Skip to content
Protection and Control of Modern Power Systems
Protection and Control of Modern Power Systems Cover Image

We’re sorry, something doesn't seem to be working properly.

Please try refreshing the page. If that doesn't work, please contact us so we can address the problem.

Novel transient-energy-based directional pilot protection method for HVDC line

Protection and Control of Modern Power Systems20172:15

https://doi.org/10.1186/s41601-017-0047-z

©  The Author(s) 2017

  • Received: 1 December 2016
  • Accepted: 21 March 2017
  • Published:

Abstract

This paper proposes a novel directional pilot protection method based on the transient energy for bipolar HVDC line. Supposing the positive direction of current is from DC bus to the DC line, in the case of an internal line fault, the transient energies detected on both sides of the line are all negative within a short time, which denotes the positive direction fault; while for an external fault, the transient energy on one end is positive, which means a negative direction fault, but the transient energy on the opposite end is negative, which indicates that the fault direction is positive. According to these characteristics, an integration criterion identifying fault direction is constructed. In addition, through setting a fixed energy threshold, the faulted line and lightning disturbance can also be discriminated. Simulation results from UHVDC transmission system show the validity of the proposed protection method.

Keywords

  • Transient energy
  • HVDC line
  • Directional pilot protection
  • Fault direction
  • Lightning stroke

1 Introduction

Compared with the high voltage AC power transmission, HVDC power transmission has some advantages, such as larger transmission capacity, longer transmission distance, lower line loss, etc., which is becoming an important power transmission way on asynchronous grid interconnection and clean energy power integration [1–3]. Because of the long distance and passing through the valleys and mountains, HVDC lines easily suffer from the faults caused by lightning, storm, and so on. Therefore, to ensure the safety and stability of DC transmission system, a fast, reliable and sensitive HVDC line protection is indispensable.

At present, the primary protections used in HVDC line are traveling wave protection and voltage variation protection, which have poor ability to resist the high ground resistance fault [4]. Additionally, their performances are also affected by other disturbance signals. HVDC line differential protection used for the back-up protection also has certaion shortcomings, such as slow operation speed and requiring the synchronous data [5, 6].

Aiming at these problems mentioned above, many protection methods have been put forward. In [7], authors analyze the performances of HVDC line protection for different fault transition resistance, fault position, etc., and finally present several improvement suggestions. Through analyzing the harmonic current characteristics of converter station, a protection scheme based on the transient harmonic current is present for HVDC line in [8]. According to the boundary characteristics of HVDC line, some protection methods only using one-end information are proposed in [9–12]. Although these methods have fast speed, their sensitivity and reliability are still influenced by the fault resistance, in addition, it is also difficult to set the threshold value. In [13, 14], authors propose the distance protection methods for HVDC line, but the high ground resistance fault still has a negative influence on their protection performances. To improve the reliability of protection, the hybrid protection schemes based on different principles are put forward in [15–17], but implementing these schemes is still a challenge in actual HVDC transmission engineering.

In [18] and [19], the transient-energy based protection methods are proposed for HVDC line, which can identify an internal or external fault by comparing the amplitudes of the transient energies on both ends of the line, these methods are similar to the current differential protection, and they need strict data synchronization. Different from the aforementioned methods, this paper presents a novel directional pilot protection method based on the polarity characteristic of transient energy. For a fault inside the DC line, the transient energies detected on both sides of HVDC line are negative; while the transient energy on one side is positive, and that on the other side is negative for an external fault. On the basis of this fact, an integral criterion identifying the fault direction is constructed. By analyzing the fault directions on both sides, the internal fault can be discriminated from the external fault. Due to only using the directional information, the proposed protection method does not require the synchronous data at all. To verify the performance of the proposed method, a bipolar HVDC transmission system model is built, and extensive simulations are carried out.

2 Methods

2.1 Characteristic analysis of transient energy

2.1.1 Simplified equivalent circuit of HVDC transmission system

To simply analyze, the converter may be approximate equivalent to a series of voltage source and impedance, this equivalent circuit does not produce an obvious influence on the fault analysis. Figure 1 shows the equivalent circuit of single-pole HVDC system, where Z eq denotes the equivalent impedance of the converter station; Z L is the impedance of DC line; u m+ and i m+ are the voltage and current at terminal M, respectively; u n+ and i n+ are the voltage and current at terminal N, respectively; u 1 and u 2 are the equivalent voltage sources at two converters. Here, supposing the positive direction of current is from DC bus to DC line, as shown in Fig. 1. The main fault types for bipolar DC line include the single pole to earth faults and pole to pole fault, where the single pole to earth faults contain the positive pole to earth fault and the negative pole to earth fault. The analyses of internal and external faults for HVDC line are described as below.
Fig. 1
Fig. 1

Simplified equivalent circuit of DC power transmission system

2.1.2 Transient energy characteristics for pole-earth fault

If a pole-earth fault occurs on the positive pole line, Fig. 2 shows an equivalent fault superimposed circuit.
Fig. 2
Fig. 2

Fault superimposed circuit for a positive-pole to earth fault

In Fig. 2, L denotes the length of DC line; F is the fault point; Z x is the line impedance from F to terminal M, and Z (l -x) is the line impedance from F to terminal N; R F is the fault resistance; u F represents the fault superimposed voltage source; Δu m+ and Δi m+ are the fault components of voltage and current at terminal M, respectively; Δu n+ and Δi n+ are the fault components of voltage and current at terminal N.

According to Fig. 2, the following equations can be obtained:
$$ \varDelta {u}_{\mathrm{m}+}=-{Z}_{eq}\varDelta {i}_{\mathrm{m}+} $$
(1)
$$ \varDelta {u}_{\mathrm{n}+}=-{Z}_{eq}\varDelta {i}_{\mathrm{n}+} $$
(2)
From (1) and (2) it can be seen that the polarities of Δu m+ and Δi m+ are opposite, so are the polarities of Δu n+ and Δi n+ . Therefore, the variations of transient power on both sides of the line ΔP m + = Δu m + Δi m + and ΔP n + = Δu n + Δi n + are all negative, further their integral values shown in (3) and (4) are also negative.
$$ {S}_{\mathrm{m}+}={\displaystyle {\int}_0^{\tau}\varDelta {P}_{\mathrm{m}+}(t) dt} $$
(3)
$$ {S}_{\mathrm{n}+}={\displaystyle {\int}_0^{\tau}\varDelta {P}_{\mathrm{n}+}}(t) d t $$
(4)
where, S m+ and S n+ denote the transient energies measured at terminals M and N of the positive pole line, respectively; τ is the integral time. Here, the reason that introduces the transient power integral is to decrease the influence from disturbance and improve the reliability of protection.

Similarly, if there is a pole-earth fault occurring on the negative pole line, the transient energies S m- and S n- detected at terminals M and N of the negative pole line are also negative.

2.1.3 Transient energy characteristics for pole-pole fault

If a bipolar line fault occurs on the HVDC lines, the fault superimposed circuit is shown in Fig. 3, where F1 and F2 are the fault points on the positive pole line and negative pole line, respectively. Δu m- and Δi m- are the fault components of voltage and current at terminal M of the negative pole line; Δu n- and Δi n- are the fault components of voltage and current at terminal N.
Fig. 3
Fig. 3

Fault superimposed circuit for a pole-pole fault

According to Fig. 3, the following equations can be obtained:
$$ \left\{\begin{array}{c}\hfill \varDelta {u}_{\mathrm{m}+}=-{Z}_{eq}\varDelta {i}_{\mathrm{m}+}\hfill \\ {}\hfill \varDelta {u}_{\mathrm{n}+}=-{Z}_{eq}\varDelta {i}_{\mathrm{n}+}\hfill \\ {}\hfill \varDelta {u}_{\mathrm{m}-}=-{Z}_{eq}\varDelta {i}_{\mathrm{m}-}\hfill \\ {}\hfill \varDelta {u}_{\mathrm{n}-}=-{Z}_{eq}\varDelta {i}_{\mathrm{n}-}\hfill \end{array}\right. $$
(5)

From (5) it can be seen that the variations of transient power on each side of bipolar line are all negative and, after the integral calculation, the transient energies are also negative.

Based on the above analyses, the following conclusions can be drawn: for an internal DC line fault, whatever it is a single pole to earth fault or a pole to pole fault, the power variations on both sides of the faulted line are always negative, as well as the transient energies.

2.1.4 Transient energy characteristics for external fault

For HVDC line, external faults include two types, one type occurs on the DC side, and the other type occurs on the AC side. Actually, the influence generated by an AC side external fault on HVDC line protection is similar to that generated by a DC side external fault, and the transient analyses for the external faults are discussed as follows.

Faults outside the positive pole line

If a fault occurs on the converter valve or DC bus of the rectifier side, the fault superimposed circuit is shown in Fig. 4a, where Z eq1 and Z eq2 are the equivalent impedances from the fault point to both sides of the rectifier station. For a fault occurring on the AC side at the rectifier station, the fault superimposed circuit is shown in Fig. 4b.
Fig. 4
Fig. 4

Fault superimposed circuit for a fault occurring on the rectifier side. a Fault occurring on the converter valve or DC bus. b Fault occurring on the AC side

From Fig. 4, Δu m+ and Δi m+ can be expressed as:
$$ \varDelta {u}_{\mathrm{m}+}=\left({Z}_{eq}+{Z}_L\right)\varDelta {i}_{\mathrm{m}+} $$
(6)
$$ \varDelta {u}_{\mathrm{n}+}=-{Z}_{eq}\varDelta {i}_{\mathrm{n}+} $$
(7)

In (6) and (7), the polarities of Δu m+ and Δi m+ at the rectifier side are the same, while those of Δu n+ and Δi n+ at the inverter side are opposite. Therefore, the transient power variation ΔP m+ is positive, but ΔP n+ is negative and, thus the transient energy S m+ is positive while S n+ is negative.

When a fault occurs on the converter valve or DC bus of the inverter side, the corresponding fault superimposed circuit is shown in Fig. 5a and b illustrates the fault superimposed circuit for a fault occurring on the AC side.
Fig. 5
Fig. 5

Fault superimposed circuit for a fault occurring on the inverter side. a Fault occurring on the converter valve or DC bus. b Fault occurring on the AC side

As shown in Fig. 5:
$$ \varDelta {u}_{\mathrm{m}+}=-{Z}_{eq}\varDelta {i}_{\mathrm{m}+} $$
(8)
$$ \varDelta {u}_{\mathrm{n}+}=\left({Z}_{eq}+{Z}_L\right)\varDelta {i}_{\mathrm{n}+} $$
(9)

From (8) and (9) it can be seen that the polarities of Δu m+ and Δi m+ at the rectifier side are opposite, while those of Δu n+ and Δi n+ at the inverter side are the same. Therefore, the transient power variation ΔP m+ is negative, and ΔP n+ is positive, so the corresponding transient energy S m+ is negative while S n+ is positive.

Faults outside the negative pole line

Similarly, the same conclusions as the aforementioned cases can be drawn: for the faults outside the negative pole line, no matter a fault occurs on the rectifier station or on the inverter station, the polarities of the transient energies detected on both sides of the negative pole line are always opposite.

2.2 Protection criterion for HVDC line

According to the analyses in Section 2.1, the following conclusions can be obtained: in case of an internal fault occurring on the HVDC line, the transient energies detected on both the rectifier side and the inverter side are all negative; but for a fault occurring outside the HVDC line, the transient energy on one side is positive, and the transient energy on the other side is negative.

Therefore, using the characteristic difference of transient energy after the fault, the fault direction can be determined. If the transient energy is negative, the fault direction is positive; if the transient energy is positive, the fault direction is negative. As a result, if the fault directions on both sides of HVDC line are all positive, an internal fault will be discriminated. However, If the fault direction on one side is positive, and that on the opposite side is negative, an external fault will be identified.

It has been specified that the substitution of transient energy for fault component power is to improve the reliability of protection.

To implement conveniently, the discretized transient energy equation of (3) and (4) can be expressed:
$$ {S}_{\eta p}=\varDelta t{\displaystyle \sum_1^j\varDelta {u}_{\eta p}(k)\varDelta {i}_{\eta p}(k)} $$
(10)
where, Δu ηp (k) and Δi ηp (k) are the fault components of voltage and current at the kth sampling point, which can be extracted by filtering load component; j is the number of the sampling point used for integral calculation; Δt is the sampling interval; η denotes the rectifier side M or the inverter side N; the variable p denotes + or -, which means the positive pole line or the negative pole line. In actual calculation process, Δt may be omitted.
If a single pole to earth fault occurs, the transient signals on the faulted line can be coupled to the normal line, which possibly affects the fault identification of the normal line. Moreover, lightning stroke or normal operation can also generate disturbance signals. To avoid these influences, a fixed energy threshold S set is necessary, which is defined as follows:
$$ {S}_{set}= j{k}_{rel}{k}_i{k}_u $$
(11)
where k rel is the reliable coefficient; k i and k u are the proportional coefficients of rated current and rated voltage, respectively. Note that the rated current and the rated voltage are all expressed as per unit value here, so that S set can be applied to different HVDC system. In addition, for a long HVDC line, the probability of lightning stroke is high. Therefore, lightning stroke line without causing fault must be correctly identified by the protection. The sampling frequency of the proposed method is relatively low (10 kHz) and integral calculation is used in the algorithm, which can filter high frequency components to some extent. Moreover, the amplitude of lightning current for direct stroke line is low [20, 21], and generally the transient energy caused by lightning disturbance will not exceed the fixed threshold.
For convenient analysis, a rule is defined here. The logic value of a positive directional fault is 1, and that of the negative directional fault is equal to −1, and 0 means there is no fault. Therefore, the transient energy direction Dir[S ηp ] is expressed as follows:
$$ D i r\left[{S}_{\eta p}\right]=\left\{\begin{array}{l}-1\kern1em {S}_{\eta p}\kern0.5em \ge {S}_{set}\\ {}\kern0.5em 0\kern1.5em \left|{S}_{\eta p}\right.\kern0.5em \left|<{S}_{set}\right.\\ {}\kern0.5em 1\kern1.5em {S}_{\eta p}\kern0.5em \le -{S}_{set}\end{array}\right. $$
(12)

The logic identifying fault is described as below: if the logic values of fault direction detected on both sides of HVDC line are equal to 1, an internal fault will be determined; if the logic value of fault direction on one side is 1, while that on the other side is −1, an external fault will be discriminated; otherwise, it is normal.

3 Results and discussion

3.1 Simulation and analysis

3.1.1 Simulation model

To test the performance of the proposed protection principle, using the actual parameters of ±800 kV Hami-Zhengzhou HVDC transmission system in China, this paper constructs a simulation model of bipolar UHVDC system with a double 12-pulse valves at each converter station. The frequency-dependent line model is utilized for accurate simulation. As shown in Fig. 6, the length of UHVDC line is 2190 km, the transmission capacity is up to 8000 MW, and the rated current is 5 kA.
Fig. 6
Fig. 6

±800 kV UHVDC transmission system model

In Fig. 6, extensive internal and external faults will be simulated, and the sampling frequency is 10 kHz. Practical operating experience shows the polarity of lightning current is generally negative, so the lightning stroke mainly occurs on the positive pole line and a standard 2.6/50 μs lightning current is used in the simulation. A multi-wave-impedance tower model, a flashover insulator model and a nonlinear surge earth impedance model are included to evaluate the back-flashover accurately. For convenient analysis, the fault components of voltage and current, and the value of transient energy are all expressed in per unit value. Considering the lightning stroke interference of 2 ~ 3 ms and the influence of fault resistance, the integral time is set as 5 ms, and the fixed threshold S set is set as 1 here.

3.1.2 Typical internal faults

Single-pole to earth fault

When a fault occurs on the positive pole line at F1 500 km from the rectifier station, and the fault ground resistance and fault initial instant are 300 Ω and 0 ms, respectively. The waveforms of fault component voltage and fault component current, and the waveforms of transient energies detected on the rectifier side and the inverter side are shown in Figs. 7a and b, respectively. The corresponding simulation results are listed in Table 1, where RF denotes the fault ground resistance, sign/means that the relay does not start. Here, once the variation of voltage exceeds 0.2 times rated voltage or the variation of current exceeds 0.1 times rated current in three consecutive samples, the relay starts.
Fig. 7
Fig. 7

Waveforms of fault components and transient energies detected on the positive pole line for a fault at F1. a Rectifier station. b Inverter station

Table 1

Simulation results for a fault at F1

Location

RF (Ω)

Pole

Rectifier side

Inverter side

Result

S m

Dir

S n

Dir

 

F1

300

+

−1.96

1

−1.91

1

Internal

-

/

/

/

/

Normal

For positive pole line, it can be seen from Fig. 7 and Table 1 that the polarities of fault component voltage and current are opposite; the transient energies detected on both the rectifier side and the inverter side are negative, and they all exceed the threshold value, so two protection units on both sides of the positive pole line identify a positive direction fault. According to the identification logic, finally an internal fault occurring on the positive pole line is verified. Therefore, the result is correct, and this method has a powerful ability to resist the fault resistance.

Metallic earth fault at F2

For a fault at F2 occurring on the middle of the negative pole line, Fig. 8 shows the waveforms of fault components and transient energies detected on both ends of the negative pole line, and the waveforms of fault components and transient energies detected on both ends of the positive pole line (normal line) are shown in Fig. 9. Table 2 shows the relevant simulation results.
Fig. 8
Fig. 8

Waveforms of fault components and transient energies detected on the negative pole line for a fault at F2. a Rectifier station. b Inverter station

Fig. 9
Fig. 9

Waveforms of fault components and transient energies detected on the positive pole line for a fault at F2. a Rectifier station. b Inverter station

Table 2

Simulation results for a fault at F2

Location

RF (Ω)

Pole

Rectifier side

Inverter side

Result

S m

Dir

S n

Dir

F2

0

+

−0.19

0

−0.19

0

Normal

-

−11.01

1

−11.52

1

Internal

From Fig. 8 and Table 2, it can be seen that the transient energies on both ends of the negative pole line have the same negative polarity and they both exceed the fixed threshold. Therefore, the protection units at two sides of the negative pole line identify a positive direction fault, finally an internal fault occurring on the negative pole line is determined.

Because of the coupling influence, the transient voltage and current can also be detected on the normal line. As shown in Fig. 9 and Table 2, the transient voltage and current on two ends of the positive pole line rise at fault initial stage for a fault at F2, but the transient energies detected on both ends of the line don’t exceed the fixed threshold, thus the protection units at two ends will not operate. Therefore, through setting a fixed threshold, a single pole to earth fault has no effect on the fault identification of the normal line.

Pole to pole fault at F3

For a pole to pole fault at F3 occurring on the middle of the bipolar line, Figs. 10 and 11 show the transient waveforms detected on both ends of the bipolar line, and the simulation data are shown in Table 3.
Fig. 10
Fig. 10

Waveforms of fault components and transient energies detected on the positive pole line for a fault at F3. a Rectifier station. b Inverter station

Fig. 11
Fig. 11

Waveforms of fault components and transient energies detected on the negative pole line for a fault at F3. a Rectifier station. b Inverter station

Table 3

Simulation results for a fault at F3

Location

RF (Ω)

Pole

Rectifier side

Inverter side

Result

S m

Dir

S n

Dir

F3

0

+

−27.41

1

−27.66

1

Internal

-

−27.63

1

−27.72

1

Internal

As shown in Figs. 10, 11 and Table 3, the transient energies detected on the positive pole line and the negative pole line exceed the fixed threshold, so the protection units at two ends of the bipolar line all identify a positive direction fault. In combination with the results on the two sides, a fault inside both the positive pole line and the negative pole line is identified, and the results are correct.

3.1.3 Typical external faults

External fault at F4

Supposing a fault occurs at F4 on the DC bus of the positive pole line in the rectifier station, Fig. 12 shows the transient waveforms detected on the positive pole line, and the simulation results are indicated in Table 4.
Fig. 12
Fig. 12

Waveforms of fault components and transient energies detected on the positive pole line for a fault at F4. a Rectifier station. b Inverter station

Table 4

Simulation results for a fault at F4

Location

RF (Ω)

Pole

Rectifier side

Inverter side

Result

S m

Dir

S n

Dir

F4

0

+

23.73

−1

−14.01

1

External

-

1.85

−1

−4.05

1

External

From Fig. 12 and Table 4, it can be seen that the transient energies detected on both ends of the positive pole line have obvious differences. The transient energy detected on the rectifier side is positive while it is negative on the inverter side. According to the fault identification logic, the protection unit at the rectifier side identifies a negative direction fault while the protection unit at the inverter side identifies a positive direction fault. Through analyzing the above results, an external fault is finally determined, and the same characteristic exists in the negative pole line, so the identification results are all correct.

External fault at F5

For a fault at F5 occurring on the AC side of the inverter station, Figs. 13 and 14 illustrate the transient waveforms detected on the positive pole line and the negative pole line, respectively, and Table 5 lists the relevant simulation results.
Fig. 13
Fig. 13

Waveforms of fault components and transient energies detected on the positive pole line for a fault at F5. a Rectifier station. b Inverter station

Fig. 14
Fig. 14

Waveforms of fault components and transient energies detected on the negative pole line for a fault at F5. a Rectifier station. b Inverter station

Table 5

Simulation results for a fault at F5

Location

RF (Ω)

Pole

Rectifier side

Inverter side

Result

S m

Dir

S n

Dir

F5

0

+

−11.08

1

12.24

−1

External

-

−11.20

1

12.48

−1

External

As shown in Figs. 13, 14, and Table 5, the polarities of transient energies detected on both ends of the positive line and the negative line are all opposite. Therefore, an external fault will be identified and the discrimination results are correct.

3.1.4 Simulation analysis of the influence factors

Fault location and fault ground resistance

Both the fault location and the fault ground resistance have certain impacts on the traditional DC line protection. To verify whether these factors have influences or not on the proposed protection method, the following simulations are carried out. Several faults with different fault ground resistances at different locations are set, and the simulation results for internal faults and external faults are shown in Tables 6 and 7, respectively.
Table 6

Simulation results for internal DC line faults

Location

RF (Ω)

Pole

Rectifier station

Inverter station

Result

S m

Dir

S n

Dir

F1 (1 km)

10

+

−34.02

1

−10.51

1

Internal

-

−0.27

0

−2.44

1

Normal

200

+

−5.64

1

−1.91

1

Internal

-

/

/

−0.43

0

Normal

300

+

−3.24

1

−1.13

1

Internal

-

/

/

/

/

Normal

F2 (500 km)

10

+

−0.17

0

−0.64

0

Normal

-

−13.23

1

−9.33

1

Internal

200

+

/

/

−0.04

0

Normal

-

−2.85

1

−2.37

1

Internal

300

+

/

/

/

/

Normal

-

−1.70

1

−1.71

1

Internal

F3 (1000 km)

10

+

−24.96

1

−25.01

1

Internal

-

−25.21

1

−25.09

1

Internal

200

+

−8.13

1

−8.44

1

Internal

-

−8.20

1

−8.46

1

Internal

300

+

−5.37

1

−5.69

1

Internal

-

−5.40

1

−5.80

1

Internal

Table 7

Simulation results for faults outside the DC line

Location

RF (Ω)

Pole

Rectifier station

Inverter station

Result

S m

Dir

S n

Dir

F4

10

+

19.14

−1

−11.08

1

External

-

1.61

−1

−3.16

1

External

200

+

1.66

−1

−0.88

0

Normal

-

/

/

−0.14

0

Normal

300

+

0.83

0

−0.26

0

Normal

-

/

/

/

/

Normal

F5 (AG)

10

+

−2.70

1

2.94

−1

External

-

−2.74

1

3.02

−1

External

300

+

/

/

/

/

Normal

-

/

/

/

/

Normal

F5 (BCG)

10

+

−11.92

1

12.10

−1

External

-

−11.50

1

12.22

−1

External

300

+

/

/

/

/

Normal

-

/

/

/

/

Normal

As seen from Table 6, for the single pole to earth faults or the pole-pole faults with different fault locations and different fault ground resistances, although the fault resistance has a negative influence on the transient energy value, the proposed method can still identify these faults, and the results are all correct.

For external faults with different fault ground resistances, the simulation results from Table 7 show that the proposed protection method can accurately identify these external faults, and the results are all right.

Lightning stroke

As mentioned in Section 2, lightning stroke on line or tower without causing fault may result in the maloperation of protective relay, so it is necessary to study the influence of lightning stroke on the proposed method. Tables 8 and 9 show the simulation results for lightning stroke disturbance and lightning stroke causing fault, respectively. It has to been explained, for direct lightning stroke, that only the positive pole line is considered.
Table 8

Simulation results for lightning stroke disturbance

Condition

Pole

S m

S n

Result

Lightning stroke on line without causing fault

20 kA

100 km

+

0.29

0.04

Normal

-

0.10

0.02

Normal

1095 km

+

−0.01

−0.01

Normal

-

0.03

/

Normal

30 kA

10 km

+

1.95

−0.05

Normal

-

−0.13

0.05

Normal

1500 km

+

0.17

0.15

Normal

-

0.07

0.13

Normal

Lightning stroke on tower without causing back-flashover

50 kA

1 km

+

/

/

Normal

-

/

/

Normal

2100 km

+

/

/

Normal

-

/

/

Normal

100 kA

10 km

+

/

/

Normal

-

/

/

Normal

1800 km

+

/

/

Normal

-

/

/

Normal

Table 9

Simulation results for lightning stroke causing faults

Condition

Pole

S m

S n

Result

Shielding failure

15 kA

1 km

+

−29.83

−9.14

Internal

-

−0.23

−2.13

Normal

500 km

+

−12.33

−8.77

Internal

-

−0.10

−0.62

Normal

30 kA

300 km

+

−13.79

−8.48

Internal

-

0.15

−0.84

Normal

900 km

+

−10.84

−9.18

Internal

-

−0.14

−0.27

Normal

Back- flashover

120 kA

10 km

+

−38.95

−11.56

Internal

-

−0.34

−2.40

Normal

1200 km

+

−9.46

−12.06

Internal

-

−0.57

0.88

Normal

200 kA

1095 km

+

−28.07

−27.16

Internal

-

−26.86

−28.61

Internal

2100 km

+

−25.49

−33.10

Internal

-

−25.23

−28.75

Internal

From Table 8 it can be seen, for lightning stroke without causing fault, that no matter it strikes on line or tower, the identification results are all correct. Moreover, for lightning stroke on tower without causing back-flashover, the protection units will not start.

As shown in Table 9, for shielding failure and back-flashover with different lightning current amplitudes and lightning stroke locations, those faults can also be correctly identified. Note that lightning stroke on tower with the amplitude of 200 kA causes both the positive pole and negative pole insulators back-flashover, but for lightning current of 120 kA, it only results in the insulator back-flashover of positive pole line. Therefore, the protection criteria can effectively discriminate between lightning stroke disturbance and lightning stroke fault.

4 Conclusions

Using the characteristic differences of transient energy on both sides of HVDC line after the fault, the paper proposes a novel directional pilot protection method. From the theoretical analysis and simulation results, the following conclusions can be obtained:
  1. 1)

    Due to applying directional pilot protection principle and energy integral criteria, the proposed protection method is rarely influenced by fault position, fault resistance and lightning stroke disturbance. For special fault cases, such as close-up faults or high ground resistance faults, the method can make a correct identification, so it has absolute selectivity and high reliability.

     
  2. 2)

    The proposed protection criteria can correctly identify the faulted line for a single pole to earth fault, so the method has good adaptability.

     
  3. 3)

    Because of only identifying the fault directions on both sides of HVDC line, so the pilot protection does not require the synchronous data.

     

Declarations

Acknowledgements

This work was supported in part by National Natural Science Foundation of China (51677109), and in part by National Key Research and Development Program of China (2016YFB0906003).

Authors’ contributions

Guibin Zou carried out the protection principle studies, drafted the manuscript. Qiang Huang participated in the sequence alignment. Shenglan Song and Bingbing Tong carried out the simulation and analysis. Houlei Gao participated in protection principle study and the design of study. All authors read and approved the final manuscript.

Competing interests

The authors declare that they have no competing interests.

Open AccessThis article is distributed under the terms of the Creative Commons Attribution 4.0 International License (http://creativecommons.org/licenses/by/4.0/), which permits unrestricted use, distribution, and reproduction in any medium, provided you give appropriate credit to the original author(s) and the source, provide a link to the Creative Commons license, and indicate if changes were made.

Authors’ Affiliations

(1)
Key Laboratory of Power System Intelligent Dispatch and Control of Ministry of Education, Shandong University, Ji’nan, China
(2)
State Grid Weifang Electric Power Company, Weifang, 261021, China
(3)
State Grid Langfang Electric Power Company, Langfang, 065000, China

References

  1. Yang, J., Fletcher, J. E., & O’Reilly, J. (2010). Multiterminal dc wind farm collection grid internal fault analysis and protection design. IEEE Transactions on Power Delivery, 25(4), 2308–2318.View ArticleGoogle Scholar
  2. Bresesti, P., Kling, W. L., Hendriks, R. L., et al. (2007). HVDC connection of offshore wind farms to the transmission system. IEEE Transactions on Energy Conversion, 22(1), 37–43.View ArticleGoogle Scholar
  3. Andersen, B. R., & Lie, X. (2004). Hybrid HVDC system for power transmission to island networks. IEEE Transactions on Power Delivery, 19(4), 1884–1890.View ArticleGoogle Scholar
  4. Zhang, S., & Li, Y. L. (2011). Simulation and analysis of HVDC line protection under the single pole to ground fault with high transition resistance (Electric Utility Deregulation and Restructuring and Power Technologies, 2011 4th International Conference on, pp. 926–929).Google Scholar
  5. Li, A. M., Cai, Z. X., Sun, Q. Z., et al. (2009). Study on the dynamic performance characterisitcs of HVDC control and protections for the HVDC line fault (Power & Energy Society General Meeting, p. 5).Google Scholar
  6. Gao, S. P., Chu, X., Shen, Q. Y., et al. (2015). A novel whole-line quick-action protection principle for HVDC transmission lines using one-end voltage. International Journal of Electrical Power and Energy Systems, 65, 262–270.View ArticleGoogle Scholar
  7. Kong, F., Hao, Z. G., Zhang, S., et al. (2014). Development of a novel protection device for bipolar HVDC transmission lines. IEEE Transactions on Power Delivery, 29(5), 2270–2278.View ArticleGoogle Scholar
  8. Song, G. B., Chu, X., Gao, S. P., et al. (2015). A new whole-line quick-action protection principle for HVDC transmission lines using one-end current. IEEE Transactions on Power Delivery, 30(2), 599–607.View ArticleGoogle Scholar
  9. Liu, K. Z., Yu, J. L., Shu, H. C., et al. (2012). Study on electrical transient protection for ±800kV UHVDC Transmission Lines. In:sia-Pacific Power and Energy Engineering Conference.Google Scholar
  10. Takeda, H., Ayakawa, H., Tsumenaga, M., et al. (2012). New protection method for HVDC lines including cables. IEEE Transactions on Power Delivery, 10(4), 2035–2039.View ArticleGoogle Scholar
  11. Ha, H., Yu, Y., & Yi, R. (2010). Novel scheme of traveling wave based differential protection for bipolar HVDC transmission lines (Proceedings of the International Conference Power Systems, Technology, p. 5).Google Scholar
  12. Zheng, X. D., Tai, T. N. L., Thorp, J. S., et al. (2001). A Transient Harmonic Current Protection Scheme for HVDC Transmission Line. IEEE Transactions on Power Delivery, 27(4), 2278–2285.View ArticleGoogle Scholar
  13. Han, K. L., Cai, Z. X., Liu, Y., et al. (2011). Study on protective performance of HVDC transmission line protection with different types of line fault (Electric utility deregulation and restructuring and power technologies (DRPT), pp. 358–361).Google Scholar
  14. Li, A. M., Cai, Z. X., Sun, Q. Z., et al. (2009). Study on the dynamic performance characteristics of HVDC control and protections for the HVDC line fault (Power & energy society general meeting, p. 5).Google Scholar
  15. Zheng, X. D., Tai, N. L., Yang, G. L., et al. (2012). A transient protection scheme for HVDC transmission line. IEEE Transactions on Power Delivery, 27(2), 718–724.View ArticleGoogle Scholar
  16. Liu, X. L., Osman, A. H., & Malik, O. P. (2009). Hybrid traveling wave/boundary protection for monopolar HVDC line. IEEE Transactions on Power Delivery, 24(2), 569–578.View ArticleGoogle Scholar
  17. Kerf, K. D., Srivastava, K., Reza, M., et al. (2012). Wavelet-based protection strategy for DC faults in multi-terminal VSC HVDC system. IET Generation Transmission and Distribution, 5(4), 496–503.View ArticleGoogle Scholar
  18. Liu, X. L., Osman, A. H., & Malik, O. P. (2011). Real-time implementation of a hybrid protection scheme for double-pole HVDC line using FPGA. IEEE Transactions on Power Delivery, 26(1), 101–108.View ArticleGoogle Scholar
  19. Liang, Y. S., Wang, G., & Li, H. F. (2015). Time-Domain Fault-Location Method on HVDC Transmission Lines Under Unsynchronized Two-End Measurement and Uncertain Line Parameters. IEEE Transactions on Power Delivery, 30(3), 1031–1038.View ArticleGoogle Scholar
  20. Azizi, S., Sanaye-Pasand, M., Abedini, M., et al. (2014). A Traveling-Wave-Based Methodology for Wide-Area Fault Location in Multiterminal DC Systems. IEEE Transactions on Power Delivery, 29(6), 2552–2560.View ArticleGoogle Scholar
  21. Nanayakkara, O. M. K. K., Rajapakse, A. D., & Wachal, R. (2012). Traveling-Wave-Based Line Fault Location in Star-Connected Multiterminal HVDC Systems. IEEE Transactions on Power Delivery, 27(4), 2286–2294.View ArticleGoogle Scholar

Copyright

© The Author(s) 2017

Advertisement