https://doi.org/10.6113/JPE.2019.19.2.333

ISSN(Print): 1598-2092 / ISSN(Online): 2093-4718

A Novel Method for Compensating Phase Voltage Based on Online Calculating Compensation Time

Mingyu Wang^*, Dafang Wang^†, Chuanwei Zhou^**, Xiu Liang^*, and Guanglin Dong^*

^†,*College of Automotive Engineering, Harbin Institute of Technology, Weihai, China

^**Integrated Project Management, Beijing Benz Automotive Co. Ltd., Beijing, China

Abstract

Dead time and the nonideal characteristics of components all lead to phase voltage distortions. In order to eliminate the harmful effects caused by distortion, numerous methods have been proposed. The efficacy of a method mainly depends on two factors, the compensation voltage amplitude and the phase current polarity. Theoretical derivations and experiments are given to explain that both of these key factors can be deduced from the compensation time, which is defined as the error time between the ideal phase voltage duration and the actual phase voltage duration in one Pulse Width Modulation (PWM) period. Based on this regularity, a novel method for compensating phase voltage has been proposed. A simple circuit is constructed to realize the real-time feedback of the phase voltage. Utilizing the actual phase voltage, the compensation time is calculated online. Then the compensation voltage is derived. Simulation and experimental results show the feasibility and effectivity of the proposed method. They also show that the error voltage is decreased and that the waveform is improved.

Key words: Compensation time, Dead time, Nonideal characteristics of components, Real-time feedback on phase voltage

Manuscript received Mar. 23, 2018; accepted Nov. 23, 2018

Recommended for publication by Associate Editor Younghoon Cho.

^†Corresponding Author: wdflcjl@163.com Tel: +86-138-6300-9863, Fax: +86-631-5687212, HIT (Weihai)

^* College of Automotive Eng., Harbin Inst. Tech. (Weihai), China

^** Integrated Project Mgmt., Beijing Benz Automotive Co. Ltd., China

Ⅰ. INTRODUCTION

The phase voltage produced by a Voltage Source Inverter (VSI) cannot always be measured directly. When this occurs, the actual phase voltage is often replaced by the command phase voltage. However, due to the dead time effect and the nonideal characteristics of components [1], [2], there is a distinct error between the actual phase voltage and the command phase voltage which may result in current distortion and torque ripples. Thus, it is necessary to compensate the error of the phase voltage.

Numerous methods have been studied and proposed to alleviate the distortion of phase voltage. Most of these methods can be sorted into two types, methods based on model observation [3]-[5] and methods based on mechanism analysis [6]-[8].

Methods based on model observation estimate the error voltage caused by the dead-time effect and the nonideal characteristics of components through adopting motor models or observers. In [9], a simple vectorial disturbance estimator is established by transforming the phase voltage, phase current and rotor position. In [10], the sixth harmonic of the integrator output of a synchronous d-axis proportional integral (PI) current regulator is used to compensate output voltage distortion. Usually, the calculation costs of methods based on model observation are fairly high.

Methods based on mechanism analysis quantitively and theoretically analyze and evaluate dead-time effect. The error voltage is drawn by the volt-second principle of PWM. The efficacy of such method depends on amplitude of compensation voltage and the polarity of phase current. The compensation voltage amplitude can be obtained by off-line pointing and on-line testing [11]. With regard to the current polarity, direct A/D sample is used in many papers [12]. However, the accuracy is usually very low because of Direct Current (DC) drift of sensors and high frequency noise. Since the current polarity determines compensation accuracy, the wrong detection results can make the situation worse [13]. In [14], a hardware circuit is applied to detect the current of the freewheeling diode. In [15], [16], terminal voltage of diode is used to judge current polarity, however, the power supply is complex which may increase costs. The current predictive control in [17] can judge the polarity of current. However, in this method, precise machine parameters are needed.

In this paper, the cause and effect of the error voltage is analyzed, and the change rules of the compensation voltage are determined. Consistency between the compensation time and the phase current is found. On the basis of this new discovery, a novel method for compensating phase voltage is proposed. A simple hardware circuit is designed to realize the real-time feedback of VSI output. Then the compensation time is calculated according to the output. The compensation voltage amplitude and the phase current polarity are both derived from the compensation time. Then the compensation voltage is determined. Simulation and experimental results are presented to verify the effectiveness of the proposed method.

Ⅱ. ANALYSIS OF PHASE VOLTAGE DISTORTION

A. Distortion Analysis

In reality, due to the nonideal characteristics of components and the parasitic capacitors of switching devices, voltage changes are not instantaneous. They act as a slope process which is plotted in the heavy line in Fig. 1. For the sake of convenience, the actual slope process can be equivalent to a step process which is plotted in the dashed line in Fig. 1. The transformation process is as follows. Taking U_BAT/2 as the vertex, shadowed triangles are plotted. Obviously, the upper triangle and the lower triangle have the same area. If the lower triangle is rotated around the U_BAT/2 vertex, the lower triangle overlaps with the upper triangle and an equivalent pulse width is made.

Fig. 1. Slope process of voltage change and the equivalent step process.

One arm (phase A) from a VSI is taken as an example to analyze the distortion. Fig. 2 shows the waveform applied to a gate electrode in one PWM period after inserting dead time. Fig. 3 shows the one arm condition when i_A>0. The power devices are Insulated Gate Bipolar Transistors (IGBTs). Thus, the current can only flow in one direction.

Fig. 2. Waveform applied to a gate electrode.

Fig. 3. One arm condition when i_A>0.

Analyzing Fig. 2 and Fig. 3, the condition of i_A >0 is discussed here. In the ‘a’ period of Fig. 2, Q_L is turned on. Since the IGBT can only conduct in one direction, the current flows through D_L, and the potential of the output terminal is (-U_BAT/2-U_D), where U_D is the voltage drop of the freewheeling diode. In the ‘b’ period, Q_L and Q_H are both turned off. In this case, the power devices of phase A operate in dead time, and potential of the output terminal is still (-U_BAT/2-U_D). In the ‘c’ period, Q_H is turned on and the current flows through Q_H. Hence, the potential of the output terminal is (U_BAT/2-U_F), where U_F represents the forward voltage drop of the IGBT. In the ‘d’ period, Q_H and Q_L are both turned off, and the power devices are working in the other dead time. Thus, the potential of the output terminal is (-U_BAT/2-U_D), which is the same as the ‘b’ period. The condition of i_A <0 is similar to the condition of i_A >0. Therefore, it will not be covered here. It can be concluded that the amplitude and phase of the terminal voltage are both distorted.

The authors of [18] deduced the phase voltage distortion in detail. Fig. 4 shows the whole process of how the phase voltage gets distorted. Take phase A as an example. In Fig. 4, T_d is the inserting dead time; T_ton and T_toff are the total turn on delay and turn off delay of the gate drive circuits; T_von is the delay between the gate rising edge and the phase voltage changes, while T_voff defines the delay between the gate falling edge and the phase voltage changes. To be sure, T_von and T_voff both contain two stages.

Fig. 4. Waveform distortion process when i_A >0 and i_A <0. (a) i_A >0. (b) i_A <0.

(a)

(b)

Fig. 5 shows the two stages of T_von and T_voff in different current polarities. In Fig. 5, V_GE is the switch signals applied to an IGBT gate electrode. Usually, the power devices used in the upper and lower bridge are identical. Therefore, their time-delay characteristics are the same. Taking Fig. 5(a) i_A >0 as example, T_von includes two parts. The first part is the device turns on delay, which is the delay time from the rising edge of gate electrode to the breakover of the IGBT. The second part is the delay of the rise time, which is the delay of the charging time of the parasitic capacitor. T_voff also includes two parts. The first part is the device turn off delay, which is the delay time from the falling edge of the gate electrode to the shut of the IGBT. The second part is the delay of the fall time. Since the turn on (off) delay is mainly decided by the gate drive circuits, the turn on (off) delay varies little under different conditions. The rise (fall) time is the main factor affecting T_von and T_voff. Fig. 5(b) i_A <0 is similar to Fig. 5(a) i_A >0.

Fig. 5. T_von and T_voff in two current polarity. (a) i_A>0. (b) i_A<0.

(a)

(b)

B. Distortion Theory

The distortion process is as follows. ① Inserting dead time changes the PWM^Ideal to PWM^DT. ② Due to the non-ideal characteristics of the parts in the gate drive circuits, the PWM^DT changes to PWM^DT+TR. PWM^DT+TR is the exact signal applied to the IGBT gate electrode. In Fig. 4, U* is the corresponding phase voltage to the outcome of SVPWM. In addition, U^Ideal is the ideal output of the VSI, and U^Actual is the actual output of the VSI. As a result, ΔU=U^Ideal-U^Actual is the error voltage. Obviously, the error voltage ΔU is the exact compensation voltage.

In Fig. 4, the expression of the compensation voltage (i_A >0) can be derived using the average value principle of PWM:

       (1)

where is the compensation time for i_A >0. It can be written as (2).

                 (2)

and are defined as (3) which are total delay time.

          (3)

          (4)

Similarly, the compensation voltage and compensation time for i_A <0 can be written in (5) and (6).

   (5)

         (6)

In (1) and (5), the command voltage U* varies from 0 to U_BAT. For the sake of convenience, replace U* with , and the range of is -U_BAT /2 ~ U_BAT /2. With the definition of T_c and sgn(i_A) as (7) and (8), the compensation voltage can be described as (9).

                  (7)

                 (8)

 (9)

Ⅲ. PROPOSED COMPENSATION METHOD

From (9), the amplitude of the compensation voltage is decided by T_c, T_PWM, U_BAT, U_D, U_F and . Among all of the parameters, , U_BAT, and T_PWM are the easiest to obtain. U_D and U_F can either be obtained online or composed a look-up table offline. From (9), T_c is the key factor that affects the amplitude of the compensation voltage. However, T_c is hard to obtain. From (4) and (6), the parameters that affect T_c are T_d, T_ton, T_toff, T_von and T_voff. Among them, T_d is given by a program. T_ton and T_toff are the total delay of the gate drive circuits. Since the circuits work in a simple condition where the power of the circuits is approximately constant, T_ton and T_toff can be considered as constants. However, it is difficult to get the accurate values of T_von, T_voff by the off-line or prediction method. Aiming at obtaining an accurate compensation time T_c, this paper proposed a method that calculates T_c by utilizing online real-time feedback on the rectangular wave of the phase voltage. Fig. 5 illustrates that the compensation time T_c is equal to the high-level duration of U^Ideal minus the high-level duration of U^Actual. Thus, once the high-level duration of U^Actual is measured T_c can be calculated.

Equation (9) implies that the compensation time is mainly affected by the current polarity. Methods using A/D converters to get current in many papers are sensitive to noise. Moreover, a phase shift will be introduced when using filters, therefore, results in judgments are far from accurate. In this paper, the consistency between the compensation time T_c and the phase current is found. With this regularity, the current polarity can be judged by the sign of the compensation time T_c.

A. Derivation of Rise Time T_r and Fall Time T_f

As shown in Fig. 6, the rise time T_r (fall time T_f) is the main factor affecting T_von and T_voff. To verify the consistency between the current polarity and the sign of the compensation time T_c, the relationship between T_r (T_f) and the current should be derived. The derivation is based on the charging (discharging) time model of the parasitic capacitor.

Fig. 6. Analysis of waveform distortions.

The terminal voltage v linearly rises after the turn off of the lower switch when i_r is negative, as given by:

                   (10)

where C_p is the parasitic capacitance of one arm.

In Fig. 6, the rising edge of PWM^DT+TR+Tdon represents the actual turn on moment of the upper switch, so does PWM^DT+TR+Tdoff. The transmit delay T_ton and T_toff of the two gate drive signals are considered to be the same. In addition, taking into consideration the difference between the turn on delay T_don and the turn off delay T_doff, the timespan between these two moments is derived as T_d + T_don - T_doff. When i_r is equal to a critical value I_c, the terminal voltage reaches U_BAT at the end of T_d + T_don - T_doff. In addition, I_c can be deduced as (11) according to (10).

                (11)

Fig. 7 shows the variation trend of the terminal voltage v at different currents i_r. The dotted line in the figure sets as the equivalent rising time. Suppose the rising edge of terminal voltage is an ideal step signal, and the average value of terminal voltage in a PWM period remains the same after the equivalent processing. The equivalent rising edge represents the actual step moment of the terminal voltage. The blue shaded space and the red shaded space have the same area. According to this rule, the rise time T_r at different values of i_r is derived in (12).

Fig. 7. Variation trends of the terminal voltage v and rise time T_r at different currents. (a) i_r <−I_c. (b) i_r = −I_c. (c) −I_c < i_r < 0. (d) i_r > 0.

     (12)

The fall time T_f at different currents is derived as given by expression (13).

      (13)

When i_f is negative and the upper switch is turned on, the parasitic capacitor is shorted and the terminal voltage v is pulled down to zero in a very short time. This time is ignored in the analysis of T_f. Curves of T_r and T_f are plotted based on equations (12) and (13), as shown in Fig. 8, where T_d =3us, T_don=0.12us, T_doff =0.51us, U_BAT =248V and C_p=1nF.

Fig. 8. Characteristics of the rise time and fall time of inverter output voltage for the instantaneous value of phase current.

B. Demonstration of the Consistency between the Sign of the Compensation Time Tc and the Current Polarity

Before derivation the consistency, some assumptions should be set and some minor factors should be neglected. (1) The switches of one arm is of consistency. (2) The charging time of the parasitic capacitor is zero when connected to the positive pole of battery. (3) The discharging time of the parasitic capacitor is zero after the lower switch is turned on when the current is negative. (4) The transition delays of the rising and falling edge of the gate-drive signals are the same, T_ton= T_toff. (5) Ignore the effect of zero-current clamping. The demonstration is divided into 3 conditions according to the polarities of i_r and i_f.

1) i_r >0 and i_f >0: Under this condition, the rising edge and falling edge of the terminal voltage are caused by the turn on and turn off of the upper switch, respectively. As shown in Fig. 5(a), T_von and T_voff are:

                (14)

Considering (4), (14) and Fig. 7, when i_f >0, T_f increases with the decrease of i_f. When i_f →0+, T_f reaches its maximum value T_d + T_don - T_doff, and T_voff also reaches its maximum value T_d + T_don. T_c reaches its minimum value T_r according to (15). T_r is supposed to be zero when i_r >0. However, T_r is close to but slightly larger than zero. The minimum value of T_c is bigger than zero. Therefore, T_c >0 when i_r >0 and i_f >0. The derivation process is concluded as follows:

    (15)

2) i_r <0 and i_f <0: Under this condition, when i_r <0, T_r increases with the increase of i_r. When i_r →0-, T_r reaches its maximum value T_d + T_don - T_doff, and T_voff also reaches its maximum value T_d + T_don and T_c reaches its maximum value –T_f according to (16). The maximum value of T_c is negative. Therefore, T_c <0 when i_r <0 and i_f <0. The derivation process is concluded into the following equation.

  (16)

3) i_r <0 and i_f >0: The compensation time T_c in this condition is:

             (17)

As in Fig. 8, when |i_r|<|i_f |, T_r >T_f. Therefore, T_c > 0 according to equation (17). Similarly, when |i_r|=|i_f | and |i_r|>|i_f |, the conclusions T_c = 0 and T_c < 0 can be derived respectively.

Summarizing the relation between T_c, i_r and i_f under the three conditions, the following expression is obtained.

             (18)

Define the equivalent phase current polarity i_ep:

                 (19)

Introduce i_ep into expression (18). Then expression (20) is derived as:

                   (20)

It has been theoretically verified that the sign of the compensation time T_c is consistent with the equivalent phase current polarity.

C. Experiment Verification of the Demonstration

Fig. 9 shows the variation trend of the terminal voltage in 6 consecutive cycles when the phase current increases from negative to positive in experiments. Fig. 10 shows the variation trend of the phase current, the equivalent phase current polarity i_ep and the compensation time T_c of the 6 consecutive cycles in Fig. 8. In Fig. 9(a), the rise time is long and the fall time is short, which indicates that current at the rising edge i_r and falling edge i_f are both negative, as shown in Fig. 9(a). In Fig. 9(b) and Fig. 9(c), the rise time and fall time both increase when compared with Fig. 9(a). The rise time increases when the current is negative since if the amplitude of the current decreases, the charging time of the parasitic capacitor increases and then the rise time increases. The fall time increases since the current at the falling edge if it has changed from negative in Fig. 9(a) to positive in Fig. 9(b) and Fig. 9(c), as shown in Fig. 10. The fall time in Fig. 9(c) is shorter than that in Fig. 9(b) because current at the falling edge if it increases and the parasitic capacitor discharges faster. In Fig. 9(a), (b), (c), (d) and (e), the rise time remains long which means that the current at the rising edge i_r is still negative, and the rising time becomes longer and longer since i_r becomes smaller and smaller and the parasitic capacitor charges slower and slower. When the absolute value of i_r is smaller than I_c, the charging time of the parasitic capacitor is limited by T_d + T_don - T_doff. Therefore, the slope of the rising edge changes sharply in Fig. 9(e). In Fig. 9(f), the rise time is short and the fall time is long, which indicates that the current is positive at both the rising edge and the falling edge. To summarize, the current finishes the change from negative to positive in 6 consecutive cycles, and the phase current is oscillating in this process. In particular, in Fig. 9(d), the current amplitude at the rising edge and the falling edge are about equal but the polarities are opposite. This is the condition where the equivalent phase current polarity i_ep is equal to zero. It can be seen roughly that T_c=0 in the figure. It is experimentally verified that the compensation time T_c has the same sign as the equivalent phase current. The variation trend of the phase voltage in 6 consecutive cycles when the phase current decreases from positive to negative in experiments will not be repeated here.

Fig. 9. Trend of the terminal voltage in 6 consecutive cycles when the phase current increases from negative to positive in experiments.

(a)

(b)

(c)

(d)

(e)

(f)

Fig. 10. Variation trend of the phase current, equivalent phase current polarity i_ep and compensation time T_c of the 6 consecutive cycles in Fig. 9.

Taken together, the amplitude and polarity of the compensation voltage can be derived from the compensation time T_c. Thus, the compensation method is simplified. The key factor turns into accurately measuring the compensation time T_c. Since the change rule of T_c is complicated, the online measurement of T_c is implemented in this paper. As defined above, the compensation time T_c is equal to the high-level duration of U^Ideal minus the high-level duration of U^Actual. The high-level duration of U^Ideal is given by PWM^Ideal, and the high-level duration of U^Actual can be measured by real-time feedback of the terminal voltage. The actual terminal voltage is a periodic rectangular wave. Thus, the event capture unit can be used to obtain the high-level duration of U^Actual. In addition, since the actual terminal voltage is digital signal, it is easy to catch and interference-free. As a result, isolation is not required for the hardware feedback circuit, and a high-speed comparator for voltage comparison is used to get the high-level duration of U^Actual precisely and quickly. Fig. 11 shows a control-model with the proposed compensation method.

Fig. 11. Control-model with the proposed compensation method.

Ⅳ. SIMULATION RESULTS

A simulation model is established to verify the proposed method. The simulation parameters are shown in Table I.

TABLE I SIMULATION PARAMETERS

Variables	Quantities	Units
Battery voltage UBAT	248	V
PWM period	100	μs
Dead time	3	μs
Forward voltage drop UF	1.6	V
Diode voltage drop UD	1.5	V
Electric time constant	2.979	ms
Stator phase resistance Rs	2.35	ohm

The conventional open-loop fixed compensation is a simple and relatively effective compensation solution. The compensation time T_c equals to dead-time T_d. The compensation phase voltage can be defined in (21).

           (21)

Fig. 12 is a voltage waveform of the α axis and β axis in actual situations without compensation. In actual situations, the voltage and current are severely distorted especially by the 5^th and 7^th harmonics.

Fig. 12. Voltage waveforms of the α axis and β axis with FFT results in actual situations without compensation. (a) α axis voltage waveform and FFT results. (b) β axis voltage waveform and FFT results.

(a)

(b)

Fig. 13 is a voltage waveform of the α axis and β axis in actual situations adopting the conventional compensation scheme. It can be seen in Fig. 13 that the conventional scheme does reduce the distortion effect. However, the distortion in the zero-crossing region is still serious. This is because in the conventional scheme, the compensation time is fixed to T_d. However, as shown above, the compensation time is approximately equal to T_d only when the current amplitude is large and it varies a lot when the current amplitude is close to zero. Therefore, the conventional scheme can alleviate distortion when the current amplitude is large. However, it has no effect when the current amplitude is close to zero.

Fig. 13. Voltage waveforms of the α axis and β axis with FFT results in actual situations adopting the conventional compensation scheme. (a) α axis voltage waveform and FFT results. (b) β axis voltage waveform and FFT results.

(a)

(b)

Fig. 14 shows voltage waveforms of the α axis and β axis in actual situations by adopting the proposed compensation method. Fig. 14 verifies that the proposed method can make the voltage and current waveforms approach to a sine wave. The THD value is near 1%, and the proposed method behaves much better when current is close to zero.

Fig. 14. Voltage waveforms of the α axis and β axis with FFT results in actual situations adopting the proposed compensation method. (a) α axis voltage waveform and FFT results. (b) β axis voltage waveform and FFT results.

(a)

(b)

Ⅴ. EXPERIMENT RESULTS

An experimental platform is set up with a TMS320F28335. The load motor is an 184W induction motor. The experimental platform set up is shown in Fig. 15. The parameters of the experimental platform are listed in Table II.

Fig. 15. Experimental platform.

TABLE II EXPERIMENTAL PARAMETERS

Variables	Quantities	Units
Battery voltage UBAT	248	V
Motor rated voltage	200	V
Motor rated current	1.3	A
Motor rated speed	1725	rpm
Power module	PS21765	--

Fig. 16 shows waveforms of DSP feedback signal and the output signal of the VSI. As shown in Fig. 16, U^Actual has a distinct phase error and the feedback signal mirrors the actual pulse width quite well. In addition, when the rise time or fall time is long, the feedback signal reflects the equivalent pulse width defined in Fig. 1.

Fig. 16. DSP output signal, feedback signal and VSI output signal. (a) Phase current is negative. (b) Phase current is positive.

(a)

(b)

A. Comparison of the Compensation Error

Fig. 17 shows a contrast of the compensation voltage between the conventional scheme and the proposed scheme. It is clear that after compensation, the error voltage with the proposed scheme is much less than the error voltage with the conventional scheme. Moreover, the compensation voltages of the two schemes differ greatly at the zero-crossing regions.

Fig. 17. Comparison of compensation voltages between the conventional method and proposed method. (a) Error voltage after compensation. (b) Compensation voltage. (c) Errors of the two compensation methods.

(a)

(b)

(c)

B. Compensation Effects at Low Speed

Fig. 18 and Fig. 19 show current and voltage waveforms at an ultra-low speed of 3r/min. As can be seen in the figures, the voltage and current are seriously distorted and the motor jitters violently. The actual voltage is almost the same as the command voltage when applying the proposed method. However, the effect of the conventional scheme is not satisfying. The compensation voltage of the conventional method consists of straight lines. However, the compensation voltage of the proposed method has more rounded edges.

Fig. 18. α axis current and α axis compensation voltage at 3r/min. (a) Phase current without compensation. (b) Phase current with the conventional compensation. (c) Phase current with the proposed compensation.

(a)

(b)

(c)

Fig. 19. α axis current and α axis compensation voltage at 3r/min. (a) Phase voltage without compensation. (b) Phase voltage with the conventional compensation. (c) Phase voltage with the proposed compensation.

(a)

(b)

(c)

Fig. 20 and Fig. 21 show current and voltage waveforms at a speed of 30r/min. The conventional method has a negative effect on the zero-crossing regions while the proposed method compensates the voltage almost perfectly during the whole process.

Fig. 20. α axis current and α axis compensation voltage at 30r/min. (a) Phase current without compensation. (b) Phase current with the conventional compensation. (c) Phase current with the proposed compensation.

(a)

(b)

(c)

Fig. 21. α axis current and α axis compensation voltage at 30r/min. (a) Phase voltage without compensation. (b) Phase voltage with the conventional compensation. (c) Phase voltage with the proposed compensation.

(a)

(b)

(c)

C. Compensation Effects When the Speed Varies

Fig. 22 shows that the compensation time always changes with the phase current. Therefore, this regularity has been verified by theoretical derivation, simulations and experiments.

Fig. 22. Waveforms when the rotor speed leaps from 3r/min to 30r/min. (a) α axis current and compensation time Tc. (b) α axis current and compensation voltage. (c) α axis actual voltage and command voltage.

(a)

(b)

(c)

In addition, in Fig. 22(c), the experiment with speed varies from 3r/min to 30r/min is carried out and the compensation time still follows the current perfectly.

Fig. 23 shows compensation results at a relatively high frequency with the proposed method in experiments. The FFT analysis indicates that the proposed method is effective in suppressing voltage harmonics at a high frequency. As can be seen in Fig. 24, with an increase of frequency, the voltage harmonics decrease to a low level even without compensation. Instead of suppressing voltage harmonics, the traditional method aggravates voltage distortion, while the proposed compensation method alleviates voltage distortion under all measured frequencies.

Fig. 23. α axis voltage and FFT analysis at a relatively high frequency with the proposed method. (a) 30Hz. (b) 60Hz.

(a)

(b)

Fig. 24. Voltage THD at various frequencies.

Ⅵ. CONCLUSIONS

The voltage distortion caused by the dead time and nonideal characteristics of components has a negative effect on the performance of motors. Therefore, compensation of the voltage is necessary in high precision control systems. The distortions in the entire driving unit are synthetically considered in the proposed method, and the feedback control of a VSI is realized. This paper theoretically and experimentally demonstrates the consistency between the compensation time and the corresponding phase current in one PWM cycle. Finally, it is concluded that the amplitude and polarity of compensation voltage can both be derived from the compensation time. Simulation and experimental results show that the proposed method can achieve a satisfactory effect under various conditions. When compared with conventional methods, the proposed method doesn’t need high-precision current sensing. Thus, it has broader application prospects.

Acknowledgment

The authors gratefully acknowledge the financial support of the Primary Research and Development Plan of Shandong Province (2016ZDJS03A04), the Fundamental Research Funds for the Central Universities (HIT.NSRIF.201705) and Natural Science Foundation of Shandong Province (ZR2017MEE011).

References

[1] H. S. Kim, K. H. Kim, and M. J. Youn, “On-line dead-time compensation method based on time delay control,” IEEE Trans. Contr. Syst. Technol. Vol. 11, No. 2, pp. 279-285, Mar./Apr. 2003.

[2] Y. Park and S.-K. Sul, “A novel method utilizing trapezoidal voltage to compensate for inverter nonlinearity,” IEEE Trans. Power Electron., Vol. 27, No. 12, pp. 4837-4846, Dec. 2012.

[3] N. Urasaki, T. Senjyu, K. Uezato, and T. Funabashi. “On-line dead-time compensation method for permanent magnet synchronous motor drive,” Proc. ICIT '02. Vol. 1. pp. 268-273, 2002.

[4] H. W. Kim, M. J. Youn, K. Y. Cho, and H. S. Kim, “Nonlinearity estimation and compensation of PWM VSI for PMSM under resistance and flux linkage uncertainty,” IEEE Trans. Contr. Syst. Technol., Vol. 14, No. 4, pp. 589-601, Jul. 2006.

[5] Y. A.-R. I. Mohamed, “Adaptive self-tuning speed control for PMSM drive system with dead time,” IEEE Trans. Energy Convers., Vol. 21, No. 4, pp. 885-862, Dec. 2006.

[6] D. Park and K. Kim, “Parameter-independent online compensation scheme for dead time and inverter nonlinearity in IPMSM drive through waveform analysis,” IEEE Trans. Ind. Electron., Vol. 61, No. 2, pp. 701-707, Feb. 2014.

[7] N. Urasaki, T. Senjyu, K. Uezato, and T. Funabashi, “An adaptive dead-time compensation strategy for voltage source inverter fed motor drives,” IEEE Trans. Power Electron., Vol. 20, No. 5, pp. 1150-1160, Sep. 2005.

[8] C.-H. Choi and J.-K. Seok, “Compensation of zero-current clamping effects in high-frequency-signal-injection-based sensorless PM motor drives,” IEEE Trans. Ind. Appl., Vol. 43, No. 5, pp. 1258-1265, Sep. 2007.

[9] K.S. Young, W. Lee, M. S. Rho, and S. Y. Park. “Effective dead-time compensation using a simple vectorial disturbance estimator in PMSM drives,” IEEE Trans. Ind. Electron., Vol. 57, No. 5, pp. 1609-1614, May 2010.

[10] S.-H. Hwang and J.-M. Kim, “Dead time compensation method for voltage-fed PWM inverter,” IEEE Trans. Energy Convers., Vol. 25, No. 1, pp. 1-10, Mar. 2010.

[11] M. Ogawa, S. Ogasawara, and M. Takemoto, “A feedback-type dead-time compensation method for high-frequency PWM inverter – Delay and pulse width characteristics,” in Proc. IEEE 27th Annu. Appl. Power Electron. Conf. Expo., pp. 100-105, 2012.

[12] L. Q. Zhou, “Dead-time compensation method of SVPWM based on DSP,” IEEE Conf. on Ind. Electron. and Appl., pp. 2355-2358, 2009.

[13] N. Urasaki, T. Senjyu, K. Uezato, and T. Funabashi, “A dead-time compensation strategy for permanent magnet synchronous motor d rive sup-pressing current distortion,” in Proc. IEEE IECON 2003, pp. 1255-1260, 2003.

[14] Y. K. Lin and Y. S. Lai, “Dead-time elimination of PWM controlled inverter/converter without separate power sources for current polarity detection circuit,” IEEE Trans. Ind. Electron., Vol. 56, No. 6, pp. 2121-2127, Jun. 2009.

[15] K. M. Cho, W. S. Oh, Y. T. Kim, and H. J. Kim, “A new switching strategy for pulse width modulation (PWM) power converters,” IEEE Trans. Ind. Electron., Vol. 54, No. 1, pp. 330-337, Feb. 2007.

[16] L. Chen and F. Z. Peng, “Dead-time elimination for voltage source inverters,” IEEE Trans. Power Electron., Vol. 23, No. 2, pp. 574-580, Mar. 2008.

[17] H.-T. Moon, H.-S. Kim, and M.-J. Youn, “A discrete-time predictive current control for PMSM,” IEEE Trans. Power Electron., Vol. 18, No. 1, pp. 464–472, Jan. 2003.

[18] D. F. Wang, B. W. Yang, C. Zhu, C. W. Zhou, and J. Qi, “A feedback-type phase voltage compensation strategy based on phase current reconstruction for ACIM drives,” IEEE Trans. Power Electron., Vol. 29, No. 9, pp. 5031-5043, Sep. 2014.

Mingyu Wang received his B.S. and M.S. degrees in Automotive Engineering, Harbin Institute of Technology, Weihai, China, in 2014 and 2016, respectively. He is presently working towards his Ph.D. degree in Mechano-Electronic Engineering for Electric Vehicles at Harbin Institute of Technology. His current research interests include e-PMSM emulations and electric vehicle motor traction systems.

Dafang Wang was born in Liaoning, China, in 1978. He received his M.S. degree in Automotive Engineering from the Harbin Institute of Technology, Harbin, China, in 2002; and his Ph.D. degree in Automotive Engineering from Beijing Institute of Technology, Beijing, China, in 2008. He is presently working as a Professor at the Harbin Institute of Technology, Weihai, China. His current research interests include new energy and intelligent connected vehicles.

Chuanwei Zhou was born in Jiangsu, China, in 1991. He received his M.S. degree in Vehicle Engineering from the Harbin Institute of Technology, Weihai, China, in 2015. After graduating, he joined Beijing Benz Automotive CO. LTD. His current research interests include power electronics, vehicle bus (CAN), and electric vehicle motor traction systems.

Xiu Liang was born in Shandong, China, in 1995. She received her B.S. degree in Vehicle Engineering from the Harbin Institute of Technology, Weihai, China, in 2017, where she is presently working towards her M.S. degree in Vehicle Engineering. Her current research interests include electric vehicle motor traction systems, rapid control prototypes, and Hardware-in-the-Loop (HIL) systems.

Guanglin Dong was born in Shandong, China, in 1995. He received his B.S. degree in Vehicle Engineering from the Harbin Institute of Technology, Weihai, China, in 2017, where he is presently working towards his M.S. degree in Vehicle Engineering. His current research interests include the Hardware-in-the-Loop (HIL) systems of electric vehicles and motor traction systems.