CN108509674B - Improved hybrid MMC (modular multilevel converter) operation reliability evaluation model and method - Google Patents
Improved hybrid MMC (modular multilevel converter) operation reliability evaluation model and method Download PDFInfo
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Abstract
The invention discloses an improved hybrid MMC operation reliability evaluation model and method based on multi-time scale heat damage, which mainly comprise the following steps: 1) and acquiring real-time data of the wind power transmission system. The real-time data mainly comprises wind speed, air temperature and equipment electrical parameters. 2) And establishing a reliability evaluation model of the hybrid MMC power device by utilizing the running characteristics of the hybrid MMC and a Miner's damage theory according to the original data. The power device of the wind power transmission system mainly comprises an insulated gate bipolar transistor IGBT and a crystal Diode. 3) And establishing a capacitor reliability evaluation model considering the voltage sharing of the fault SM according to the influence of the fault SM on the perfect SM capacitor. 4) And analyzing the loss distribution of the hybrid MMC device, thereby establishing an improved hybrid MMC operation reliability evaluation model considering SM multi-state. The method can be widely applied to the operation reliability evaluation of the hybrid MMC in the wind power and other renewable energy transmission grid connection.
Description
Technical Field
The invention relates to the field of wind power transmission, in particular to an improved hybrid MMC operation reliability evaluation model and method based on multi-time scale heat damage.
Background
The modular multilevel converter type high-voltage direct-current transmission (MMC-HVDC) is a power transmission mode which has great prospect for realizing the connection of a large-scale wind power station and a power grid. The Modular Multilevel Converter (MMC) has the characteristics of modular design, high output voltage quality and the like, is key equipment in the VSC-HVDC, and the operational reliability of the Modular Multilevel Converter (MMC) is related to the safe and stable operation of the VSC-HVDC. However, the MMC has large transmission power variation due to random fluctuation of wind speed, and junction temperature amplitude and fluctuation variation of a power device in the MMC are obvious due to power and air temperature fluctuation, so that the reliability of the MMC is greatly influenced. Meanwhile, along with the increasing of wind power transmission power, the voltage level of the MMC rises, MMC devices are increased gradually, and the influence of power frequency, switching frequency and other electrical parameters on the operation reliability of the MMC is increased due to the increase of the MMC devices. However, conventional equipment reliability evaluation based on statistical data ignores the influence of current operating conditions on equipment reliability, resulting in a large deviation of the reliability evaluation result from actual operation. Therefore, the influence of environmental factors and electrical parameters needs to be considered, and an MMC operation reliability evaluation model in the wind power transmission system needs to be researched.
In recent years, many researches are made on MMC reliability research at home and abroad, but MMC reliability is evaluated based on a device constant fault rate model, or the fault rate of an MMC device is corrected by introducing a voltage correction factor. However, since the failure rate of the power device is time-varying and does not satisfy the basic condition of the constant failure rate model, it is necessary to further study the MMC operation reliability evaluation model based on the failure mechanism of the power device. In engineering applications, the hybrid MMC becomes a practical application scheme at present due to its good dc fault ride-through capability and low cost.
Disclosure of Invention
The present invention is directed to solving the problems of the prior art.
The technical scheme adopted for achieving the purpose of the invention is that the improved hybrid MMC operation reliability evaluation model based on multi-time scale heat damage mainly comprises the following steps:
1) and acquiring real-time data of the wind power transmission system. The real-time data mainly comprises wind speed, air temperature and equipment electrical parameters.
2) And establishing a reliability evaluation model of the hybrid MMC power device by utilizing the running characteristics of the hybrid MMC and a Miner's damage theory according to the original data. The power device of the wind power transmission system mainly comprises an insulated gate bipolar transistor IGBT and a crystal Diode.
Further, the main steps of establishing the reliability evaluation model of the hybrid MMC power device are as follows:
2.1) calculating the multi-time scale junction temperature of the mixed MMC power device. The method mainly comprises the following steps:
2.1.1) determining the output power P of the fan of the wind power transmission systemWToutAnd a sampling time tnCorresponding to wind speed VtnThe relationship (2) of (c).
Output power P of ith fan of wind power transmission systemWTout,iAnd a sampling time tnCorresponding to wind speed VtnThe relationship of (a) is as follows:
in the formula, PratedThe rated power of the fan. Vcutin、VratedAnd VcutoutRespectively cut-in wind speed, rated wind speed and cut-out wind speed. k is a radical ofpRepresenting the coefficients related to air density and fan area. N is a radical ofWTThe total number of the fans in the wind power transmission system. n is the total number of samples up to the current operating time. t is tnIs the sampling instant. VtnIs the wind speed. i is any fan. 1, …, NWT。
Transport power P of hybrid MMCMMCoutAs follows:
in the formula, NWTThe total number of the fans in the wind power transmission system. i is any fan. 1, …, NWT。PWTout,iAnd outputting power for the ith fan.
2.1.2) calculating to obtain the mixed MMC bridge arm current according to the formula 1.
A phase upper bridge arm current IauAnd phase A lower bridge arm current IadRespectively as follows:
in the formula IdcIs a direct side current. I ismIs the ac side current peak.Is the power factor angle. f. of0Is the fundamental frequency.
Direct side current IdcAs follows:
in the formula of UdcIs the dc side voltage. PMMCoutIs the transport power of the hybrid MMC.
Peak value of AC side current ImAs follows:
in the formula, PMMCoutIs the transport power of the hybrid MMC.Is the power factor angle. U shapeacThe effective value of the AC side voltage.
2.1.3) calculating the average loss of the jth switching period of the IGBT of the upper bridge arm of the phase A.
Average loss of jth switching period of IGBT (insulated Gate Bipolar transistor) of upper bridge arm of A phaseAs follows:
in the formula, Rce、UceoAnd τTThe IGBT forward on-resistance, the threshold voltage and the duty cycle, respectively. a isT、bTAnd cTFor simulating IGBT dynamic characteristic curveAnd (5) synthesizing parameters. U shaperatedThe rated voltage of the IGBT. f. ofswAnd ρTThe switching frequency and the temperature coefficient of the IGBT, respectively. j is an arbitrary switching period. j is 1, …, nsw。nswIs the total number of switching cycles in one fundamental frequency cycle. I isauIs the phase A upper bridge arm current. U shapedcIs the dc side voltage.
Number of switching cycles nswAs follows:
nsw=fsw/f0。 (7)
in the formula (f)swThe switching frequency of the IGBT. f. of0Is the fundamental frequency.
in the formula: rd、UdAnd τDRespectively, Diode forward on-resistance, threshold voltage, and duty cycle. a isD、bDAnd cDParameters were fitted to the Diode dynamics curve. U shapeDIs a Diode rated voltage. f. ofdwAnd ρDRespectively, the switching frequency and the temperature coefficient of the Diode. I isauIs the phase A upper bridge arm current. U shapedcIs the dc side voltage.
2.1.5) calculating the junction temperature of the jth switching period of the IGBT in the hybrid MMC
in the formula (I), the compound is shown in the specification,is the sampling time tnThe corresponding air temperature.The temperature difference of an RC parallel unit in the jth switching period IGBT junction-shell heat network of the ith order. r represents an arbitrary order. r is 1,2,3, 4.The temperature difference of the RC parallel unit in the jth switching period IGBT shell-heat sink thermal network.The temperature difference of the RC parallel unit in the jth switching period IGBT heat sink-environment thermal network. j is an arbitrary switching period. j is 1, …, nsw。nswIs the total number of switching cycles in one fundamental frequency cycle.
Temperature difference of RC parallel unit in jth switching period IGBT junction-shell network of nth orderAs follows:
in the formula, RTjc,rIs the thermal resistance. Tau isTjc,rIs the thermal resistance RTjc,rThermal time constant of (2). T isswIs a switching cycle.Is the temperature difference of the RC parallel unit in the j-1 switching period IGBT junction-shell heat network of the r-th order.e is the base of the natural log function and is about 2.71828. .Average loss of the jth switching period of the IGBT of the upper bridge arm of the phase A. j is an arbitrary switching period. j is 1, …, nsw。nswIs the total number of switching cycles in one fundamental frequency cycle.
Temperature difference of RC parallel unit in jth switching period IGBT shell-heat sink networkAs follows:
in the formula, RTchIs the thermal resistance. Tau isTchIs the thermal resistance RTchThermal time constant of (2). T isswIs a switching cycle.Is the temperature difference of the RC parallel unit in the j-1 switching period IGBT shell-heat sink thermal network. e is the base of the natural log function and is about 2.71828. .Average loss of the jth switching period of the IGBT of the upper bridge arm of the phase A. j is an arbitrary switching period. j is 1, …, nsw。nswIs the total number of switching cycles in one fundamental frequency cycle.
The jth switching period IGBT is the temperature difference of RC parallel units in the radiating fin-environment networkAs follows:
in the formula, RhaIs the thermal resistance. Tau ishaIs the thermal resistance RhaThermal time constant of (2). T isswIs a switching cycle.Is the cycle temperature difference of the RC parallel unit in the j-1 th switch IGBT thermal network. j is an arbitrary switching period. j is 1, …, nsw。nswIs the total number of switching cycles in one fundamental frequency cycle.Average loss of the jth switching period of the IGBT of the upper bridge arm of the phase A.Average loss is the j-th switching period of the A-phase upper bridge arm Diode.
2.1.6) calculating the junction temperature of the j-th switching cycle of the Diode in the hybrid MMC
in the formula (I), the compound is shown in the specification,is the sampling time tnThe corresponding air temperature.The temperature difference of an RC parallel unit in a j-th switching period Diode junction-shell heat network of an r-th step. r represents an arbitrary order. r is 1,2,3, 4.For the temperature of the RC parallel unit in the j switching period Diode shell-fin heat networkAnd (4) poor.The temperature difference of the RC parallel unit in the jth switching period IGBT heat sink-environment thermal network.
j is an arbitrary switching period. j is 1, …, nsw。nswIs the total number of switching cycles in one fundamental frequency cycle.
Temperature difference of RC parallel unit in jth switching period Diode junction-shell networkAs follows:
in the formula, RDjc,rIs the thermal resistance. Tau isDjc,rIs the thermal resistance RDjc,rThermal time constant of (2). T isdwIs a switching cycle.Is the temperature difference of the RC parallel unit in the j-1 switching period Diode junction-shell heat network. j is an arbitrary switching period. j is 1, …, nsw。nswIs the total number of switching cycles in one fundamental frequency cycle.Average loss is the j-th switching period of the A-phase upper bridge arm Diode.
Temperature difference of RC parallel unit in jth switching period Diode shell-fin networkAs follows:
in the formula, RDchIs the thermal resistance. Tau isDchIs the thermal resistance RDchHot time ofA constant. T isswIs a switching cycle.Is the temperature difference of the RC parallel unit in the j-1 switching period Diade shell-fin heat network.Average loss is the j-th switching period of the A-phase upper bridge arm Diode. j is 1, …, nsw。nswIs the total number of switching cycles in one fundamental frequency cycle.
2.2) hybrid MMC power device multi-time scale reliability evaluation. The method mainly comprises the following steps:
2.2.1) calculating the cycle failure period number N corresponding to the low-frequency period of the IGBTTf_L. Number of cycles to failure NTf_LAs follows:
in the formula, tonThe heating time is shown. U is 0.01 times the block voltage of the module. D is the diameter of the aluminum bonding wire. k is 9.3 × 1014。β1=-4.416。β2=1285。β3=-0.463。β4=-0.716。β5=-0.761。β6=-0.5。TTjmax_LAnd the maximum value of the low-frequency junction temperature of the IGBT. T isTjmin_LAnd the minimum value of the low-frequency junction temperature of the IGBT. I isLThe effective value of the current of the IGBT low-frequency aluminum bonding wire is obtained. e is the base of the natural log function and is about 2.71828. . Cycle failure period number N corresponding to IGBT fundamental frequency periodTf_FAs follows:
in the formula, tonThe heating time is shown. U is 0.01 times the block voltage of the module. D is the diameter of the aluminum bonding wire. k is 9.3 × 1014。β1=-4.416。β2=1285。β3=-0.463。β4=-0.716。β5=-0.761。β6=-0.5。TTjmax_FAnd the maximum value of the junction temperature of the IGBT fundamental frequency. T isTjmin_FAnd the minimum value of the IGBT fundamental frequency junction temperature is obtained. I isFThe effective value of the current of the IGBT fundamental frequency aluminum bonding wire is obtained. e is the base of the natural log function and is about 2.71828. .
According to Miner's damage theory and formula (17), IGBT is in 0-tnTime of day life consumption CLT(tn) As follows:
in the formula, NTsum_LIs 0-tnThe total number of low frequency thermal cycles at that time. N is a radical ofT_L,gAnd NTf_L,gThe number of thermal cycles and the number of cycle failure cycles corresponding to the g-th low-frequency thermal cycle of the IGBT are respectively. N is a radical ofT_F,qAnd NTf_F,qAnd respectively obtaining the fundamental frequency thermal cycle times and the cycle failure cycles corresponding to the q-th sampling time interval T of the IGBT. n is the total number of samples up to the current operating time. N is a radical ofTsum_LIs the total number of low frequency thermal cycles.
IGBT sampling time tnMean time to failure MTTF corresponding to time interval TT(tn) As follows:
in the formula, CLT(tn) Is IGBT at 0-tnThe lifetime of the moment is consumed. T is the sampling time interval.
IGBT failure rate lambdaT(tn) As follows:
in the formula, MTTFT(tn) For the IGBT sampling time tnCorresponding to the average time to failure of time interval T.
IGBT reliability RT(tn)As follows:
in the formula, λT(tn) Is the IGBT failure rate. t is tnIs the sampling instant.
2.2.2) calculating the cycle failure number N corresponding to the low-frequency period of the DiodeDf_L. Number of cycles to failure NDf_LAs follows:
in the formula, tonThe heating time is shown. U is 0.01 times the block voltage of the module. D is the diameter of the aluminum bonding wire. k is 9.3 × 1014。β1=-4.416。β2=1285。β3=-0.463。β4=-0.716。β5=-0.761。β6=-0.5。TDjmax_LIs the Diode low frequency junction temperature maximum. T isDjmin_LIs the Diode low frequency junction temperature minimum. I isDLThe effective value of the current of the Diode low-frequency aluminum bonding wire is obtained.
Number of cycle failure cycles N corresponding to the period of the Diode fundamental frequencyDf_FAs follows:
in the formula, tonThe heating time is shown. U is 0.01 times the block voltage of the module. D is the diameter of the aluminum bonding wire. k is 9.3 × 1014。β1=-4.416。β2=1285。β3=-0.463。β4=-0.716。β5=-0.761。β6=-0.5。TDjmax_FIs the Diode fundamental frequency junction temperature maximum. T isDjmin_FIs the Diode fundamental frequency junction temperature minimum. I isDFThe effective value of the current of the Diode fundamental frequency aluminum bonding wire is obtained.
According to Miner's theory of injuryEquation (23), the Diade is between 0 and tnTime of day life consumption CLD(tn) As follows:
in the formula, NDsum_LIs a Diode at 0-tnTotal number of low frequency thermal cycles at the moment. N is a radical ofD_L,αAnd NDf_L,αThe number of thermal cycles and the number of cycle failure cycles corresponding to the alpha-th low-frequency thermal cycle of the Diode are respectively. N is a radical ofD_F,ωAnd NDf_F,ωThe thermal cycle number of the fundamental frequency and the cycle failure cycle number corresponding to the omega th sampling time interval T are respectively. n is the total number of samples up to the current operating time.
The Diode sampling time tnMean time to failure MTTF corresponding to time interval TD(tn) As follows:
in the formula, CLD(tn) Is a Diode at 0-tnThe lifetime of the moment is consumed. T is the sampling time interval.
Diade failure rate λD(tn) As follows:
in the formula, MTTFD(tn) For the moment t of the Diade samplingnCorresponding to the average time to failure of time interval T.
Diade reliability RD(tn) is as follows:
in the formula, λD(tn) Is the Diode failure rate. e is a natural logarithmic functionAbout 2.71828. . t is tnIs the sampling instant.
3) And establishing a hybrid MMC capacitor reliability evaluation model considering the voltage sharing of the fault SM according to the influence of the fault SM on the perfect SM capacitor.
Further, the main steps of establishing the reliability evaluation model of the hybrid MMC capacitor are as follows:
3.1) calculating the capacitor reliability RC(tn) Namely:
in the formula, λcIs the capacitor failure rate. Ws0Is in an initial state. WsiSelf-healing energy corresponding to i SM faults. t is tnIs the sampling instant.
Self-healing energy WsiAs follows:
UCicapacitor voltage for i SM faults. RCIs a sheet resistance. C is capacitance. And f (P) is a sandwich pressure related function. k is a radical ofcTo calculate the correlation coefficient of the self-healing energy. a is the capacitor correlation coefficient. And b is the resistance correlation coefficient.
3.2) according to the capacitor reliability RC(tn) The hybrid MMC capacitor reliability was evaluated.
4) And analyzing the loss distribution of the hybrid MMC device, thereby establishing an improved hybrid MMC operation reliability evaluation model considering SM multi-state.
Further, the main steps of establishing the hybrid MMC operation reliability evaluation model considering SM multi-state are as follows:
4.1) calculating the reliability of the SM multi-state. The SM main circuit consists of an IGBT, a Diode and a capacitor.
According to the combination relation of IGBT, Diode and capacitor in SM, CSSM reliability R under intact stateCSu(tn) As follows:
RCSu(tn)=RT1(tn)·RD1(tn)·RT2(tn)·RD2(tn)·RT3(tn)·RD3(tn)·RC(tn)。 (30)
in the formula, RT1(tn)、RT2(tn) And RT3(tn) Reliability of the first IGBT, the second IGBT and the third IGBT, respectively. RD1(tn)、RD2(tn) And RD3(tn) Reliability of the first, second and third Diode, respectively. Rc(tn) The reliability of the capacitor.
HBSM reliability R in good conditionHBu(tn) As follows:
RHBu(tn)=RT1(tn)·RD1(tn)·RT2(tn)·RD2(tn)·RC(tn)。 (31)
in the formula, RT1(tn)、RT2(tn) And RT3(tn) Reliability of the first IGBT, the second IGBT and the third IGBT, respectively. RD1(tn)、RD2(tn) And RD3(tn) Reliability of the first, second and third Diode, respectively. Rc(tn) The reliability of the capacitor.
Reliability R of CSSM under half fault conditionCSp(tn) As follows:
RCSp(tn)=RT1(tn)·RD1(tn)·RT2(tn)·RD2(tn)·(1-RT3(tn)·RD3(tn))·RC(tn)。 (32)
in the formula, RT1(tn)、RT2(tn) And RT3(tn) Reliability of the first IGBT, the second IGBT and the third IGBT, respectively. RD1(tn)、RD2(tn) And RD3(tn) Reliability of the first, second and third Diode, respectively. Rc (t)n) The reliability of the capacitor.
4.2) accounting for SM multistate hybrid MMC reliability
The reliability of the bridge arm is mainly divided into two cases.
The first case is: when neither CSSM nor HBSM damaged number exceeds its own redundancy number, iCS≤MCSAnd i isHB≤MHBMeanwhile, the hybrid MMC normally operates.
According to a binomial distribution probability formula, in the first case, the total CSSM reliability R of the upper bridge armCSs1(tn) As follows:
in the formula, NCSIs the baseline number of CSSM. RCSu(tn) The CSSM reliability in good condition. i.e. icsIs the number of CSSM damages. MCSIs the redundancy number of the CSSM.
In the first case, the total HBSM reliability R of the upper bridge armHBs1(tn) As follows:
in the formula, NHBThe baseline number for the HBSM. RHBu(tn) The HBSM reliability in the intact state. i.e. iHBIs the number of HBSM breakages. MHBIs the redundancy number of the HBSM.
Based on the series relation between CSSM and HBSM in bridge arm, the reliability R of single-phase upper bridge arm under the first conditionArm_u1(tn) As follows:
RArm_u1(tn)=RCSs1(tn)·RHBs1(tn)。 (35)
in the formula, RHBs1(tn) The total HBSM reliability for the upper arm in the first case. RCSs1(tn) The total CSSM reliability for the upper leg in the first case.
The second case is: when the CSSM defect number does not exceed the self-redundancy number, the HBSM defect number exceeds the self-redundancy number, and the good and half-fault CSSMs replace the damaged HBSM, i.e., iCS≤MCSAnd M isHB<iHB≤MHB+MCS-(iCS-iCSp) Meanwhile, the hybrid MMC normally operates. i.e. iCSpIs the CSSM half-fault number.
According to a polynomial distribution probability formula, the total CSSM reliability R of the upper bridge armCSs2(tn) As follows:
in the formula iCSpIs the CSSM half-fault number. N is a radical ofCSIs the baseline number of CSSM. RCSu(tn) The CSSM reliability in good condition. i.e. icsIs the number of CSSM damages. McsIs the redundancy number of the CSSM. RCSp(tn) Reliability of the half fault state CSSM.
Based on the serial connection relation of all HBSM in the bridge arms and according to a binomial distribution probability formula, the total HBSM reliability R of the upper bridge armHBs2(tn) As follows:
in the formula iCSpIs the CSSM half-fault number. i.e. icsIs the number of CSSM damages. N is a radical ofHBThe baseline number for the HBSM. RHBu(tn)The HBSM reliability in the intact state. i.e. iHBIs the number of HBSM breakages. MHBIs the redundancy number of the HBSM.
Based on the series connection of CSSM and HBSM in the bridge arm, the second caseReliability R of single-phase upper bridge arm under conditionArm_u2(tn) As follows:
RArm_u2(tn)=RCSs2(tn)·RHBs2(tn)。 (38)
in the formula, RHBs2(tn) The total HBSM reliability for the upper arm in the second case. RCSs2(tn) The overall CSSM reliability for the upper leg in the second case.
Reliability function R of single-phase upper bridge armArm_u(tn)As follows:
RArm_u(tn)=RArm_u1(tn)+RArm_u2(tn)。 (39)
in the formula, RArm_u1(tn) The single-phase upper arm reliability in the first case. RArm_u2(tn) The reliability of the single-phase upper bridge arm in the second condition.
Based on the symmetry of the mixed MMC and the series relation of each bridge arm, the reliability R (t) of the mixed MMCn) As follows:
R(tn)=RArm_u(tn)6。 (40)
in the formula, RArm_u(tn) Is a single-phase upper bridge arm reliability function.
A method for using an improved hybrid MMC operational reliability assessment model based on multi-time scale thermal damage, comprising the steps of:
I) data is input in the improved hybrid MMC operational reliability evaluation model. The data mainly comprises environmental parameters and mixed MMC and fan electrical parameters. The environmental parameters mainly comprise wind speed VtnAnd air temperature Ta,tn. The hybrid MMC and wind turbine electrical parameters mainly comprise switching frequency fswThe hybrid MMC comprises a direct current side rated voltage, an alternating current side rated voltage, a power factor, a modulation ratio and a duty ratio.
II) according to the input data, the improved hybrid MMC operation reliability evaluation model calculates the loss of the power device. I.e. calculating samplesTime tnAverage loss P of IGBT switching period in corresponding time interval TT,avgAnd the average loss P of the switching period of the DiodeD,avg。
III) according to the input data, the improved hybrid MMC operation reliability evaluation model calculates the multi-time scale junction temperature of the power device.
Calculating the sampling time tnJunction temperature mean value T of IGBT fundamental frequency period within corresponding time interval TTjavg_FMaximum value TTjmax_FMinimum value TTjmin_FAnd effective value of current I of aluminum bonding wireF. Calculating 0-t according to the rain flow algorithmnMaximum T of junction temperature curve of IGBT low-frequency period at momentTjmax_LMinimum value TTjmin_LAnd effective value of current I of aluminum bonding wireL。
IV) according to the input data, the improved hybrid MMC operation reliability evaluation model calculates the service life consumption, the average failure time and the failure rate of the power device and the multi-time scale.
Calculating the number N of low-frequency cyclic failure cycles of the IGBTTf_LAnd the number N of cycles of failure of fundamental frequency cycleTf_FThereby obtaining the IGBT at 0-tnTime of day life consumption CLT(tn) Sampling time tnMean time to failure MTTF corresponding to time interval TT(tn) Failure rate λT(tn) And degree of reliability RT(tn)。
Calculating the number N of low-frequency cycle failure cycles of the DiodeDf_LAnd the number N of cycles of failure of fundamental frequency cycleDf_FThus obtaining a Diode in the range of 0-tnTime of day life consumption CLD(tn) Sampling time tnMean time to failure MTTF corresponding to time interval TD(tn) Failure rate λD(tn) And degree of reliability RD(tn)。
V) according to the input data, the improved mixed MMC operation reliability evaluation model calculates the reliability R of the capacitorC(tn)。
VI) based on the input data, the improved hybrid MMC operational reliability assessment model calculates and accounts for the reliability of the SM multi-state hybrid MMCDegree R (t)n) Thereby evaluating the reliability of improving the operation of the hybrid MMC.
The technical effect of the present invention is undoubted. The invention focuses on researching the coupling relation between the reliability of the hybrid MMC and the wind speed, the air temperature and the internal parameters of the electrical equipment, comprehensively considers the influence of the environmental factors such as the wind speed, the air temperature, the power frequency and the like and the electrical parameters on the operation reliability of the hybrid MMC from the failure mechanism of a device, and can effectively reflect the influence of the environmental factors and the internal electrical parameters of the equipment on the operation reliability of the hybrid MMC. The method couples the operational reliability of the hybrid MMC with the environmental factors and the electrical parameters, optimizes the topology of the hybrid MMC from the operation angle on the basis of loss, accurately describes the relationship between the operational reliability of the hybrid MMC and the environmental factors and the electrical parameters, and improves the operational reliability level of the hybrid MMC. Based on the running characteristic of the hybrid MMC, the invention provides a measure for reusing the fault SM aiming at the problem that the loss distribution of the SM in the hybrid MMC is seriously uneven, thereby improving the utilization rate of the SM in the hybrid MMC and achieving the effect of improving the running reliability of the hybrid MMC. The method can be widely applied to the operation reliability evaluation of the hybrid MMC in the wind power and other renewable energy transmission grid connection.
Drawings
FIG. 1 is a diagram of a hybrid MMC topology;
FIG. 2 is an HBSM topology;
FIG. 3 is a CSSM topology;
FIG. 4 is an annual wind speed data curve;
FIG. 5 is a plot of annual air temperature data;
FIG. 6 is a mixed MMC reliability curve before and after modification;
FIG. 7 is a hybrid MMC reliability curve;
FIG. 8 is an SM failure rate curve;
FIG. 9 is a graph of hybrid MMC reliability as a function of switching frequency and time.
Detailed Description
The present invention is further illustrated by the following examples, but it should not be construed that the scope of the above-described subject matter is limited to the following examples. Various substitutions and alterations can be made without departing from the technical idea of the invention and the scope of the invention is covered by the present invention according to the common technical knowledge and the conventional means in the field.
Example 1:
an improved hybrid MMC operation reliability evaluation model based on multi-time scale heat damage mainly comprises the following steps:
1) and acquiring real-time data of the wind power transmission system. The real-time data mainly comprises wind speed, air temperature and equipment electrical parameters.
2) And establishing a reliability evaluation model of the hybrid MMC power device by utilizing the running characteristics of the hybrid MMC and a Miner's damage theory according to the original data. The power device of the wind power transmission system mainly comprises an insulated gate bipolar transistor IGBT and a crystal Diode.
Further, the hybrid MMC topology mainly includes three a, b, c three phase cells.
The a-phase units are sequentially connected in series with NCSCSSM module and NHBAnd each HBSM module.
The b-phase units are sequentially connected in series with NCSCSSM module and NHBAnd each HBSM module.
The c-phase units are sequentially connected in series with NCSCSSM module and NHBAnd each HBSM module.
The HBSM is composed of power modules T1, T2, and a capacitor C.
The CSSM is comprised of power modules T1, T2, T3, and a capacitor C.
Preferably, the MMC topology structure may be an upper bridge arm and a lower bridge arm each formed by connecting N sub-modules and 1 bridge arm reactance L in series, where SM is formed by 2 switching devices and 1 energy storage capacitor. Each SM can be in 3 operative states of plunge, cut and latch.
Further, the main steps of establishing the reliability evaluation model of the hybrid MMC power device are as follows:
2.1) calculating the multi-time scale junction temperature of the mixed MMC power device. The method mainly comprises the following steps:
2.1.1) determining the output power P of the fan of the wind power transmission systemWToutAnd a sampling time tnCorresponding to wind speed VtnThe relationship (2) of (c).
Output power P of ith fan of wind power transmission systemWTout,iAnd a sampling time tnCorresponding to wind speed VtnThe relationship of (a) is as follows:
in the formula, PratedThe rated power of the fan. Vcutin、VratedAnd VcutoutRespectively cut-in wind speed, rated wind speed and cut-out wind speed. k is a radical ofpRepresenting the coefficients related to air density and fan area. N is a radical ofWTThe total number of the fans in the wind power transmission system. n is the total number of samples up to the current operating time. t is tnIs the sampling instant. VtnIs the wind speed. i is any fan. 1, …, NWT。
Transport power P of hybrid MMCMMCoutAs follows:
in the formula, NWTThe total number of the fans in the wind power transmission system. i is any fan. 1, …, NWT。PWTout,iAnd outputting power for the ith fan.
2.1.2) calculating to obtain the mixed MMC bridge arm current according to the formula 1.
A phase upper bridge arm current IauAnd phase A lower bridge arm current IadRespectively as follows:
in the formula IdcIs a direct side current. I ismIs the ac side current peak.Is the power factor angle. f. of0Is the fundamental frequency.
Direct side current IdcAs follows:
in the formula of UdcIs the dc side voltage. PMMCoutIs the transport power of the hybrid MMC.
Peak value of AC side current ImAs follows:
in the formula, PMMCoutIs the transport power of the hybrid MMC.Is the power factor angle. U shapeacThe effective value of the AC side voltage.
2.1.3) calculating the average loss of the jth switching period of the IGBT of the upper bridge arm of the phase A.
Average loss of jth switching period of IGBT (insulated Gate Bipolar transistor) of upper bridge arm of A phaseAs follows:
in the formula, Rce、UceoAnd τTThe IGBT forward on-resistance, the threshold voltage and the duty cycle, respectively. a isT、bTAnd cTAnd fitting parameters for the IGBT dynamic characteristic curve. U shaperatedThe rated voltage of the IGBT. f. ofswAnd ρTThe switching frequency and the temperature coefficient of the IGBT, respectively. j is an arbitrary switching period. j is 1, …, nsw。nswIs the total number of switching cycles in one fundamental frequency cycle. I isauIs the phase A upper bridge arm current. U shapedcIs the dc side voltage.
Number of switching cycles nswAs follows:
nsw=fsw/f0。 (7)
in the formula (f)swThe switching frequency of the IGBT. f. of0Is the fundamental frequency.
in the formula: rd、UdAnd τDRespectively, Diode forward on-resistance, threshold voltage, and duty cycle. a isD、bDAnd cDParameters were fitted to the Diode dynamics curve. U shapeDIs a Diode rated voltage. f. ofdwAnd ρDRespectively, the switching frequency and the temperature coefficient of the Diode. I isauIs the phase A upper bridge arm current. U shapedcIs the dc side voltage.
2.1.5) calculating the junction temperature of the jth switching period of the IGBT in the hybrid MMCThe loss of the hybrid MMC power device causes the junction temperature of the device to rise, and the junction temperature of the power module can be effectively calculated by constructing a foster heat network model.
in the formula (I), the compound is shown in the specification,is the sampling time tnThe corresponding air temperature.The temperature difference of an RC parallel unit in the jth switching period IGBT junction-shell heat network of the ith order. r represents an arbitrary order. r is 1,2,3, 4.The temperature difference of the RC parallel unit in the jth switching period IGBT shell-heat sink thermal network.The temperature difference of the RC parallel unit in the jth switching period IGBT heat sink-environment thermal network. j is an arbitrary switching period. j is 1, …, nsw。nswIs the total number of switching cycles in one fundamental frequency cycle.
Temperature difference of RC parallel unit in jth switching period IGBT junction-shell network of nth orderAs follows:
in the formula, RTjc,rIs the thermal resistance. Tau isTjc,rIs the thermal resistance RTjc,rThermal time constant of (2). T isswIs a switching cycle.Is the temperature difference of the RC parallel unit in the j-1 switching period IGBT junction-shell heat network of the r-th order. e is the base of the natural log function and is about 2.71828. .Average loss of the jth switching period of the IGBT of the upper bridge arm of the phase A. j is an arbitrary switching period. j is 1, …, nsw。nswIs the total number of switching cycles in one fundamental frequency cycle.
Temperature difference of RC parallel unit in jth switching period IGBT shell-heat sink networkAs follows:
in the formula, RTchIs the thermal resistance. Tau isTchIs the thermal resistance RTchThermal time constant of (2). T isswIs a switching cycle.Is the temperature difference of the RC parallel unit in the j-1 switching period IGBT shell-heat sink thermal network. e is the base of the natural log function and is about 2.71828. .Average loss of the jth switching period of the IGBT of the upper bridge arm of the phase A. j is an arbitrary switching period. j is 1, …, nsw。nswIs the total number of switching cycles in one fundamental frequency cycle.
The jth switching period IGBT is the temperature difference of RC parallel units in the radiating fin-environment networkAs follows:
in the formula, RhaIs the thermal resistance. Tau ishaIs the thermal resistance RhaThermal time constant of (2). T isswIs a switching cycle.Is the cycle temperature difference of the RC parallel unit in the j-1 th switch IGBT thermal network. j is an arbitrary switching period. j is 1, …, nsw。nswIs the total number of switching cycles in one fundamental frequency cycle.Average loss of the jth switching period of the IGBT of the upper bridge arm of the phase A.Average loss is the j-th switching period of the A-phase upper bridge arm Diode.
Because the power frequency and other electrical parameters of different switching periods are different, the electrical parameters are reflected in the fundamental frequency junction temperature of a short time scale. 0-tnThe time instant comprises n sampling time intervals T, where TnCorresponding to a sampling time interval T having NT_FOne period of fundamental frequency (N)T_F=T×f0) The ith fundamental frequency period (i ═ 1, …, NT_F) And taking the temperature difference of the RC parallel unit as an iterative variable to obtain a junction temperature curve of the fundamental frequency period, and further obtain a junction temperature mean value T corresponding to the fundamental frequency periodTjavg_FMaximum value TTjmax_FMinimum value TTjmin_FAnd effective value of current I of aluminum bonding wireFAnd the method is used for evaluating the reliability of the IGBT fundamental frequency time scale. Assuming that the wind speed and air temperature are constant within a sampling time interval T, then N isT_FT of one fundamental frequency periodTjavg_F、TTjmax_F、TTjmin_FAnd IFAnd therefore, the junction temperature parameter of one fundamental frequency period can be extracted.
The wind speed and air temperature at different sampling time intervals T are different and are reflected in the low-frequency junction temperature of a long time scale. According to 0-tnMean value T of junction temperature of fundamental frequency of each sampling time interval T at momentTjavg_FObtaining N by rain flow algorithmTsum_LObtaining a low-frequency period junction temperature curve, and further obtaining a g-th low-frequency period junction temperature curve (g is 1, …, N)Tsum_L) Corresponding maximum value of junction temperature TTjmax_LMinimum value TTjmin_LAnd effective value of current I of aluminum bonding wireLAnd the method is used for evaluating the reliability of the IGBT low-frequency time scale.
2.1.6) calculating the junction temperature of the j-th switching cycle of the Diode in the hybrid MMC
in the formula (I), the compound is shown in the specification,is the sampling time tnThe corresponding air temperature.The temperature difference of an RC parallel unit in a j-th switching period Diode junction-shell heat network of an r-th step. r represents an arbitrary order. r is 1,2,3, 4.The temperature difference of the RC parallel units in the j switching period Diode shell-fin heat network.The temperature difference of the RC parallel unit in the jth switching period IGBT heat sink-environment thermal network. j is an arbitrary switching period. j is 1, …, nsw。nswIs the total number of switching cycles in one fundamental frequency cycle. Because the temperature difference of the RC parallel unit in the jth switching period IGBT radiating fin-environment heat network and the temperature difference of the RC parallel unit in the jth switching period Diode radiating fin-environment heat network are equal in value, in order to simplify the calculation steps, the Diode junction temperature is calculatedIn time, the temperature difference can be directly used
Temperature difference of RC parallel unit in jth switching period Diode junction-shell networkAs follows:
in the formula, RDjc,rIs the thermal resistance. Tau isDjc,rIs the thermal resistance RDjc,rThermal time constant of (2). T isdwIs a switching cycle.Is the temperature difference of the RC parallel unit in the j-1 switching period Diode junction-shell heat network. j is an arbitrary switching period. j is 1, …, nsw。nswIs the total number of switching cycles in one fundamental frequency cycle.Average loss is the j-th switching period of the A-phase upper bridge arm Diode.
Temperature difference of RC parallel unit in jth switching period Diode shell-fin networkAs follows:
in the formula, RDchIs the thermal resistance. Tau isDchIs the thermal resistance RDchThermal time constant of (2). T isswIs a switching cycle.Is the temperature difference of the RC parallel unit in the j-1 switching period Diade shell-fin heat network.Average loss is the j-th switching period of the A-phase upper bridge arm Diode. j is 1, …, nsw。nswIs the total number of switching cycles in one fundamental frequency cycle.
2.2) hybrid MMC power device multi-time scale reliability evaluation. In the reliability evaluation of the hybrid MMC power device, the influence of environmental factors such as wind speed and air temperature and electrical parameters such as power frequency on the reliability of the power device is quantified by taking the low-frequency junction temperature and the fundamental-frequency junction temperature of the power device into consideration, so that the reliability evaluation precision of the power device is improved.
The method mainly comprises the following steps:
2.2.1) calculating the cycle failure period number N corresponding to the low-frequency period of the IGBTTf_L. Number of cycles to failure NTf_LAs follows:
in the formula, tonThe heating time is shown. U is 0.01 times the block voltage of the module. D is the diameter of the aluminum bonding wire. k is 9.3 × 1014。β1=-4.416。β2=1285。β3=-0.463。β4=-0.716。β5=-0.761。β6=-0.5。TTjmax_LAnd the maximum value of the low-frequency junction temperature of the IGBT. T isTjmin_LAnd the minimum value of the low-frequency junction temperature of the IGBT. I isLThe effective value of the current of the IGBT low-frequency aluminum bonding wire is obtained. e is the base of the natural log function and is about 2.71828. . Cycle failure period number N corresponding to IGBT fundamental frequency periodTf_FAs follows:
in the formula, tonThe heating time is shown. U is 0.01 times the block voltage of the module. D is the diameter of the aluminum bonding wire. k is 9.3 × 1014。β1=-4.416。β2=1285。β3=-0.463。β4=-0.716。β5=-0.761。β6=-0.5。TTjmax_FAnd the maximum value of the junction temperature of the IGBT fundamental frequency. T isTjmin_FAnd the minimum value of the IGBT fundamental frequency junction temperature is obtained. I isFThe effective value of the current of the IGBT fundamental frequency aluminum bonding wire is obtained. e is the base of the natural log function and is about 2.71828. .
According to Miner's damage theory and formula (17), IGBT is in 0-tnTime of day life consumption CLT(tn) As follows:
in the formula, NTsum_LIs 0-tnThe total number of low frequency thermal cycles at that time. N is a radical ofT_L,gAnd NTf_L,gThe number of thermal cycles and the number of cycle failure cycles corresponding to the g-th low-frequency thermal cycle of the IGBT are respectively. N is a radical ofT_F,qAnd NTf_F,qAnd respectively obtaining the fundamental frequency thermal cycle times and the cycle failure cycles corresponding to the q-th sampling time interval T of the IGBT. n is the total number of samples up to the current operating time. N is a radical ofTsum_LIs the total number of low frequency thermal cycles.
Preferably, the Miner's damage theory mainly needs to calculate the damage caused by one cycle and N under the constant-amplitude loadTsum_LDamage caused by individual cycles, N under variable amplitude loadTsum_LDamage caused by one cycle.
IGBT sampling time tnMean time to failure MTTF corresponding to time interval TT(tn) As follows:
in the formula, CLT(tn) Is IGBT at 0-tnThe lifetime of the moment is consumed. T is the sampling time interval.
IGBT failure rate lambdaT(tn) As follows:
in the formula, MTTFT(tn) For the IGBT sampling time tnCorresponding to the average time to failure of time interval T.
IGBT reliability RT(tn) As follows:
in the formula, λT(tn) Is the IGBT failure rate. t is tnIs the sampling instant.
2.2.2) calculating the cycle failure number N corresponding to the low-frequency period of the DiodeDf_L. Number of cycles to failure NDf_LAs follows:
in the formula, tonThe heating time is shown. U is 0.01 times the block voltage of the module. D is the diameter of the aluminum bonding wire. k is 9.3 × 1014。β1=-4.416。β2=1285。β3=-0.463。β4=-0.716。β5=-0.761。β6=-0.5。TDjmax_LIs the Diode low frequency junction temperature maximum. T isDjmin_LIs the Diode low frequency junction temperature minimum. I isDLThe effective value of the current of the Diode low-frequency aluminum bonding wire is obtained.
Number of cycle failure cycles N corresponding to the period of the Diode fundamental frequencyDf_FAs follows:
in the formula, tonThe heating time is shown. U is 0.01 times the block voltage of the module. D is the diameter of the aluminum bonding wire. k is 9.3 × 1014。β1=-4.416。β2=1285。β3=-0.463。β4=-0.716。β5=-0.761。β6=-0.5。TDjmax_FIs the Diode fundamental frequency junction temperature maximum. T isDjmin_FIs the Diode fundamental frequency junction temperature minimum. I isDFThe effective value of the current of the Diode fundamental frequency aluminum bonding wire is obtained.
According to Miner's injury theory and equation (23), the Diode is at 0-tnTime of day life consumption CLD(tn) As follows:
in the formula, NDsum_LIs a Diode at 0-tnTotal number of low frequency thermal cycles at the moment. N is a radical ofD_L,αAnd NDf_L,αThe number of thermal cycles and the number of cycle failure cycles corresponding to the alpha-th low-frequency thermal cycle of the Diode are respectively. N is a radical ofD_F,ωAnd NDf_F,ωThe thermal cycle number of the fundamental frequency and the cycle failure cycle number corresponding to the omega th sampling time interval T are respectively. n is the total number of samples up to the current operating time.
The Diode sampling time tnMean time to failure MTTF corresponding to time interval TD(tn) As follows:
in the formula, CLD(tn) Is a Diode at 0-tnThe lifetime of the moment is consumed. T is the sampling time interval.
Diade failure rate λD(tn) As follows:
in the formula, MTTFD(tn) For the moment t of the Diade samplingnCorresponding to the average time to failure of time interval T.
Diade reliability RD(tn) is as follows:
in the formula, λD(tn) Is the Diode failure rate. e is the base of the natural log function and is about 2.71828. . t is tnIs the sampling instant.
3) And establishing a hybrid MMC capacitor reliability evaluation model considering the voltage sharing of the fault SM according to the influence of the fault SM on the perfect SM capacitor.
Further, the main steps of establishing the reliability evaluation model of the hybrid MMC capacitor are as follows:
3.1) calculating the capacitor reliability RC(tn) Namely:
in the formula, λcIs the capacitor failure rate. Ws0Is in an initial state. WsiSelf-healing energy corresponding to i SM faults. t is tnIs the sampling instant.
Self-healing energy WsiAs follows:
UCicapacitor voltage for i SM faults. RCIs a sheet resistance. C is capacitance. And f (P) is a sandwich pressure related function. k is a radical ofcTo calculate the correlation coefficient of the self-healing energy. a is the capacitor correlation coefficient. And b is the resistance correlation coefficient.
3.2) according to the capacitor reliability RC(tn) The hybrid MMC capacitor reliability was evaluated.
4) And analyzing the loss distribution of the hybrid MMC device, thereby establishing an improved hybrid MMC operation reliability evaluation model considering SM multi-state.
The hybrid MMC main circuit consists of three phase units, namely a phase unit, a phase unit and a phase unit, wherein each phase unit is divided into an upper bridge arm and a lower bridge arm, and each bridge arm is formed by connecting a plurality of SM in series. In order to take cost into consideration, the SM in each bridge arm comprises a half-bridge SM (HBSM) and an SM with direct current fault ride-through capability, and the single-clamping SM (CSSM) is selected as the SM with the direct current fault ride-through capability. Both SM main circuits consist of IGBTs, diodes (diodes) and capacitors. Meanwhile, in order to improve the reliability of the hybrid MMC, each bridge arm includes a redundant SM as a backup, and the embodiment adopts an active backup which is usually adopted in practice.
Further, the main steps of establishing the hybrid MMC operation reliability evaluation model considering SM multi-state are as follows:
4.1) calculating the reliability of the SM multi-state. The SM main circuit consists of an IGBT, a Diode and a capacitor.
According to the combination relation of IGBT, Diode and capacitor in SM, CSSM reliability R under intact stateCSu(tn) As follows:
RCSu(tn)=RT1(tn)·RD1(tn)·RT2(tn)·RD2(tn)·RT3(tn)·RD3(tn)·RC(tn)。 (30)
in the formula, RT1(tn)、RT2(tn) And RT3(tn) Reliability of the first IGBT, the second IGBT and the third IGBT, respectively. RD1(tn)、RD2(tn) And RD3(tn) Reliability of the first, second and third Diode, respectively. Rc(tn) The reliability of the capacitor.
HBSM reliability R in good conditionHBu(tn) As follows:
RHBu(tn)=RT1(tn)·RD1(tn)·RT2(tn)·RD2(tn)·RC(tn)。 (31)
in the formula, RT1(tn)、RT2(tn) And RT3(tn) Of a first IGBT, a second IGBT and a third IGBT respectivelyAnd (7) reliability. RD1(tn)、RD2(tn) And RD3(tn) Reliability of the first, second and third Diode, respectively. Rc(tn) The reliability of the capacitor.
At unpaired T3Before the module is added with a bypass switch, when T3And D3When any one of the devices fails, the entire CSSM is considered to have failed and immediately exits operation.
If it is at this time to T3The module carries out bypass processing, can make CSSM be in the half fault state who maintains voltage support function to the equivalence continues the operation for HBSM, and then promotes CSSM utilization ratio.
Reliability R of CSSM under half fault conditionCSp(tn) As follows:
RCSp(tn)=RT1(tn)·RD1(tn)·RT2(tn)·RD2(tn)·(1-RT3(tn)·RD3(tn))·RC(tn)。 (32)
in the formula, RT1(tn)、RT2(tn) And RT3(tn) Reliability of the first IGBT, the second IGBT and the third IGBT, respectively. RD1(tn)、RD2(tn) And RD3(tn) Reliability of the first, second and third Diode, respectively. Rc (t)n) The reliability of the capacitor.
4.2) accounting for SM multistate hybrid MMC reliability
The hybrid MMC bridge arm is formed by connecting a plurality of CSSM and HBSM in series.
Because both the complete CSSM and the half-fault CSSM can be equivalent to the HBSM, the voltage supporting function is maintained, and when the damage number of the HBSM is excessive, the condition that the complete CSSM and the half-fault CSSM replace the damaged HBSM exists, so that the hybrid MMC keeps normal operation.
Therefore, the bridge arm reliability can be divided into two cases, taking the single-phase upper bridge arm reliability as an example:
the reliability of the single-phase upper bridge arm is mainly divided into two cases.
The first case is: when neither CSSM nor HBSM damaged number exceeds its own redundancy number, iCS≤MCSAnd i isHB≤MHBMeanwhile, the hybrid MMC normally operates.
According to a binomial distribution probability formula, in the first case, the total CSSM reliability R of the upper bridge armCSs1(tn) As follows:
in the formula, NCSIs the baseline number of CSSM. RCSu(tn) The CSSM reliability in good condition. i.e. icsIs the number of CSSM damages. MCSIs the redundancy number of the CSSM.
In the first case, the total HBSM reliability R of the upper bridge armHBs1(tn) As follows:
in the formula, NHBThe baseline number for the HBSM. RHBu(tn) The HBSM reliability in the intact state. i.e. iHBIs the number of HBSM breakages. MHBIs the redundancy number of the HBSM.
Based on the series relation between CSSM and HBSM in bridge arm, the reliability R of single-phase upper bridge arm under the first conditionArm_u1(tn) As follows:
RArm_u1(tn)=RCSs1(tn)·RHBs1(tn)。 (35)
in the formula, RHBs1(tn) The total HBSM reliability for the upper arm in the first case. RCSs1(tn) The total CSSM reliability for the upper leg in the first case.
The second case is: when CSSM damage number does not exceed self redundancy number, and HBSM damage number exceeds self redundancy number, and good and half fault CSSMWhen displacing a damaged HBSM, i.e. iCS≤MCSAnd M isHB<iHB≤MHB+MCS-(iCS-iCSp) Meanwhile, the hybrid MMC normally operates. i.e. iCSpIs the CSSM half-fault number.
According to a polynomial distribution probability formula, the total CSSM reliability R of the upper bridge armCSs2(tn) As follows:
in the formula iCSpIs the CSSM half-fault number. N is a radical ofCSIs the baseline number of CSSM. RCSu(tn) The CSSM reliability in good condition. i.e. icsIs the number of CSSM damages. McsIs the redundancy number of the CSSM. RCSp(tn) Reliability of the half fault state CSSM.
Based on the serial connection relation of all HBSM in the bridge arms and according to a binomial distribution probability formula, the total HBSM reliability R of the upper bridge armHBs2(tn) As follows:
in the formula iCSpIs the CSSM half-fault number. i.e. icsIs the number of CSSM damages. N is a radical ofHBThe baseline number for the HBSM. RHBu(tn)The HBSM reliability in the intact state. i.e. iHBIs the number of HBSM breakages. MHBIs the redundancy number of the HBSM.
Based on the series relation between CSSM and HBSM in bridge arm, the reliability R of single-phase upper bridge arm under the second conditionArm_u2(tn) As follows:
RArm_u2(tn)=RCSs2(tn)·RHBs2(tn)。 (38)
in the formula, RHBs2(tn) The total HBSM reliability for the upper arm in the second case. RCSs2(tn) Total C of upper bridge arm in the second caseSSM reliability.
Reliability function R of single-phase upper bridge armArm_u(tn)As follows:
RArm_u(tn)=RArm_u1(tn)+RArm_u2(tn)。 (39)
in the formula, RArm_u1(tn) The single-phase upper arm reliability in the first case. RArm_u2(tn) The reliability of the single-phase upper bridge arm in the second condition.
Based on the symmetry of the mixed MMC and the series relation of each bridge arm, the reliability R (t) of the mixed MMCn) As follows:
R(tn)=RArm_u(tn)6。 (40)
in the formula, RArm_u(tn) Is a single-phase upper bridge arm reliability function.
Example 2:
a method for using an improved hybrid MMC operational reliability assessment model based on multi-time scale thermal damage, comprising the steps of:
1) data is input in the improved hybrid MMC operational reliability evaluation model. The data mainly comprises environmental parameters and mixed MMC and fan electrical parameters.
The environmental parameter mainly comprises wind speedAnd air temperatureThe hybrid MMC and wind turbine electrical parameters mainly comprise switching frequency fswThe hybrid MMC comprises a minimum cut-in wind speed, a maximum cut-off wind speed, a rated wind speed and the like, a direct current side rated voltage, an alternating current side rated voltage, a power factor, a modulation ratio, a duty ratio and the like.
2) And according to the input data, calculating the loss of the power device by the improved hybrid MMC operation reliability evaluation model.
I.e. calculating the sampling instant tnAverage IGBT switching period in corresponding time interval TLoss PT,avgAnd the average loss P of the switching period of the DiodeD,avg。
3) And according to the input data, calculating the multi-time scale junction temperature of the power device by the improved hybrid MMC operation reliability evaluation model.
Calculating the sampling time tnJunction temperature mean value T of IGBT fundamental frequency period within corresponding time interval TTjavg_FMaximum value TTjmax_FMinimum value TTjmin_FAnd effective value of current I of aluminum bonding wireF。
Calculating 0-t according to the rain flow algorithmnMaximum T of junction temperature curve of IGBT low-frequency period at momentTjmax_LMinimum value TTjmin_LAnd effective value of current I of aluminum bonding wireL。
4) According to input data, the improved hybrid MMC operation reliability evaluation model calculates the service life consumption, the average failure time and the failure rate of the power device in consideration of multiple time scales.
Calculating the number N of low-frequency cyclic failure cycles of the IGBTTf_LAnd the number N of cycles of failure of fundamental frequency cycleTf_FThereby obtaining the IGBT at 0-tnTime of day life consumption CLT(tn) Sampling time tnMean time to failure MTTF corresponding to time interval TT(tn) Failure rate λT(tn) And degree of reliability RT(tn)。
Calculating the number N of low-frequency cycle failure cycles of the DiodeDf_LAnd the number N of cycles of failure of fundamental frequency cycleDf_FThus obtaining a Diode in the range of 0-tnTime of day life consumption CLD(tn) Sampling time tnMean time to failure MTTF corresponding to time interval TD(tn) Failure rate λD(tn) And degree of reliability RD(tn)。
5) According to the input data, the improved hybrid MMC operation reliability evaluation model calculates the reliability RC (t) of the capacitorn)。
6) According to the input data, the improved hybrid MMC operation reliability evaluation model calculates hybrid MMC reliability R (t) of SM multi-staten) Thereby improving the hybrid MMCThe reliability of the operation was evaluated.
Example 3:
a test for verifying an improved hybrid MMC operation reliability evaluation model based on multi-time scale thermal damage mainly comprises the following steps:
1) and configuring experimental parameters. In the embodiment, an FF1000R17IE4 model power module of Infineon company is used as a hybrid MMC power module, as shown in Table 1, and 2016-year wind speed and temperature data of Ireland Dublin are used as external working conditions of a wind farm and the hybrid MMC, so that the operational reliability of the hybrid MMC is evaluated based on the model provided by the invention. The annual data curves of the wind speed and the air temperature are shown in figures 2 and 3, and the mixed MMC and fan parameters are shown in table 2.
TABLE 1 thermal parameter Table for FF1000R17IE4 model Power Module
Parameter(s) | Numerical value |
Rated capacity of system | 400MW |
Network side voltage | 220kV |
Voltage on the direct current side | 400kV |
Reference number of HBSM | 137 |
CSSM reference number | 113 |
Reference failure rate of capacitor | 1ⅹ10-8occ/hour |
Reference voltage of capacitor | 1.6kV |
Output frequency | 50Hz |
Switching frequency | 2kHz |
Power factor | 0.9 |
Modulation ratio | 0.8 |
Fan capacity | 2MW |
Number of fans | 200 |
Cut-in wind speed | 3m/s |
Rated wind speed | 8.5m/s |
Cut-out wind speed | 16m/s |
TABLE 2 hybrid MMC and Fan parameters
2) And (4) analyzing the thermal damage of the hybrid MMC power device. In order to verify the accuracy of the multi-time scale reliability evaluation model of the hybrid MMC power device, the low-frequency and fundamental frequency annual life consumption conditions of the power device are respectively obtained based on the reliability evaluation model of the power device, which is provided by the invention, by taking wind speed and air temperature annual data as input, and the specific table is shown in Table 3.
As can be seen from Table 3, although the low frequency lifetime was consumed at T1、T2、T3、D1And D2The medium ratio is large, but the consumption ratio of the life of the fundamental frequency is not negligible, and the consumption ratio is T2、D1And D3The percentage of the component (A) is respectively 16.39%, 25.06% and 67.82%, especially in D3In the middle, the consumption of the life of the fundamental frequency is dominant over the consumption of the low frequency. Therefore, compared with the reliability evaluation only considering the low-frequency service life consumption, the multi-time scale reliability evaluation model established by the invention can comprehensively take the influence of environmental factors and electrical parameters on the hybrid MMC power device into account, and lays a foundation for the operation reliability evaluation of equipment.
TABLE 3 hybrid MMC power device annual lifetime consumption
3) Improved measure to hybrid MMC reliability impact
As can be seen from Table 3, T3And D3The sum of the lifetime consumptions of (a) is up to 50.08% higher in CSSM lifetime consumption than in other devices, and thus, T is higher3The module is most vulnerable. The invention passes the fault T3Short-circuiting the modules to enable T3CSSM equivalent of module trouble is HBSM, continues to maintain voltage support function to promote CSSM utilization ratio, reach and promote mixed MMC reliability level.
To verify the impact of improved CSSM on hybrid MMC reliability proposed by the present invention, the SM multi-state-taking hybrid MMC operational reliability assessment is proposed based on the conventional model and the present inventionModel to obtain improved front and back mixed MMC reliability R1And R2See, in particular, fig. 4 and table 4.
As can be seen from FIG. 4, the improved reliability R of the hybrid MMC2Greater than reliability before improvement R1. As can be seen from Table 4, R is the time when the mixed MMC is operated for 15 years1And R20.7421 and 0.8838, respectively, in comparison to R1Improved mixed MMC reliability R2The improvement is 19.10%. And when the mixed MMC is 20 years, R1And R20.2018 and 0.4978, respectively, in comparison to R1The improved reliability R2 of the hybrid MMC is improved by 146.68%. Therefore, the reliability of the improved hybrid MMC is effectively improved, and the effectiveness of the improved measures is verified.
Time/year | Reliability R1 | Reliability R2 | Percentage of |
5 | 0.9999 | 0.9999 | 0.00% |
10 | 0.9861 | 0.9935 | 0.75% |
15 | 0.7421 | 0.8838 | 19.10% |
20 | 0.2018 | 0.4978 | 146.68% |
25 | 0.0113 | 0.1184 | 947.78% |
30 | 0 | 0.0096 | — |
TABLE 4 MMC reliability Table with mix of front and rear
4) And (5) evaluating the operation reliability of the hybrid MMC.
In order to verify the effectiveness of the mixed MMC operation reliability model provided by the invention, the influence of the fluctuation of environmental factors such as wind speed and air temperature and the difference of electrical parameters of the mixed MMC such as switching frequency on the operation reliability of the mixed MMC is evaluated based on the reliability evaluation model provided by the invention.
4.1) analyzing the influence of environmental factors on the operation reliability of the hybrid MMC.
In order to analyze the influence of environmental factors such as wind speed, air temperature and the like on the reliability of the hybrid MMC, the hybrid MMC is operated according to a hybrid MMC operation reliability model and a conventional constant failure rate model provided by the text by reference numbers to respectively obtain the reliability R of the hybrid MMC1And R2See, in particular, fig. 5. At the same time, CSSM and HBSM failure rate curves are derived, as shown in fig. 6.
As can be seen from FIG. 5, the reliability of the hybrid MMC may be changed by the influence of environmental factors such as wind speed and air temperature. As shown in FIGS. 2 and 6, when the hybrid MMC is operated for 1000h and 500-h, the wind speed is high and is concentrated on 7-11m/s, the service life loss of the device is large, and the fault rates of HBSM and CSSM are concentrated on 0.9 multiplied by 10-6occ/hour and 1.8X 10-6occ/hour, mixed MMC decreased faster. When the hybrid MMC operates at 3500-4000h, the wind speed is low and is concentrated at 1-5m/s, the service life loss of the device is low, the fault rate of HBSM and CSSM is close to zero, and the reliability of the hybrid MMC is slowly reduced. Similarly, as shown in FIG. 3, during the period of 4000-. Therefore, the hybrid MMC operational reliability assessment model presented herein is in line with theoretical expectations. Furthermore, as can be seen from FIG. 5, since R2Not considering the changes of environmental factors such as wind speed, air temperature and the like, and R is measured at 1000h, 4000h and 7000h2And R1The relative errors respectively reach 41.38%, 34.45% and 82.36%, and the reliability difference is large. Therefore, the influence of environmental factors such as wind speed and air temperature on the reliability of the hybrid MMC needs to be taken into consideration.
4.2) analyzing the influence of the electrical parameters on the operation reliability of the hybrid MMC.
In order to analyze the influence of electrical parameters such as switching frequency on the operation reliability of the hybrid MMC, the reliability change condition of the hybrid MMC under different switching frequencies is obtained based on the operation reliability model of the hybrid MMC provided by the invention, and the concrete figure is shown in FIG. 7. Table 5 shows the reliability operation of the hybrid MMC at different switching frequencies for 900 h.
As can be seen from fig. 7, the higher the switching frequency, the faster the reliability of the hybrid MMC decreases. As can be seen from Table 5, when the switching frequency of the power device is increased from 1000Hz to 3000Hz at time 900h, the switching loss is increased, resulting in CSSM and HBSM failure rates of 6.91 × 10-7occ/hour and 1.56X 10-7occ/hour rose to 2.17X 10-6occ/hour and 1.63X 10-6occ/hour, the mixed MMC reliability is finally reduced from 0.715 to 0.2572. Therefore, the operation reliability evaluation model provided by the invention can effectively depict the influence of the switching frequency on the operation reliability of the hybrid MMC.
Table 5900 h-time mixed MMC operation reliability table under different switching frequencies
In conclusion, the mixed MMC operation reliability evaluation model considering the multi-time scale accumulated damage effect can accurately depict the influence of environmental factors such as wind speed and air temperature and electrical parameters such as switches on the operation reliability of the mixed MMC, the reliability of the mixed MMC is improved from the operation angle, and the reliability level of the improved mixed MMC is proved to be remarkably improved by constructing the corresponding mixed MMC reliability evaluation model considering the SM multi-state.
Claims (4)
1. A method for establishing an improved hybrid MMC operation reliability evaluation model based on multi-time scale heat damage is characterized by mainly comprising the following steps:
1) acquiring real-time data of a wind power transmission system; the real-time data mainly comprises wind speed, air temperature and equipment electrical parameters;
2) according to the real-time data, establishing a reliability evaluation model of the hybrid MMC power device by utilizing the running characteristics of the hybrid MMC and a Miner's damage theory; the power device of the wind power transmission system mainly comprises an Insulated Gate Bipolar Transistor (IGBT) and a crystal Diode (Diode);
3) establishing a mixed MMC capacitor reliability evaluation model considering the voltage sharing of the fault SM according to the influence of the fault SM on the intact SM capacitor;
4) analyzing loss distribution of the hybrid MMC device, and thus establishing an improved hybrid MMC operation reliability evaluation model considering SM multi-state;
the method mainly comprises the following steps of establishing an improved hybrid MMC operation reliability evaluation model considering SM multi-state:
4.1) calculating the reliability of the SM multi-state; the SM main circuit consists of an IGBT, a Diode and a capacitor;
according to the combination relation of IGBT, Diode and capacitor in SM, CSSM reliability R under intact stateCSu(tn) As follows:
RCSu(tn)=RT1(tn)·RD1(tn)·RT2(tn)·RD2(tn)·RT3(tn)·RD3(tn)·RC(tn); (1)
in the formula, RT1(tn)、RT2(tn) And RT3(tn) Reliability of the first IGBT, the second IGBT and the third IGBT respectively; rD1(tn)、RD2(tn) And RD3(tn) Reliability of the first, second and third Diode, respectively; rc(tn) Capacitor reliability;
HBSM reliability R in good conditionHBu(tn) As follows:
RHBu(tn)=RT1(tn)·RD1(tn)·RT2(tn)·RD2(tn)·RC(tn); (2)
in the formula, RT1(tn)、RT2(tn) Reliability of the first IGBT and the second IGBT respectively; rD1(tn)、RD2(tn) Reliability of the first and second diodes, respectively; rc(tn) Capacitor reliability;
reliability R of CSSM under half fault conditionCSp(tn) As follows:
RCSp(tn)=RT1(tn)·RD1(tn)·RT2(tn)·RD2(tn)·(1-RT3(tn)·RD3(tn))·RC(tn); (3)
in the formula, RT1(tn)、RT2(tn) And RT3(tn) Reliability of the first IGBT, the second IGBT and the third IGBT respectively; rD1(tn)、RD2(tn) And RD3(tn) Respectively, a first, a second and a third DiodeReliability; rc (t)n) Capacitor reliability;
4.2) accounting for SM multistate hybrid MMC reliability
The reliability of the bridge arm is mainly divided into two cases;
the first case is: when neither CSSM nor HBSM damaged number exceeds its own redundancy number, iCS≤MCSAnd i isHB≤MHBWhen the hybrid MMC normally operates;
according to a binomial distribution probability formula, in the first case, the total CSSM reliability R of the upper bridge armCSs1(tn) As follows:
in the formula, NCSA reference number for the CSSM; rCSu(tn) CSSM reliability under intact condition; i.e. icsIs the number of CSSM defects; mCSRedundancy number for CSSM;
in the first case, the total HBSM reliability R of the upper bridge armHBs1(tn) As follows:
in the formula, NHBA reference number for HBSM; rHBu(tn) HBSM reliability under intact state; i.e. iHBDamage number for HBSM; mHBRedundancy number for HBSM;
based on the series relation between CSSM and HBSM in bridge arm, the reliability R of single-phase upper bridge arm under the first conditionArm_u1(tn) As follows:
RArm_u1(tn)=RCSs1(tn)·RHBs1(tn); (6)
in the formula, RHBs1(tn) The total HBSM reliability of the upper bridge arm in the first case; rCSs1(tn) In the first caseThe total CSSM reliability of the lower and upper bridge arms;
the second case is: when the CSSM defect number does not exceed the self-redundancy number, the HBSM defect number exceeds the self-redundancy number, and the good and half-fault CSSMs replace the damaged HBSM, i.e., iCS≤MCSAnd M isHB<iHB≤MHB+MCS-(iCS-iCSp) When the hybrid MMC normally operates; i.e. iCSpIs the CSSM half fault number;
according to a polynomial distribution probability formula, the total CSSM reliability R of the upper bridge armCSs2(tn) As follows:
in the formula iCSpIs the CSSM half fault number; n is a radical ofCSA reference number for the CSSM; rCSu(tn) CSSM reliability under intact condition; i.e. icsIs the number of CSSM defects; mcsRedundancy number for CSSM; rCSp(tn) Reliability for a half fault state CSSM;
based on the serial connection relation of all HBSM in the bridge arms and according to a binomial distribution probability formula, the total HBSM reliability R of the upper bridge armHBs2(tn) As follows:
in the formula iCSpIs the CSSM half fault number; i.e. icsIs the number of CSSM defects; n is a radical ofHBA reference number for HBSM; rHBu(tn)HBSM reliability under intact state; i.e. iHBDamage number for HBSM; mHBRedundancy number for HBSM;
based on the series relation between CSSM and HBSM in bridge arm, the reliability R of single-phase upper bridge arm under the second conditionArm_u2(tn) As follows:
RArm_u2(tn)=RCSs2(tn)·RHBs2(tn); (9)
in the formula, RHBs2(tn) The total HBSM reliability of the upper bridge arm under the second condition; rCSs2(tn) The total CSSM reliability for the upper leg in the second case;
reliability function R of single-phase upper bridge armArm_u(tn)As follows:
RArm_u(tn)=RArm_u1(tn)+RArm_u2(tn); (10)
in the formula, RArm_u1(tn) The reliability of the single-phase upper bridge arm under the first condition; rArm_u2(tn) The reliability of the single-phase upper bridge arm under the second condition;
based on the symmetry of the mixed MMC and the series relation of each bridge arm, the reliability R (t) of the mixed MMCn) As follows:
R(tn)=RArm_u(tn)6; (11)
in the formula, RArm_u(tn) Is a single-phase upper bridge arm reliability function.
2. The method for establishing the improved hybrid MMC operation reliability evaluation model based on multi-time scale heat damage according to claim 1, wherein: the method mainly comprises the following steps of establishing the reliability evaluation model of the hybrid MMC power device:
1) calculating the multi-time scale junction temperature of the hybrid MMC power device; the method mainly comprises the following steps:
1.1) determining the output power P of the fan of the wind power transmission systemWToutAnd a sampling time tnCorresponding to wind speed VtnThe relationship of (1);
output power P of ith fan of wind power transmission systemWTout,iAnd a sampling time tnCorresponding to wind speed VtnThe relationship of (a) is as follows:
in the formula, PratedRated power for the fan; vcutin、VratedAnd VcutoutRespectively the cut-in wind speed, the rated wind speed and the cut-out wind speed; k is a radical ofpRepresenting coefficients related to air density and fan area; n is a radical ofWTThe total number of fans in the wind power transmission system; n is the total number of sampling points until the current running time; t is tnIs the sampling time;is the wind speed; i is any fan; 1, …, NWT;
Transport power P of hybrid MMCMMCoutAs follows:
in the formula, NWTThe total number of fans in the wind power transmission system; i is any fan; 1, …, NWT;PWTout,iOutputting power for the ith fan;
1.2) calculating to obtain a mixed MMC bridge arm current according to a formula 1;
a phase upper bridge arm current IauAnd phase A lower bridge arm current IadRespectively as follows:
in the formula IdcIs direct current side current; i ismIs the ac side current peak;is a power factor angle; f. of0Is the fundamental frequency;
direct side current IdcAs follows:
in the formula of UdcIs a direct current side voltage; pMMCoutA transport power for a hybrid MMC;
peak value of AC side current ImAs follows:
in the formula, PMMCoutA transport power for a hybrid MMC;is a power factor angle; u shapeacThe effective value of the voltage at the alternating current side;
1.3) calculating the average loss of the jth switching period of the IGBT of the upper bridge arm of the phase A;
average loss of jth switching period of IGBT (insulated Gate Bipolar transistor) of upper bridge arm of A phaseAs follows:
in the formula, Rce、UceoAnd τTThe IGBT positive on-resistance, the threshold voltage and the duty ratio are respectively; a isT、bTAnd cTFitting parameters for the IGBT dynamic characteristic curve; u shaperatedRated voltage for IGBT; f. ofswAnd ρTThe switching frequency and the temperature coefficient of the IGBT are respectively; j is any switching period; j is 1, …, nsw;nswThe total number of switching cycles in a fundamental frequency cycle; i isauIs the A phase upper bridge arm current; u shapedcIs a direct current side voltage;
number of switching cycles nswAs follows:
nsw=fsw/f0; (18)
in the formula (f)swIs the switching frequency of the IGBT; f. of0Is the fundamental frequency;
in the formula: rd、UdAnd τDRespectively, Diode forward on-resistance, threshold voltage and duty cycle; a isD、bDAnd cDFitting parameters for the dynamic characteristic curve of the Diode; u shapeDIs a Diode rated voltage; f. ofdwAnd ρDRespectively, the switching frequency and the temperature coefficient of the Diode; i isauIs the A phase upper bridge arm current; u shapedcIs a direct current side voltage;
in the formula (I), the compound is shown in the specification,is the sampling time tnA corresponding air temperature;the temperature difference of an RC parallel unit in an IGBT junction-shell thermal network in the jth switching period of the nth order; r represents an arbitrary order; r is 1,2,3, 4;the temperature difference of RC parallel units in the jth switching period IGBT shell-radiating fin heat network is obtained;the temperature difference of an RC parallel unit in the jth switching period IGBT radiating fin-environment thermal network is obtained; j is any switching period; j is 1, …, nsw;nswThe total number of switching cycles in a fundamental frequency cycle;
temperature difference of RC parallel unit in jth switching period IGBT junction-shell network of nth orderAs follows:
in the formula, RTjc,rIs the thermal resistance; tau isTjc,rIs the thermal resistance RTjc,rThermal time constant of (d); t isswIs a switching cycle;is the temperature difference of RC parallel units in the ith order of switching period (j-1) IGBT junction-shell thermal network;average loss of the jth switching period of the IGBT of the upper bridge arm of the phase A; j is any switching period; j is 1, …, nsw;nswThe total number of switching cycles in a fundamental frequency cycle;
temperature difference of RC parallel unit in jth switching period IGBT shell-heat sink networkAs follows:
in the formula, RTchIs the thermal resistance; tau isTchIs the thermal resistance RTchThermal time constant of (d); t isswIs a switching periodThe temperature difference of RC parallel units in the j-1 switching period IGBT shell-radiating fin heat network;average loss of the jth switching period of the IGBT of the upper bridge arm of the phase A; j is any switching period; j is 1, …, nsw;nswThe total number of switching cycles in a fundamental frequency cycle;
the jth switching period IGBT is the temperature difference of RC parallel units in the radiating fin-environment networkAs follows:
in the formula, RhaIs the thermal resistance; tau ishaIs the thermal resistance RhaThermal time constant of (d); t isswIs a switching cycle;is the cycle temperature difference of the RC parallel unit in the j-1 th switch IGBT thermal network; j is any switching period; j is 1, …, nsw;nswThe total number of switching cycles in a fundamental frequency cycle;average loss of the jth switching period of the IGBT of the upper bridge arm of the phase A;average loss of the jth switching period of the A-phase upper bridge arm Diode;
in the formula (I), the compound is shown in the specification,is the sampling time tnA corresponding air temperature;the temperature difference of an RC parallel unit in a j-th switching period Diode junction-shell heat network of an r-th order; r represents an arbitrary order; r is 1,2,3, 4;the temperature difference of RC parallel units in the j switching period Diode shell-radiating fin heat network is obtained;for the temperature difference of RC parallel unit in jth switching period IGBT heat sink-environment heat network(ii) a j is any switching period; j is 1, …, nsw;nswThe total number of switching cycles in a fundamental frequency cycle;
temperature difference of RC parallel unit in jth switching period Diode junction-shell networkAs follows:
in the formula, RDjc,rIs the thermal resistance; tau isDjc,rIs the thermal resistance RDjc,rThermal time constant of (d); t isdwIs a switching cycle;is the temperature difference of the RC parallel unit in the j-1 switching period Diode junction-shell heat network; j is any switching period; j is 1, …, nsw;nswThe total number of switching cycles in a fundamental frequency cycle;average loss of the jth switching period of the A-phase upper bridge arm Diode;
temperature difference of RC parallel unit in jth switching period Diode shell-fin networkAs follows:
in the formula, RDchIs the thermal resistance; tau isDchIs the thermal resistance RDchThermal time constant of (d); t isswIs a switching cycle;is the temperature difference of RC parallel units in the j-1 switching period Diade shell-fin heat network;average loss of the jth switching period of the A-phase upper bridge arm Diode; j is 1, …, nsw;nswThe total number of switching cycles in a fundamental frequency cycle;
2) evaluating the multi-time scale reliability of the hybrid MMC power device; the method mainly comprises the following steps:
2.1) calculating the cycle failure period number N corresponding to the low-frequency period of the IGBTTf_L(ii) a Number of cycles to failure NTf_LAs follows:
in the formula, tonIs the heating time; u is 0.01 times of the blocking voltage of the module; d is the diameter of the aluminum bonding wire; k is 9.3 × 1014;β1=-4.416;β2=1285;β3=-0.463;β4=-0.716;β5=-0.761;β6=-0.5;TTjmax_LThe maximum value of the IGBT low-frequency junction temperature is obtained; t isTjmin_LThe minimum value of the IGBT low-frequency junction temperature is obtained; i isLThe effective value of the current of the IGBT low-frequency aluminum bonding wire is obtained;
cycle failure period number N corresponding to IGBT fundamental frequency periodTf_FAs follows:
in the formula, tonIs the heating time; u is 0.01 times of the blocking voltage of the module; d is the diameter of the aluminum bonding wire; k is 9.3 × 1014;β1=-4.416;β2=1285;β3=-0.463;β4=-0.716;β5=-0.761;β6=-0.5;TTjmax_FThe maximum value of the IGBT fundamental frequency junction temperature is obtained; t isTjmin_FJunction temperature of IGBT fundamental frequencyA minimum value; i isFThe effective value of the current of the IGBT fundamental frequency aluminum bonding wire is obtained;
according to Miner's damage theory and formula (17), IGBT is in 0-tnTime of day life consumption CLT(tn) As follows:
in the formula, NT_L,gAnd NTf_L,gRespectively corresponding thermal cycle times and cycle failure cycles of the IGBTs in the g-th low-frequency thermal cycle; n is a radical ofT_F,qAnd NTf_F,qRespectively corresponding to the q sampling time interval T of the IGBT, the fundamental frequency thermal cycle times and the cycle failure cycles; n is the total number of sampling points until the current running time; n is a radical ofTsum_LIs the total number of low frequency thermal cycles;
IGBT sampling time tnMean time to failure MTTF corresponding to time interval TT(tn) As follows:
in the formula, CLT(tn) Is IGBT at 0-tnThe consumption of the lifetime at a moment; t is a sampling time interval;
IGBT failure rate lambdaT(tn) As follows:
in the formula, MTTFT(tn) For the IGBT sampling time tnThe average time to failure of the corresponding time interval T;
IGBT reliability RT(tn)As follows:
in the formula, λT(tn) Is the IGBT failure rate; t is tnIs the sampling time;
2.2) calculating the cycle failure period number N corresponding to the Diode low-frequency periodDf_L(ii) a Number of cycles to failure NDf_LAs follows:
in the formula, tonIs the heating time; u is 0.01 times of the blocking voltage of the module; d is the diameter of the aluminum bonding wire; k is 9.3 × 1014;β1=-4.416;β2=1285;β3=-0.463;β4=-0.716;β5=-0.761;β6=-0.5;TDjmax_LIs the maximum value of the Diode low-frequency junction temperature; t isDjmin_LIs the minimum value of the Diode low-frequency junction temperature; i isDLThe effective value of the current of the Diode low-frequency aluminum bonding wire is obtained;
number of cycle failure cycles N corresponding to the period of the Diode fundamental frequencyDf_FAs follows:
in the formula, tonIs the heating time; u is 0.01 times of the blocking voltage of the module; d is the diameter of the aluminum bonding wire; k is 9.3 × 1014;β1=-4.416;β2=1285;β3=-0.463;β4=-0.716;β5=-0.761;β6=-0.5;TDjmax_FIs the maximum value of the junction temperature of the Diode fundamental frequency; t isDjmin_FIs the minimum value of the junction temperature of the Diode fundamental frequency; i isDFThe effective value of the current of the Diade fundamental frequency aluminum bonding wire is obtained;
according to Miner's injury theory and equation (23), the Diode is at 0-tnTime of day life consumption CLD(tn) As follows:
in the formula, NDsum_LIs a Diode at 0-tnTotal number of low frequency thermal cycles at the moment; n is a radical ofD_L,αAnd NDf_L,αRespectively corresponding thermal cycle times and cycle failure cycles of the alpha-th low-frequency thermal cycle of the Diode; n is a radical ofD_F,ωAnd NDf_F,ωRespectively corresponding to the omega th sampling time interval T, the fundamental frequency thermal cycle times and the cycle failure cycles; n is the total number of sampling points until the current running time;
the Diode sampling time tnMean time to failure MTTF corresponding to time interval TD(tn) As follows:
in the formula, CLD(tn) Is a Diode at 0-tnThe consumption of the lifetime at a moment; t is a sampling time interval;
diade failure rate λD(tn) As follows:
in the formula, MTTFD(tn) For the moment t of the Diade samplingnThe average time to failure of the corresponding time interval T;
diade reliability RD(tn) is as follows:
in the formula, λD(tn) Is the rate of Diade failures; t is tnIs the sampling instant.
3. The method for establishing the improved hybrid MMC operation reliability evaluation model based on multi-time scale heat damage according to claim 1, wherein: the method mainly comprises the following steps of establishing a reliability evaluation model of the hybrid MMC capacitor:
1) calculating capacitor reliability RC(tn) Namely:
in the formula, λcIs the capacitor failure rate; ws0Is in an initial state; wsiSelf-healing energy corresponding to the i SM faults; t is tnIs the sampling time;
self-healing energy WsiAs follows:
UCicapacitor voltages corresponding to i SM faults; rCIs a thin film resistor; c is capacitance; (p) is a sandwich pressure related function; a is the capacitor correlation coefficient; b is a resistance correlation coefficient; k is a radical ofcCalculating the correlation coefficient of self-healing energy;
2) according to capacitor reliability RC(tn) The hybrid MMC capacitor reliability was evaluated.
4. A method for modeling an improved hybrid MMC operational reliability assessment model based on multi-time scale thermal damage according to any one of claims 1-3, and mainly comprising the steps of:
1) inputting data in an improved hybrid MMC operation reliability evaluation model; the data mainly comprises environmental parameters, mixed MMC and fan electrical parameters; the environmental parameter mainly comprises wind speedAnd air temperatureThe hybrid MMC and wind turbine electrical parameters mainly comprise switching frequency fswThe hybrid MMC has a direct current side rated voltage, an alternating current side rated voltage, a power factor, a modulation ratio and a duty ratio;
2) according to input data, the improved hybrid MMC operation reliability evaluation model calculates the loss of a power device; i.e. calculating the sampling instant tnAverage loss P of IGBT switching period in corresponding time interval TT,avgAnd the average loss P of the switching period of the DiodeD,avg;
3) According to input data, the improved hybrid MMC operation reliability evaluation model calculates the multi-time scale junction temperature of the power device;
calculating the sampling time tnJunction temperature mean value T of IGBT fundamental frequency period within corresponding time interval TTjavg_FMaximum value TTjmax_FMinimum value TTjmin_FAnd effective value of current I of aluminum bonding wireF(ii) a Calculating 0-t according to the rain flow algorithmnMaximum T of junction temperature curve of IGBT low-frequency period at momentTjmax_LMinimum value TTjmin_LAnd effective value of current I of aluminum bonding wireL;
4) According to input data, the improved hybrid MMC operation reliability evaluation model calculates the service life consumption, the average failure time and the failure rate of the power device and the multi-time scale;
calculating the number N of low-frequency cyclic failure cycles of the IGBTTf_LAnd the number N of cycles of failure of fundamental frequency cycleTf_FThereby obtaining the IGBT at 0-tnTime of day life consumption CLT(tn) Sampling time tnMean time to failure MTTF corresponding to time interval TT(tn) Failure rate λT(tn) And degree of reliability RT(tn);
Calculating the number N of low-frequency cycle failure cycles of the DiodeDf_LAnd the number N of cycles of failure of fundamental frequency cycleDf_FThus obtaining a Diode in the range of 0-tnTime of day life consumption CLD(tn) Sampling time tnMean time to failure MTTF corresponding to time interval TD(tn) Failure rate λD(tn) And degree of reliability RD(tn);
5) According to input data, the improved hybrid MMC operation reliability evaluation model calculates the reliability R of the capacitorC(tn);
6) According to the input data, the improved hybrid MMC operation reliability evaluation model calculates hybrid MMC reliability R (t) of SM multi-staten) Thereby evaluating the reliability of improving the operation of the hybrid MMC.
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CN109149982B (en) * | 2018-08-21 | 2020-01-31 | 南方电网科学研究院有限责任公司 | Reliability evaluation method for power module of modular level converter |
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