-step-ahead reference current. where The transfer function of the discretized closed-loop current control is derived based on the plant (7) and the updated control law (16), which can be written as 18 i* (k ) V. . 15 where a, b, c, d and e are the coefficients to be optimized by artificial neural network (ANN) which provides advantages including very fast computation speed, adaptability to changing parameters or even plant structure and high noise immunity [13]. The proposed current reference predictor using ANN is presented in Fig. 5 which is a three-layered back propagation network consisting of 5 inputs, 3 nodes in hidden layer and one output. -0.4 2 3 4 -10 1 , B. Robustness Analysis Robustness to the variations of the plant parameters is an important issue of the proposed deadbeat control since the control law is obtained based on the plant model. As the main variations of the plant parameters come from the inductance and capacitance , robustness of the proposed controller is investigated regarding to the variations of these two parameters. If and are defined as parameters of the real 24 where 1 25 2 2 3 26 2 3 27 2 2 28 The magnitude Bode plot of the gain is used to evaluate the tracking performance of the controller with variation of the and . Fig. 8 shows that the curve of variations of (80% and 120%) overlaps with the case with perfect matched parameters, which denotes that the variation of has minor influences on tracking performance of the deadbeat controller compared to the perfect matched parameters. Variations of have larger impact as shown in Fig. 8, while it is still within the acceptable limits. It is worth to note that ±20% variation is large considering inductance and capacitance can be produced to have variation less than ±10% in practice [12]. Thus, the tracking performance is degraded slightly with the mismatched parameters. A. Extraction of the Compensation Reference Current (Simulation) The load harmonics and unbalance currents are extracted using the CDSC-PLL. The significantly distorted load side current, the extracted fundamental current and the compensation reference current are shown in Fig. 9. Fig. 9 shows that the advanced PLL can extract the fundamental current within a short period (less than 0.01s) and good transients as well. The FFT analysis presented in Fig. 9 shows that the THD of the extracted fundamental current is 0.03% while the original distorted current has THD value of 36.7%, which implies the accurate extraction of the unbalance and harmonic components from the distorted current thanks to the CDSC theory. 40 20 0 -20 -40 0 20 0.01 0.02 0.03 0.04 0.05 0.06 0.07 0.08 0.09 0.1 0.01 0.02 0.03 0.04 0.05 0.06 0.07 0.08 0.09 0.1 0.01 0.02 0.03 0.04 0.05 Time (s) 0.06 0.07 0.08 0.09 0.1 0 -20 0 20 0 -20 0 Fig. 9. Extraction of compensation reference current. 16 THD=36.70% THD=0.03% 14 Mag (% of Fundamental) 23 Load Current (A) 0 From the above equation, we can notice that only the variation of has impact on the stability of the closed-loop system. There are two roots, one is at origin, and the other is equal to / . The absolute value of the second root is always smaller than 1 within the variation range of 10%~200% of which means the stability is ensured. In and have no impact to the conclusion, variations of stability of the controlled system. The effect of parameters variations on the transient performance which is determined by the gain of the disturbance input is investigated, and the transfer function is formulated as following. and further validation is carried out on a HIL OPAL-RT platform. The system parameters used in simulation and experiment are listed in the Appendix. Harmonic & Fundamental Unbalance Current (A) Current (A) plant, and are the estimated parameters for the control algorithm. The characteristic equation of the closed-loop system is rewritten and given as follows. 12 10 8 6 4 2 0 0 2 4 6 8 10 Harmonic Order 12 14 16 Fig. 10. FFT analysis of load and extracted fundamental current. B. Harmonic and Unbalanced Current Compensation (Simulation) 10 Iabc Grid Current (A) 0 -20 -30 10 0 -10 -20 0 80% Cf,Lf Cf, Lf Cf, 80% Lf Cf,120% Lf 120% Cf,Lf -40 -50 -60 -70 -80 1 10 2 10 Frequency (Hz) 10 3 Fig. 8. Bode diagram of the gain of the disturbance input (io(k)/vo(k) under parameters variations. VI. RESULTS AND DISCUSSION The validation of the proposed control scheme includes two parts: extraction of the compensation reference current and harmonic and unbalanced current compensation with the designed deadbeat current control. The simulation is implemented and tested in real-time on an OPAL-RT platform, 0.02 0.04 0.06 0.08 0.1 0.12 0.08 0.1 0.12 Ioabc 10 Inverter injected Current (A) Magnitude (dB) -10 20 5 0 -5 -10 0 0.02 0.04 0.06 Time (s) Fig. 11. Grid and inverter injected current for unbalance compensation In this simulation scenario, the grid current is unbalanced due to the connection of an unbalanced load, and the DG is connected to the main grid at 0.045s. The results are shown in Fig. 11, which depicts that the unbalance in the grid caused by the load is well compensated by the grid connected inverterinterfaced DG, which is connected at 0.045s. In this simulation scenario, the grid current is severely distorted by harmonic and unbalance currents and the DG is connected to the main grid at 0.045s. The simulation results of the proposed deadbeat control with two-step-ahead prediction are provided for comparison. Grid Current(A) As shown in Fig. 12, using two-step-ahead prediction, the grid current distortion is well compensated thanks to the good tracking performance of the proposed deadbeat control. And the THD value of the grid current as shown in Fig. 13 is significantly reduced from 36.7% to 2.00% and within the acceptable limit as per IEEE standard 519. The reference tracking performance of the deadbeat controller in phase A is presented in Fig. 12: it shows that the proposed deadbeat controller tracks the reference current with slight tracking error and delay but good and acceptable accuracy as demonstrated by the THD of the compensated grid current. 50 0 -50 0 Reference & Injection Current(A) Fig. 14. Experimental results of extraction of compensation reference current (blue: grid current, red:fundamental current, pink: harmonics and unbalance). 0.01 0.02 0.03 0.04 0.05 0.06 0.07 0.08 30 0.09 0.1 Reference Current 20 Injection Current 10 0 -10 -20 0.1 0.11 0.12 0.13 Time(s) 0.14 0.15 0.16 Fig. 12. Grid current (top), injected current and refernce current of phase A(bottom). 16 THD=36.70% THD=2.00% Mag (% of Fundamental) 14 12 10 8 6 4 2 0 0 2 4 6 8 10 Harmonic Order 12 14 16 Fig. 13. FFT analysis of grid current before and after compensation. C. Hardware-in-the-loop Experimental Verification In order to validate the practical application of the proposed compensation approach, a signal level HIL experimental verification is carried out in OPAL-RT platform. In this HIL platform, the power system and inverter models run in CPU, the measurements (voltage and current) are sent to the controller under test. A Field-Programmable Gate Array (FPGA) is applied to implement the CDSC-PLL algorithm to generate the compensation reference current, to calculate the fundamental reference current and the deadbeat control algorithm.The voltage reference for the inverter is sent back to the CPU to generate the PWM for the inverter. The optimized coefficients of ANN are directly applied in the reference current prediction, thus no ANN algorithm is programmed in FPGA. The experimental parameters are listed in the Appendix, and the results are shown in Figure 14-16. Fig. 15. Grid current before and after compensation (blue), reference current (red), inverter injected curent (pink) and switching signal of DG (green). The extraction of the compensation reference current shown in Fig. 14 further validates that the CDSC-PLL can extract the compensation reference current accurately. The THD value (0.12%) is slightly larger than the simulation results due to the problems in the practical implementation such as delay and data conversion error in data transmission between CPU and FPGA, data resolution and timing-delay of digital implementation in FPGA. Fig. 16 shows the experimental result of the grid current before (unbalanced) and after compensation. It proves that the proposed control method can compensate the grid unbalance current very well. The experimental results of the grid current before (unbalanced and harmonics) and after compensation are shown in Fig. 15 which indicates that the grid current is well compensated in a fast dynamics. The comparison between the injected inverter current and the reference current shows that there is a tracking error in the more distorted area in the compensation reference current, while in the non-distorted area the injected current tracks the reference current perfectly. The THD of the grid current after compensation is 2.54%, which is acceptable as per IEEE standard 519. Fig. 16. Grid current before (unbalanced) and after compensation. The experimental results clearly show that the proposed approach can compensate the harmonic and unbalance current with excellent performance. D. Discussion The CDSC-PLL can be used to extract the fundamental current component accurately if the parameters of CDSC-PLL are properly designed. However, sub-harmonics (e.g 2.5 order) cannot completely be cancelled but only attenuated to some extent, which results in tracking error for the compensation reference current. This can be considered the limitation of this method. The other limiting factors for the inverter-interfaced DG to compensate the harmonics and unbalance in the grid current are the power rating of the DG and the tracking accuracy of the deadbeat controller. The simulation result shows that the errors in the two-step-ahead prediction 1 and output 2 , output current (reference current 2 and 1 ) cause tracking error (it is voltage acceptable from the results) with the proposed deadbeat controller. In addition, the non-ideality in the practical implementation such as delay in data transmission, error in data conversion, and data resolution in digital computation cause tracking error as well. However, the compensation effects are satisfactory as seen from the simulation and experimental results, and the simplicity of implementation and effectiveness shows the proposed method is a good solution for grid harmonics and unbalance current compensation. VII. CONCLUSION This work presents a generalized approach for harmonics and unbalance current compensation through inverter interfaced DG. The proposed control scheme is composed of an advanced PLL and a deadbeat current controller. Compared to the commonly used SOGI and DSRF PLL, the adopted advanced PLL can extract the compensation reference current more accurately and rapidly, and the implantation and computation effort of the PLL is much reduced. The proposed predictive deadbeat controller has accurate reference tracking performance for a wide band of frequencies with fast dynamics and less implementation complexity. The simulation and experimental results show that the proposed compensation scheme of DG can improve the power quality (current) with fast dynamics, satisfactory accuracy and good transient behavior. Therefore the proposed control scheme is validated to be an effective solution for unbalanced harmonics current compensation. 0.4mH, power reference 200μs, DC link voltage 0 var, REFERENCES [1] [2] [3] [4] [5] [6] [7] [8] [9] [10] [11] [12] APPENDIX Supply: Nominal grid line-line voltage at the PCC=400V at 50 Hz; Inverter: 0.15Ω, 1.8mH, 30μF, 0.1Ω, 2 kW, 750 V. [13] J. H, Y. W. Li, Md. Munir, “A Flexible Harmonic Control Approach Through Voltage-Controlled DG-Grid Interfacing Converters,” in IEEE Trans. On Ind. Electronics, vol. 59, no. 1, pp: 444-455, Jan. 2012. Y. Wang and Y. W. Li, “An Overview of Grid Fundamental and Harmonic Components Detection Methods,” in Conf. Rec. IEEE Energy Conversion Congress and Exposition (ECCE’ 13), Denver, USA, 2013. P. Rodriguez, “Grid Synchronization of Power Converters Using Multiple Second Order Generalized Generators,” in 34thAnnual Conf. of IEEE IECON, pp. 755-160, Nov. 2008. J. Rocabert, “Control of Power Converters in AC Microgrids,” IEEE Trans. on Power Electronics, vol. 27, pp. 4734-4749, Nov. 2012. P. Rodriguez, “New Positive Sequence Voltage Detector for Grid Synchronization of Power Converters under Faulty Grid Condition,” in 37th IEEE PESC, pp. 1-7, Jun. 2006. Herbert L. Ginn, “Comparison of Applicability of Power Theories to Switching Compensator Control,” International School of Nonsinusoida Currents and Compensation, June, 20-21, 2013, Zielona Góra, Poland. M. Mojiri, M. Ghartemani and A. Bahkshai, “Procesing of Harmnics and Interharmonics Using an Adaptive Notch Filter,” IEEE Power Del., vol. 25, no. 2, pp: 534-542, Apri, 2010. Y. F. Wang, “Three-phase cascaded delayed signal cancellation PLL for fast selective compensation,” in IEEE Transaction on Industrial Electronics, pp. 1452-1459, Apr. 2013. H. L. Ginn, “Flexible Active Compensator Control for Variable Compensation Objectives,” in IEEE Tran. on Power Elecctronics, vol. 23, pp: 2931-2940, Nov, 2008. P. Tenti, “Conservative Power Theroy, A Framework to Approach Control and Accountability Issue in Smart Grid,” in IEEE Tran. on Power Electronics, pp: 664-668, Mar. 2011. M. Odavic, P. Zanchetta, M. Sumner, “A Genetic Algorithm Design Method for A Current Controller Employing “Two Ahead” Prediction,” IEEE International Conference on Industrial Technology, ICIT 2006, Dec., 15-17, 2006, Mumbai, India. H. Deng, R. Oruganti, D. Srinivasan, “A Simple Control Method for High-Performance UPS Inverters Through Output Impedance Reduction,” IEEE Trans. on Ind. Electronics, vol. 55, no. 2, pp: 888-898, Feb. 2008. F. Kamran, T. G. Habetler, “An Improved Deadbeat Rectifier Regulator Using a Neural Net Predictor,” IEEE Tran. on Power Electronics, vol. 10, no. 4, pp. 504-510, July, 1995.