WO2015185096A1 - Appareil disjoncteur de courant continu à haute tension - Google Patents

Appareil disjoncteur de courant continu à haute tension Download PDF

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Publication number
WO2015185096A1
WO2015185096A1 PCT/EP2014/061384 EP2014061384W WO2015185096A1 WO 2015185096 A1 WO2015185096 A1 WO 2015185096A1 EP 2014061384 W EP2014061384 W EP 2014061384W WO 2015185096 A1 WO2015185096 A1 WO 2015185096A1
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WIPO (PCT)
Prior art keywords
interrupter
node
circuit breaker
capacitance
branch
Prior art date
Application number
PCT/EP2014/061384
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English (en)
Inventor
Markus Bujotzek
Angelos Garyfallos
Philipp Simka
Emmanouil Panousis
Nitesh Ranjan
Original Assignee
Abb Technology Ag
Priority date (The priority date is an assumption and is not a legal conclusion. Google has not performed a legal analysis and makes no representation as to the accuracy of the date listed.)
Filing date
Publication date
Application filed by Abb Technology Ag filed Critical Abb Technology Ag
Priority to PCT/EP2014/061384 priority Critical patent/WO2015185096A1/fr
Publication of WO2015185096A1 publication Critical patent/WO2015185096A1/fr

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Classifications

    • H—ELECTRICITY
    • H01—ELECTRIC ELEMENTS
    • H01H—ELECTRIC SWITCHES; RELAYS; SELECTORS; EMERGENCY PROTECTIVE DEVICES
    • H01H33/00—High-tension or heavy-current switches with arc-extinguishing or arc-preventing means
    • H01H33/02—Details
    • H01H33/59—Circuit arrangements not adapted to a particular application of the switch and not otherwise provided for, e.g. for ensuring operation of the switch at a predetermined point in the ac cycle
    • H01H33/596—Circuit arrangements not adapted to a particular application of the switch and not otherwise provided for, e.g. for ensuring operation of the switch at a predetermined point in the ac cycle for interrupting dc
    • H—ELECTRICITY
    • H01—ELECTRIC ELEMENTS
    • H01H—ELECTRIC SWITCHES; RELAYS; SELECTORS; EMERGENCY PROTECTIVE DEVICES
    • H01H33/00—High-tension or heavy-current switches with arc-extinguishing or arc-preventing means
    • H01H33/02—Details
    • H01H33/04—Means for extinguishing or preventing arc between current-carrying parts
    • H01H33/14—Multiple main contacts for the purpose of dividing the current through, or potential drop along, the arc
    • H01H33/143—Multiple main contacts for the purpose of dividing the current through, or potential drop along, the arc of different construction or type
    • H—ELECTRICITY
    • H01—ELECTRIC ELEMENTS
    • H01H—ELECTRIC SWITCHES; RELAYS; SELECTORS; EMERGENCY PROTECTIVE DEVICES
    • H01H33/00—High-tension or heavy-current switches with arc-extinguishing or arc-preventing means
    • H01H33/02—Details
    • H01H33/04—Means for extinguishing or preventing arc between current-carrying parts
    • H01H33/14—Multiple main contacts for the purpose of dividing the current through, or potential drop along, the arc
    • H01H2033/146—Multiple main contacts for the purpose of dividing the current through, or potential drop along, the arc using capacitors, e.g. for the voltage division over the different switches

Definitions

  • the invention relates to a circuit breaker for switching off high-voltage DC currents by employing a gas interrupter and a vacuum interrupter electrically con- nected in series to one another and an auxiliary circuit for causing a current zero required for interrupting the electric arc.
  • DC direct currents
  • MTDC multi-terminal DC networks
  • a first approach is made by breaking an HVDC current path is performed by a breaker employing semiconductor elements.
  • the drawback of such an approach resides in that the semiconductors will cause a steady loss in a closed state which steady loss lowers the overall electric efficiency.
  • the controlling of all individual switching elements is very demanding.
  • a second approach resides in circuit breaker unit having a different type of a hybrid switching elements causing less steady losses and thus allow for achieving a better overall electric efficiency than the embodiments disclosed in WO2012/084693A1 .
  • a representative of this approach is disclosed by "IEEE Transactions on Power Apparatus and Systems, Vol. PAS-103, No.3, 3 March 1984" where a vacuum interrupter and a gas interrupter are electrically con- nected in series to form an interrupter branch. A non-linear resistor and a voltage dividing capacitor are connected parallel thereto such that a voltage divider is formed.
  • This hybrid breaker unit further comprises an LC circuit electrically connected in parallel to the interrupter branch.
  • the LC circuit comprises a triggerable spark gap and a pre-charged capacitor and an inductance for injecting a counter current pulse into the interrupter branch. Since the vacuum interrupter and the gas interrupter employed in said approach are standard high voltage AC circuit breakers their movable contact members can be activated only comparatively slow such that said circuit breaker unit can be used for handling fault currents in a classic HVDC system such as a line commutated converter (LCC), for example. As a result, the circuit breaker unit of this second type is not applicable in a modern HVDC system comprising voltage source converters (VSC) requiring short switching times.
  • VSC voltage source converters
  • WO2013/014041 A1 is a further representative of the second approach.
  • a disad- vantage of this solution resides in that the gas interrupter is stressed already at the very beginning of the interruption process, i.e. at CZ. Only gas interrupters of the top range and top quality can meet such requirements. Since such gas interrupters are more complicated than standard gas interrupters they are far more expensive. Furthermore a mere upscaling to higher voltages is not possible since the voltage over the vacuum interrupter is not limited.
  • the second approach allows for upscaling the voltage over the vacuum interrupter only to some limited extent.
  • the object to be solved by the present invention resides in providing an economic circuit breaker unit that is able to protect a VSC-based HVDC system against damage from fault currents, e.g. short circuit currents.
  • HVDC is understood as a direct current with a voltage of at least 40kV, in particular more than 80kV, for example 160kV or 320kV.
  • An HVDC system can be formed by a point-to-point HVDC link or network, a multi terminal HVDC system comprising at least three stations whereof one station is provided just for tapping a HVDC current, or a so-called HVDC grid comprising a plurality of power senders and receivers.
  • fault current is understood and used herein interchangeably as the line current in case of a fault.
  • the present breaker can also be employed for interrupting a nominal current in the the nom- inal line of a HVDC system.
  • the key element for solving the above-mentioned object resides in establishing a high switching speed for preventing an excessive and thus undesired and harmful rise in current in the DC system already at an early point in time after a fault current is detected. Owing to the high switching speed the mechanical interrupters can be kept as basic as possible. This allows for profiting from existing standard AC experience and interrupting devices as well as for economic solutions.
  • the inventive HVDC circuit breaker unit comprises, an interruptible high voltage current path extending between a first node and a second node. Further it comprises an interrupter branch comprising a vacuum interrupter connected to the first node, and a gas interrupter connected to the second node of the circuit breaker unit, wherein the vacuum interrupter is connected to the circuit breaker unit at a third node such that the gas interrupter is electrically connected in series to the vacuum interrupter.
  • the interrupter branch forms the nominal current path through the circuit breaker unit.
  • a first movable contact member of the vacuum interrupter and a second movable contact member of the gas interrupter is operatable by at least one Thomson coil drive.
  • the term Thomson coil drive denotes the type of drive employing an electromagnetic repelling force and is not limited to a drive from a specific manufacturer of such drives.
  • employing a Thomson coil drive for putting the movable contact members into motion to open the interrupters is advantageous since such a drive concept allows for accelerating the movable contact members of the interrupters of the present inventive concept about at least ten times faster from trip signal compared to acceleration times from standard AC high voltage interrupters.
  • An arrestor branch is connected to the first node and the second node, wherein said arrestor branch comprises a first non-linear resistor and is electrically connected in parallel to the interrupter branch.
  • the required high acceleration of the movable contact members is achieved in that the first movable contact member and the second movable contact member are actuated by the at least one Thomson coil drive such that a line current in the interrupter branch in case of a fault can be commutated within less than 20 milliseconds from a trip signal sent to at least one of the vacuum interrupter and the gas interrupter to the arrestor branch.
  • the trip signal is understood as a signal from a control unit to at least one of the interrupters in the interrupter branch until the movable contact member is sufficiently moved to its opened position such that re-arcing is preventable in a reliable manner.
  • the trip signal is a signal from a control unit to at least one of the two interrupters to perform the switching operation.
  • the term 'within less than 20 milliseconds' is not to be misunderstood as the amount of time be- tween detection of the fault in the HVDC system and the full interruption of the fault current in the HVDC circuit breaker unit. It is not to be confused with the time until a fully open position of the interrupters is reached.
  • the term 'actuating of a movable contact member' is understood as 'putting a movable contact member from stand still into motion' throughout this document.
  • the first non-linear resistor in the arrestor branch is provided for dissipating energy from the HVDC system and thus for protecting the interrupters from harmful overvoltage due to the fault current. Since the current can increase tremendously and quickly in case of a ground fault in an HVDC system the switching speed plays a major role. The faster the HVDC circuit breaker unit interrupts the line current in the interrupter branch in case of a fault the smaller the amount of fault current to be dissipated and the smaller the required first non-linear resistor can be. Thus the faster the interruption process the lower the amount of energy the interrupter branch has to bear. As an example, said amount of energy to dissipate may be in the order of MJ/ms. Having a higher acceleration of the movable contact members and thus a higher interruption speed in the interrupters eventually contributes to minimum ex-conces for the first non-linear resistor and thus for creating a more economical circuit breaker unit because one can save on varistors.
  • Striving for shortest possible arcing times is further advantageous since it reduces the amount of contact wear. This is not only advantageous for economic reason but also for electric reasons since it reduces the risk of an electric break- down of the circuit breaker unit because sensitive arcing chamber parts of the circuit breaker unit are less exposed to wear than in circuit breaker units having longer arcing times. Furthermore, it is in general beneficial for all components of the HVDC transmission system to have as short as possible fault stress.
  • the basic embodiment of the HVDC circuit breaker unit may be adapted such that the first movable contact member of the vacuum interrupter is actuatable by a first Thomson coil drive whereas the second movable contact member of the gas interrupter is operatable by a second Thomson coil drive.
  • Dedicating separate drives to the different interrupters allows further to tailor and optimize the drives and optionally the drive gear to the different needs of the vacuum interrupter and the gas interrupter.
  • first and the second Thomson coil drive share a current source.
  • the first and the second Thomson coil drive may share a power source such as a capacitor bank or a charged capacitor.
  • a power source such as a capacitor bank or a charged capacitor.
  • An advantageous embodiment of the HVDC circuit breaker unit in terms of size versus breaking performance is achievable if the second movable contact mem- ber is actuated that fast that an insulation distance in the gas interrupter can be established in less than 10 milliseconds from the trip signal. That way said insulation distance is able to prevent re-arcing under voltage stress, i.e. to withstand the required voltage stresses.
  • a further reduction of the amount of energy from the HVDC system by way of dissipation in the arrestor branch is achievable if the second movable contact member is actuated that an insulation distance in the gas interrupter can be established in less than 7 milliseconds from the trip signal such that said insulation distance is able to prevent re-arcing under voltage stress.
  • the first movable contact member and the second movable contact member are gearless connected to the at least one Thomson coil drive. It proved that stripping all conventional drive gear known from a circuit breaker is an important measure for achieving highest acceleration values of the movable contact members.
  • One option to achieve such values resides in that the second movable contact member of the gas interrupter is rigidly connected to a piston of the second Thomson coil drive by a second drive rod along a linear switching axis. This allows for a most lean connection in between the Thomson coil drive and the dedicated movable contact member of the interrupter, for example.
  • a set of a vacuum interrupter and a gas interrupter electrically connected in se- ries has been chosen deliberately for employing their particular benefits. There are also drawbacks and limitations to both the vacuum interrupter and a gas interrupter, for example given voltage limits. A satisfactory protection of the interrupters is achievable in an embodiment where
  • a first capacitance is present between the first node and the third node
  • ⁇ a second non-linear resistor is present between the first node and the third node such that it is electrically in parallel to the first capacitance
  • the third node ensures that the overall voltage drop over the HVDC breaker unit between the first node and the second node does not need to be borne by either the vacuum interrupter or the gas interrupter alone and is achieved by dividing the overall voltage drop according to a predefined scheme established by the voltage divider. Splitting the voltage drop into shares dedicated to the vacuum interrupter and to the gas interrupter allows for establishing a purely mechanical solution that fulfills the requirements of modern HVDC systems.
  • a capacitance ratio of the first capacitance to the second capacitance needs to be dimensioned such that in case of the line current in the interrupter branch in case of a fault the vacuum interrupter carries a ma- jority of a voltage drop in between the first node and the second node in an initial stage of the interruption process until the second non-linear resistor becomes essentially conductive.
  • the gas interrupter takes over a majority of a voltage drop in between the first node and the second node in a final stage of the interruption process of the circuit breaker unit once the second non-linear resistor became essentially conductive.
  • the second non-linear resistor protects the vacuum interrupter from dielectric failure.
  • said second non-linear resistor ensures that the vacuum interrupter is electrically not overstressed. If the voltage exceeds a predefined threshold said second non-linear resistor becomes essentially conductive and protects the vacuum interrupter shortly before the transient recovery voltage (TRV) reaches the maximum voltage limit of the vacuum interrupter.
  • TRV transient recovery voltage
  • TIV transient interruption voltage
  • said second non-linear resistor ensures that the major portion of the voltage is initially dropping over the vacuum interrupter and not over the gas interrupter because the vacuum interrupter is more suitable for handling harsh di/dt and du/dt conditions at the very beginning of the interruption process than the gas interrupter because the vacuum interrupter can typically bear a higher di/dt than a gas interrupter for the same ratings.
  • the first capacitance represents the capacitance of both the vacuum interrupter itself as well as of any resistive elements including non-linear resistors and the like electrically connected in parallel to the vacuum interrupter.
  • the first ca- pacitance may comprise a dedicated capacitor, if required.
  • the second capacitance represents the capacitance of both the gas interrupter itself as well as any additional dedicated capacitance of the capacitor connected in parallel to the gas interrupter.
  • the second capacitance may comprise a dedicated capacitor, if required.
  • a good compromise between functionality and costs is achievable if the second capacitance is at least ten times as large as the first capacitance.
  • the second capacitance is dimensioned to be smaller than 1 ⁇ , preferably smaller than 100 nF as such values are regarded as a fair balance of economics and technical function to the interrupter branch. Such a second capacitance contributes to extinguishing any residual current in between the first node and the second node in an operating state of the circuit breaker unit after reaching current zero.
  • an LC circuit comprising an auxiliary switch is connected to the first node and to the second node such that the LC circuit extends parallel to the interrupter branch.
  • a triggerable spark gap for example an ABB CapThorTM
  • the LC circuit further comprises a pre-chargeable third capacitance and a first inductance, wherein the LC circuit is dimensioned such that upon closing of the auxiliary switch an oscillation is caused such that a counter- current is injectable into the interrupter branch in order to create a current zero in the interrupter branch.
  • Said third capacitance can be pre-charged by a suitable power supply or from the HVDC line.
  • a fourth capaci- tance in between the first node and the second node such that it extends over the interrupter branch.
  • Said fourth capacitance is uncharged in an initial stage of the interruption process in the circuit breaker unit. Since the charging of the fourth capacitance consumes some time the capacitance of the fourth capacitance it contributes to smoothen the slope of the initial TRV such that du/dt can be limited to a few kV/ ⁇ after CZ. Having a smoother TRV allows for some extra microseconds that are available for extinguishing the residual current from the interruption branch and for dielectric recovery of the arcing zones.
  • the fourth capacitance should be as small as possible for economic reasons but large enough to ensure proper functionality of the breaker. It is advantageous if the third capacitance is at least 4 times as large as the fourth capacitance for meeting the steepness of the slope di/dt of the TRV in order to lower the du/dt slope of the TRV. It is further advantageous and a good balance between functionality and costs that the third capacitance is charged to the HVDC system voltage.
  • the above LC circuit has been described to deal with faults that may occur both at the side of the first node as well as at the side of the second node of the circuit breaker unit once connected to the HVDC system. Since the current to be broken is an HVDC current the HVDC circuit breaker unit must be able to cope with faults regardless the polarity of the fault to zero current. Hence in the above basic em- bodiment of the LC circuit the counter current injected into the interrupter branch is always that high that it must be able to cause a reliable CZ for any faults regardless its polarity. In an exemplary embodiment the counter current for a line current in case of a fault of 10 kA with a safety margin from about 20% regardless the polarity of the fault. In continuation of the earlier example said counter current leads to a total current of about 22kA.
  • the advanced embodiment of a HVDC circuit breaker unit further comprises a further LC circuit comprising a further auxiliary switch being connected to the first node and to the second node such that the further LC circuit extends parallel to the interrupter branch.
  • a triggerable spark gap for example an ABB CapThorTM
  • the further LC circuit further comprises a pre-chargeable fifth capacitance and a second inductance, wherein the further LC circuit is dimensioned such that upon closing of the further auxiliary switch an oscillation is caused such that a counter-current is injectable into the interrupter branch in order to create a current zero in the interrupter branch.
  • Said fifth capacitance can be pre-charged by a suitable power supply analogous to the one for the third capacitor.
  • the LC circuit and the further LC circuit share their inductance, if required.
  • the first inductance and the fifth inductance may be formed by the very same electric element.
  • the first inductance can be used as the fifth inductance.
  • a disconnector to a HVDC system side at its one end and to the first node or to the second node on its other end or at both nodes of the HVDC circuit breaker unit for establishing a galvanic separation.
  • Such a galvanic separation is advantageous for preventing the arrestors of the circuit breaker unit from overheating as well as for carrying out maintenance duties.
  • the current to be interrupted by the disconnector is in the range of some Amperes only and the operating speed of the disconnector is not time critical. Depending on the embodiment the disconnector may or may not be not be part of the circuit breaker unit.
  • Fig. 1 an overall circuit of a first embodiment of the HVDC circuit breaker unit
  • Fig. 2 an embodiment illustrating the main elements of the interrupter branch
  • Fig. 3 a current-time and a voltage-time diagram of a line current and its interruption in case of a fault in the same time window around current zero;
  • Fig. 4 a current-time oscillogramme of a rising line current in an interrupter branch of the HVDC circuit breaker according to fig. 1 and a subsequent injection of a counter current into the interruption branch such that a current zero is caused;
  • Fig. 5 a voltage-time diagram showing the impact of the size of the fourth ca- pacitance extending over the HVDC circuit breaker unit.
  • Fig. 6 an overall circuit of a second embodiment of the HVDC circuit breaker unit.
  • a first embodiment of HVDC circuit breaker unit 1 is shown in fig. 1 along with fig. 2 whereas the latter figure illustrates the main elements of an interruptible interrupter branch 2 forming the nominal current path through the circuit breaker unit 1 .
  • the currents indicated in fig. 1 one has to be aware that they will not run all in the very same moment in time but they are identified in fig.1 for the sake of a better overall understanding of the different branches of the HVDC circuit breaker unit 1 and their dedicated purpose in the description.
  • Said interrupter branch 2 extends between a first node 3 and a second node 4.
  • the interrupter branch 2 comprises a vacuum interrupter 5 connected to the first node 3, and a gas interrupter 6 connected to the second node 4 of the circuit breaker unit 1 , wherein the vacuum interrupter 5 is connected to the circuit breaker unit 1 at a third node 7 such that the gas interrupter 6 is electrically connected in series to the vacuum interrupter 5.
  • An arrestor branch 8 is connected to the first node 3 and the second node 4, wherein said arrestor branch 8 comprises a first non-linear resistor 9 and is electrically connected in parallel to the interrupter branch 2.
  • a first movable contact member 1 1 of the vacuum interrupter 5 and a second movable contact member 12 of the gas interrupter 6 are actuatable by a first Thomson coil drive 13 and a second Thomson coil drive 14, respectively, such that a fault current in the HVDC system can be commutated within a few milliseconds to the arrestor branch 8 for dissipation.
  • the Thomson coil drives 13, 14 are able to accelerate all movable parts of the circuit breaker unit 1 to maximum speed from stand still within less than 7ms after a trip signal 15 is sent to at least one of the vacuum interrupter 5 and the gas interrupter 6.
  • the second movable contact member of the gas interrupter 6 is rigidly connected to a piston of the second Thomson coil drive 14 by a second drive rod along a linear switching axis 16.
  • the term rigidly connected is to be understood such that no flexible linkage such any gearing mechanism is required.
  • the circuit shown in fig. 1 has a first capacitance 17 arranged between the first node 3 and the third node 7 and a second capacitance 18 arranged between the second node 4 and the third node 7. Moreover a second non-linear resistor 19 is connected to the first node 3 and the third node 7 to be electrically parallel to the vacuum interrupter 5 and the first capacitance 17 such that a voltage divider is formed.
  • the second capacitance 18 is at least ten times as large as the first capacitance 17.
  • An LC circuit 20 comprising an auxiliary switch 21 is connected to the first node 3 and to the second node 4 such that it extends parallel to the interrupter branch 2.
  • the auxiliary switch 21 is a triggerable spark gap.
  • the LC circuit 20 also comprises a pre-chargeable third capacitance 22 and a first inductance 23 such that a resonant circuit is formed.
  • the pre-charging of the third capacitance 22 is done by means of a power supply (not shown in fig.1 ) in an operating state of the circuit breaker unit 1 .
  • the LC circuit 20 is dimensioned such that upon closing of the auxiliary switch 21 an oscillation is caused such that a counter-current 24 is injectable into the interrupter branch 2 for creating a current zero in the interrupter branch 2.
  • the second capacitance 18 is dimensioned to be below 1 ⁇ and is fifteen times as large as the first capacitance 17.
  • a fourth capacitance 25 is arranged in between the first node 3 and the second node 4 such that it extends parallel to the interrupter branch 2.
  • the fourth capacitance 20 is uncharged in an initial stage of the interruption process in the circuit breaker unit 1 .
  • the third capacitance 22 is preferably at least four times as large as the fourth capacitance 25.
  • a disconnector 26 is connected to a HVDC system side to the second node 4 for establishing a galvanic separation from the circuit breaker unit 1 to the HVDC system at the side of the second node 4.
  • Fig. 2 shows an embodiment illustrating more details of the interrupter branch 2 of the circuit breaker unit of fig .1 and represents a snapshot of the interruption branch in an initial state of the interruption process shortly after time U explained later on.
  • the display of electric arcs in between the contacts of the vacuum interrupter 5 and the gas interrupter 6 have been omittet as it would not contribute to an improved overall understandability of fig. 2.
  • the interruptible interrupter branch 2 comprises the vacuum interrupter 5 that is connected via the third node 7 in series to the gas interrupter 6.
  • the vacuum interrupter 5 has the first movable contact member 1 1 for establishing an electrical connection in between the first node 3 and the third node 7 in its closed position. Said first movable contact member 1 1 is activatable such that it moves from that closed position to an open position and vice versa by way of the first Thomson coil drive 13.
  • the gas interrupter 6 has the second movable contact member 12 for establishing an electrical connection in between the third node 7 and the second node 4 in its closed position.
  • Said second movable contact member 12 is activatable such that it moves from that closed position to an open position and vice versa by way of the second Thomson coil drive 14.
  • the first Thomson coil drive 13 and the second Thomson coil drive 14 can be activated such that their dedicated movable contacts members 1 1 and 12, respectively, get in motion by the trip signal 15 issued by the control unit 27.
  • Said control unit 27 is wired to a first current detector 28 at the first node 3 and to a second current detector 29 at the second node 4 of the HVDC system for detecting any fault current.
  • the control unit 27 is able to distinguish allowable deviations from nominal HVDC currents and fault currents.
  • Fig. 2 is simplyfied in so far as the trip signals 15 are issued to the vacuum interrupter 5 and the gas interrupter 6 in their closed state and not in their open state as shown in fig. 2.
  • first movable contact member 1 1 and the second movable contact member 12 may be actuatable by a common Thomson coil drive.
  • the control unit 27 trips the vacuum interrupter 5 and the gas interrupter 6 to open (see fig. 2).
  • the detection of the fault current takes place by conventional detection means like suitable current detectors 28, 29.
  • the detection of the fault cur- rent takes place at time to (see figures 3 and 4) where a rising line current 36 in the interrupter branch 2 departing from a nominal system current 35 is present.
  • the term nominal system current is understood as the nominal current of an HVDC system where no fault case is present such as before time to.
  • Both the gas interrupter 6 and the vacuum interrupter 5 are opened in the initial phase by the trip signal 15 at time ti and t.2 respectively.
  • the time span between ti and t.2 is in a range between 0 ms and about 3 ms.
  • the second movable contact member 12 is actuatable that fast that an insulation distance in the gas interrupter can be established in less than 7 milliseconds from the trip signal 15. Owing to the high voltage at the line current 36 in case of fault an electric arc is formed in the arcing zones of both the vacuum interrupter 5 and the gas interrupter 6 in between the movable contacts and their counter-contacts each such that a current keeps flowing in the interrupter branch 2.
  • said line current 36 entering the interrupter branch 2 from the nominal line 30 of the HVDC system rises from the nominal system current 35 constantly to about 10 kA such as shown in the lower diagram of fig. 3 as well as in fig. 4.
  • the slope of the waveform of the line current 36 is displayed as increasing in the lower diagram of fig.3.
  • the time window between U and te extends over several ten to several hundred microseconds only such that the waveform of the current 22 is displayed as being fairly constant.
  • the time window between te and tg extends over several milliseconds again such that the waveform of the line current 36 is displayed as decreasing in the lower diagram of fig.3.
  • the line current 36 in the interrupter branch 2 rises quickly, i.e. in few milliseconds up to a few kilo amperes, for example to the above-mentioned 10 kA in case of the above mentioned fault current.
  • the line current 36 in the interrupter branch 2 rises until time t.3 at which the counter-current 24 is released by closing the auxiliary switch 21 of the LC-circuit 20. Shortly thereafter the counter-current 24 injected into the interrupter branch 2 causes a CZ at time t 4 .
  • the LC circuit 20 must be able to deal with faults that may occur both at the side of the first node 3 as well as at the side of the second node 4 of the circuit breaker unit 1 in the HVDC system. Since the line current to be broken is an HVDC current the HVDC circuit breaker unit must be able to cope with faults regardless the polarity of the fault. Hence in the above basic embodiment of the LC circuit 20 the counter current 24 injected into the interrupter branch 2 is dimensioned such that it causes a reliable CZ for any faults regardless the polarity (see the total current peak 38 including the counter current 24 in fig. 4).
  • the capacitance ratio of the first capacitance 17 to the second capacitance 18 is dimensioned such that the initial voltage stress from the interruption at CZ is borne by the vacuum interrupter 5 and not by the gas interrupter 6. This is advantageous since vacuum interrupters are superior to gas interrupters in the initial phase of the interruption process because they can establish a dielectric insulation quicker. In the subsequent final stage of the interruption process the high voltage insulation is mainly done by the gas interrupter 6, since a gas interrupter is superior for that purpose as it has typically better insulation properties for higher voltages.
  • the harsh voltage step 45 of the voltage is displayed by a vertical solid line in fig. 5 is a consequence of the high di/dt of the counter current 24 measuring a few hundred Amperes per microsecond and would be too harsh for the vacuum interrupter 5 and the gas interrupter 6.
  • the initial TRV is governed by the voltage step 45 (without the fourth capacitor 25) which voltage step 45 is equal to the product of the first inductance 23 multiplied by di/dt at CZ.
  • the value of the fourth capacitor 25 has been chosen such that
  • a suffi- cient dielectric insulation is required for reliably preventing a re-arcing in the gas interrupter 6 in order to be able to take over the major portion of the voltage drop between the first node 3 and the second node 4 in the interrupter branch 2 after the limiting voltage 37 of the vacuum interrupter 5 ensured by the second non-linear resistor 19 is exceeded;
  • the TRV of the voltage across the circuit breaker unit 1 drops about the voltage step 45 after CZ and rises in the subsequent recovery phase above the system voltage 46 until the limiting volt- age level of the first non-linear resistor 9 is reached and where the first non-linear resistor 9 becomes electrically conductive such that a current 47 flows in the arrestor branch 8.
  • the first non-linear resistor 9 protects the circuit breaker unit 1 from failure of excessive line current 36 in case of fault until the system voltage 46 is reached again in that it dissipate excessive fault current energy.
  • the gas interrupter 6 Since the gas interrupter 6 has not taken over the main portion of the voltage drop across the circuit breaker unit 1 from the vacuum interrupter 5 until time te the waveform of the voltage 51 across the vacuum interrupter 5 (indicated by a dashed line 51 ) follows the one of the voltage 50 across the circuit breaker unit 1 after CZ provided that the limiting voltage levels 37 of the vacuum interrupter 5 set by the second-non-linear resistor 19 allows it.
  • the gas interrupter 6 starts taking over a portion of the voltage drop over the interrupter branch 2.
  • the time span between U and ts is employed for dielectric recovery of the gas interrupter 6.
  • the residual current 39 is present in the interrupter branch 2 from time t 4 until time ts at the latest.
  • the waveform of the voltage 52 across the gas interrupter 6 is indicated by a dotted line 52 in the upper diagram of fig. 3.
  • the voltage 51 across the vacuum interrupter 6 stagnates again because the limiting voltage levels 37 of the vacuum interrupter 5 is reached again. From time te on the gas interrupter 6 takes over the main portion of the voltage drop across the circuit breaker unit 1 from the vacuum interrupter 5.
  • the voltage across the circuit breaker unit 1 has reached the limiting voltage level 53 of the first non-linear resistor 9 where the latter starts dissipating the energy from the line current in case of the fault (i.e. the fault current) until the voltage 50 across the circuit breaker unit 1 is allowed to reach the system voltage 46 at about time tg again.
  • the stepped waveform of the voltage 52 across the gas interrupter 6 is caused by the dimensioning of the non-linear voltage divider composed by the first capacitance 17, second capacitance 18 and the second non-linear resistor 19.
  • the second non-linear resistor 19 protects the vacuum interrupter 5 against die- lectric failure in that it limits the voltage over the vacuum interrupter 5 to a voltage limit 37. As soon as the non-linear resistor 19 becomes conductive a current 43 flows through the branch with said second non-linear resistor 19, too. As can be seen in fig. 3 the voltage limit 37 of the non-linear resistor 19 is not depending on the polarity of the line current 36.
  • the voltage-time diagram of fig. 3 reveals further that the first few microseconds after CZ are decisive for the success of the whole HVDC breaking process. Any residual current 39 needs to be extinguished from the interrupter branch 2 in between time U and time ts as it hampers the dielectric recovery of the gas interrupter 6.
  • the second capacitance 18 is dimensioned to be preferably smaller than 100 nF because such a value contributes best to extinguishing any residual current 39 from the interrupter branch 2.
  • Fig. 5 is a voltage-time diagram showing the impact of a different sized fourth capacitance 25 extending over the HVDC circuit breaker unit on the TRV waveform after CZ.
  • the voltage step 45 caused by the counter current injection as well as a portion of the linear slope of a TRV (lacking a fourth capacitance) towards the system voltage are indicated by a solid line in fig. 5.
  • the voltage waveform of the actual transient recovery voltage and of the subsequent recovery voltage of a circuitry comprising a fourth capacitance 25 have been displayed by tightly dotted graphs, each.
  • a first voltage waveform 54 shows the TRV and recovery voltage of the voltage 50 across the circuit breaker unit 1 after CZ with a capacitance value C that may be 0.1 ⁇ , for example.
  • a second voltage waveform 55 shows the TRV and recovery voltage after CZ with a capacitance value of ten times the value of C.
  • a third voltage waveform 56 shows the TRV and recovery voltage after CZ with a capacitance value of a hundred times the value of C.
  • Fig. 5 shows that the larger a capacitance value for the fourth capacitance 25 the smoother the TRV slope becomes.
  • capacitors with capacitance values of a hundred times the value of C are quite costly.
  • the choice of a capacitance value for the fourth capacitance is not only a technical one as ex- plained in the context of fig. 3 but also an economic one and has an impact on the design space required (overall dimensions).
  • a second embodiment of a HVDC circuit breaker unit 100 is shown in fig. 6.
  • the circuit breaker unit 100 differs to the circuit breaker unit 1 in that it comprises a further LC circuit 60 in addition to the LC circuit 20.
  • the conceptual main differ- ence to the first embodiment shown in fig. 1 resides in that the polarity of the line current in case of a fault is detected at an early stage of the fault and in that a separate LC circuit is dedicated to each polarity of a fault current.
  • the further LC circuit 60 comprises a further auxiliary switch 61 that is connected to the first node 3 and to the second node 4 such that the further LC circuit 60 extends parallel to the interrupter branch 2.
  • the further auxiliary switch 61 forms a further triggerable spark gap.
  • the further LC circuit 60 comprises a pre-chargeable fifth capacitance 62 and makes use of the first inductance 23. A polarity of the pre-chargeable fifth capacitance 62 is opposite to the polarity of the third capacitance 22 when charged.
  • the further LC circuit 60 is dimensioned such that upon closing of the further auxiliary switch 61 an oscillation is caused such that a further counter-current 63 is injectable into the inter- rupter branch 2 in order to cause a current zero in the interrupter branch 2.

Landscapes

  • Engineering & Computer Science (AREA)
  • Power Engineering (AREA)
  • High-Tension Arc-Extinguishing Switches Without Spraying Means (AREA)

Abstract

L'invention concerne un appareil disjoncteur CCHT (1) doté d'une branche d'interrupteur (2) s'étendant entre un premier nœud (3) et un deuxième nœud (4) comprenant un interrupteur à vide (5) connecté au premier nœud (3), et un interrupteur à gaz (6) connecté au deuxième nœud (4) de l'appareil disjoncteur. L'interrupteur à vide (5) est connecté à l'appareil disjoncteur (1) au niveau d'un troisième nœud (7), de telle sorte que l'interrupteur à gaz (6) est connecté électriquement en série à l'interrupteur à vide (5). Un premier élément de contact amovible (11) de l'interrupteur à vide (5) et un second élément de contact amovible (12) de l'interrupteur à gaz (6) peuvent être actionnés par au moins une excitation de bobine Thomson. Une branche de limiteur de surtension (8) comprenant une première résistance non linéaire (9) est connectée au premier nœud (3) et au deuxième nœud (4).
PCT/EP2014/061384 2014-06-02 2014-06-02 Appareil disjoncteur de courant continu à haute tension WO2015185096A1 (fr)

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WO2019062172A1 (fr) * 2017-09-26 2019-04-04 全球能源互联网研究院有限公司 Modèle de simulation et procédé de disjoncteur à courant continu, et support de stockage
CN109888749A (zh) * 2019-03-20 2019-06-14 国网冀北电力有限公司检修分公司 一种直流断路器控制方法及装置
CN110007220A (zh) * 2019-03-28 2019-07-12 南方电网科学研究院有限责任公司 一种断路器机构运行状态诊断方法及装置
CN110224379A (zh) * 2018-03-01 2019-09-10 郑州大学 基于真空与sf6灭弧室串联的新型高压直流断路器
DE102018214806A1 (de) * 2018-08-31 2020-03-05 Siemens Aktiengesellschaft Hoch- oder Mittelspannungsschaltgerät
WO2020136340A1 (fr) 2018-12-27 2020-07-02 Supergrid Institute Dispositif de coupure de courant pour courant continu haute tension avec circuit capacitif tampon et procédé de pilotage
WO2020136350A1 (fr) 2018-12-27 2020-07-02 Supergrid Institute Dispositif de coupure de courant pour courant continu haute tension avec circuit d'oscillation adaptatif et procédé de pilotage
FR3094136A1 (fr) 2019-03-22 2020-09-25 Supergrid Institute Dispositif de coupure de courant pour courant continu haute tension avec résonateur et commutation
JP6808091B1 (ja) * 2019-10-28 2021-01-06 三菱電機株式会社 直流遮断器
CN113612193A (zh) * 2021-07-19 2021-11-05 西安交通大学 一种基于真空触发开关和超导限流的高压直流断路器及工作方法
CN113991501A (zh) * 2021-12-07 2022-01-28 西安西电高压开关有限责任公司 一种手车式中压直流断路器
WO2022208029A1 (fr) 2021-03-31 2022-10-06 Supergrid Institute Dispositif de coupure pour courant électrique sous haute tension continue avec tube à plasma

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WO2019062172A1 (fr) * 2017-09-26 2019-04-04 全球能源互联网研究院有限公司 Modèle de simulation et procédé de disjoncteur à courant continu, et support de stockage
CN110224379A (zh) * 2018-03-01 2019-09-10 郑州大学 基于真空与sf6灭弧室串联的新型高压直流断路器
DE102018214806A1 (de) * 2018-08-31 2020-03-05 Siemens Aktiengesellschaft Hoch- oder Mittelspannungsschaltgerät
US11824346B2 (en) 2018-12-27 2023-11-21 Supergrid Institute Current cut-off device for high-voltage direct current with adaptive oscillatory circuit, and control method
US11791617B2 (en) 2018-12-27 2023-10-17 Supergrid Institute Current cut-off device for high-voltage direct current with capacitive buffer circuit, and control method
WO2020136340A1 (fr) 2018-12-27 2020-07-02 Supergrid Institute Dispositif de coupure de courant pour courant continu haute tension avec circuit capacitif tampon et procédé de pilotage
WO2020136350A1 (fr) 2018-12-27 2020-07-02 Supergrid Institute Dispositif de coupure de courant pour courant continu haute tension avec circuit d'oscillation adaptatif et procédé de pilotage
FR3091408A1 (fr) 2018-12-27 2020-07-03 Supergrid Institute Dispositif de coupure de courant pour courant continu haute tension avec circuit d’oscillation adaptatif et procédé de pilotage
FR3091407A1 (fr) 2018-12-27 2020-07-03 Supergrid Institute Dispositif de coupure de courant pour courant continu haute tension avec circuit capacitif tampon et procédé de pilotage
CN109888749B (zh) * 2019-03-20 2021-04-09 国网冀北电力有限公司检修分公司 一种直流断路器控制方法及装置
CN109888749A (zh) * 2019-03-20 2019-06-14 国网冀北电力有限公司检修分公司 一种直流断路器控制方法及装置
WO2020193906A1 (fr) 2019-03-22 2020-10-01 Supergrid Institute Dispositif de coupure de courant pour courant continu haute tension avec résonateur et commutation
FR3094136A1 (fr) 2019-03-22 2020-09-25 Supergrid Institute Dispositif de coupure de courant pour courant continu haute tension avec résonateur et commutation
US11798763B2 (en) 2019-03-22 2023-10-24 Supergrid Institute Current cut-off device for high-voltage direct current with resonator and switching
CN110007220A (zh) * 2019-03-28 2019-07-12 南方电网科学研究院有限责任公司 一种断路器机构运行状态诊断方法及装置
EP4054037A4 (fr) * 2019-10-28 2022-12-14 Mitsubishi Electric Corporation Disjoncteur à cc
WO2021084585A1 (fr) * 2019-10-28 2021-05-06 三菱電機株式会社 Disjoncteur à cc
JP6808091B1 (ja) * 2019-10-28 2021-01-06 三菱電機株式会社 直流遮断器
WO2022208029A1 (fr) 2021-03-31 2022-10-06 Supergrid Institute Dispositif de coupure pour courant électrique sous haute tension continue avec tube à plasma
FR3121547A1 (fr) 2021-03-31 2022-10-07 Supergrid Institute Dispositif de coupure pour courant électrique sous haute tension continue avec tube à plasma
CN113612193B (zh) * 2021-07-19 2022-05-06 西安交通大学 一种基于真空触发开关和超导限流的高压直流断路器及工作方法
CN113612193A (zh) * 2021-07-19 2021-11-05 西安交通大学 一种基于真空触发开关和超导限流的高压直流断路器及工作方法
CN113991501A (zh) * 2021-12-07 2022-01-28 西安西电高压开关有限责任公司 一种手车式中压直流断路器
CN113991501B (zh) * 2021-12-07 2024-05-14 西安西电高压开关有限责任公司 一种手车式中压直流断路器

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