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december 2011 doc id 022380 rev 1 1/53 AN3994 application note managing the best in cla ss mdmesh? v and mdmesh? ii super junction technologies: driving and layout key notes introduction one of the bigger challenges of the 21 st century is to deal with the growing need for power and, at the same time, the necessity of product compactness. the new mdmesh? v series from stmicroelectronics, based on the super junction concept, meets these targets by offering an extremely low r ds(on) value in a given package, unobtainable in standard hv mosfets. in addition to the dramatic reduction of r ds(on) , super junction mosfets are extremely fast in transients and this may lead to some issues when a better performing technology replaces an older version on the same board with the same driving network. the two main components in the st super junction mosfet family (mdmesh? ii and mdmesh? v) are analyzed and compared in terms of energy losses, voltage, and current rates. it is shown how the external driving network impacts on their performances. furthermore, a separate section is dedicated to the layout parasitic effects and their impact on mosfet behavior. it is clear in the end that layout can be crucial, especially when managing very fast transients, and it must be carefully planned in order to help the mosfet exploit its best potential. www.st.com
contents AN3994 2/53 doc id 022380 rev 1 contents 1 st multidrain technology evolut ion . . . . . . . . . . . . . . . . . . . . . . . . . . . . 5 2 parasitic capacitances overview . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 8 3 mosfet standard turn-on and turn-off analysi s . . . . . . . . . . . . . . . . . 11 4 gate charge curve impact on dynamic r esponses . . . . . . . . . . . . . . . 15 5 latest st md ii and md v technology at a glance . . . . . . . . . . . . . . . . 20 6 md ii and md v: which is t he lowest loss one? . . . . . . . . . . . . . . . . . . 21 6.1 stb42n65m5 vs. stw48nm60n . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 21 6.2 stp35n65m5 vs. stb36nm60n . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 24 6.3 stp21n65m5 vs. stp24nm60n . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 27 6.4 stp16n65m5 vs. stp18nm60n . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 30 6.5 comments about energy on comparison . . . . . . . . . . . . . . . . . . . . . . . . 33 6.6 comments about energy off comparison . . . . . . . . . . . . . . . . . . . . . . . 33 7 mosfet critical paramete rs in high switching environments . . . . . . 36 7.1 parasitic inductance influence on switching losses . . . . . . . . . . . . . . . . . 36 7.2 common source inductance . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 37 7.3 minimizing common source inductance: layout optimization and kelvin source connection on stw77n65m5 . . . . . . . . . . . . . . . . . . . . . . . . . . . . 39 7.4 minimizing common s ource inductance impac t at turn-off: negative v gmoff . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 49 7.5 switching loop induct ance . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 51 8 revision history . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 52
AN3994 list of figures doc id 022380 rev 1 3/53 list of figures figure 1. standard hv mosfet device cross section . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 5 figure 2. md device cross section . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 5 figure 3. silicon ideal limit, sj limit and st md v position . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 6 figure 4. st?s hv technology evolution . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 7 figure 5. n-channel power mosfet structure and intrinsic capacitances . . . . . . . . . . . . . . . . . . . . . 8 figure 6. equivalent model of power mosfet intrinsic capacitances . . . . . . . . . . . . . . . . . . . . . . . . 8 figure 7. clamped inductive load test circuit used to carry out the dynamic tests on the mosfets 10 figure 8. turn-on of a mosfet in a clamped inductive load . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 12 figure 9. equivalent capacitive model of a mosfet . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 12 figure 10. turn-off of a mosfet in a clamped inductive load . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 13 figure 11. vg(t) curve measured on stb42nm60n @16 a, 400 v, ig=1.5 ma . . . . . . . . . . . . . . . . . 17 figure 12. vg(t) curve measured on stw48nm60n @16 a, 400 v, ig=1.5 ma . . . . . . . . . . . . . . . . 17 figure 13. turn-on of stb42n65m5 @16 a, 400 v, 47 w . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 19 figure 14. turn-on of stw48nm60n @16 a, 400 v, 47 w . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 19 figure 15. turn-off of stb42n65m5 @16 a, 400 v, 47 w . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 19 figure 16. turn-off of stw48nm60n @16 a, 400 v, 47 w . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 19 figure 17. minimum rds(on) per package achievable by md ii and md v . . . . . . . . . . . . . . . . . . . . 20 figure 18. stb42n65m5 vs. stw48nm60n eon @ 8 a/16 a, 400 v . . . . . . . . . . . . . . . . . . . . . . . . 21 figure 19. stb42n65m5 vs. stw48nm60n di/dt at turn-on @ 8 a/16 a, 400 v . . . . . . . . . . . . . . . . 21 figure 20. stb42n65m5 vs. stw48nm60n dv/dt at turn-on @ 8 a/16 a 400 v . . . . . . . . . . . . . . . . 22 figure 21. stb42n65m5 vs. stw48nm60n zoom of dv/dt at turn-on @ 8 a/16 a 400 v . . . . . . . . . 22 figure 22. stb42n65m5 vs. stw48nm60n eoff @ 8 a/16 a, 400 v . . . . . . . . . . . . . . . . . . . . . . . . 23 figure 23. stb42n65m5 vs. stw48nm60n di/dt at turn-off @ 8 a/16 a, 400 v . . . . . . . . . . . . . . . . 23 figure 24. stb42n65m5 vs. stw48nm60n dv/dt at turn-off @ 8 a/ 16 a, 400 v . . . . . . . . . . . . . . . 24 figure 25. stp35n65m5 vs. stb36nm60n eon @ 7.5 a/15 a, 400 v . . . . . . . . . . . . . . . . . . . . . . . 24 figure 26. stp35n65m5 vs. stb36nm60n di/dt at turn-on @ 7.5 a/15 a, 400 v . . . . . . . . . . . . . . . 25 figure 27. stp35n65m5 vs. stb36nm60n dv/dt at turn-on @ 7.5 a/15 a 400 v . . . . . . . . . . . . . . . 25 figure 28. stp35n65m5 vs. stb36nm60n eoff @ 7.5 a/15 a, 400 v . . . . . . . . . . . . . . . . . . . . . . . 26 figure 29. stp35n65m5 vs. stb36nm60n di/dt at turn-off @ 7.5 a/15 a, 400 v . . . . . . . . . . . . . . . 26 figure 30. stp35n65m5 vs. stb36nm60n dv/dt at turn-off @ 7.5 a/15 a, 400 v . . . . . . . . . . . . . . 27 figure 31. stp21n65m5 vs. stp24nm60n eon @ 4 a/ 8 a, 400 v . . . . . . . . . . . . . . . . . . . . . . . . . 27 figure 32. stp21n65m5 vs. stp24nm60n di/dt at turn-on @ 4 a/8 a, 400 v . . . . . . . . . . . . . . . . . 28 figure 33. stp21n65m5 vs. stp24nm60n dv/dt at turn-on @ 4 a/8 a, 400 v . . . . . . . . . . . . . . . . . 28 figure 34. stp21n65m5 vs. stp24nm60n eoff @ 4 a/8 a, 400 v . . . . . . . . . . . . . . . . . . . . . . . . . . 29 figure 35. stp21n65m5 vs. stp24nm60n di/dt at turn-off @ 4 a/8 a, 400 v . . . . . . . . . . . . . . . . . 29 figure 36. stp21n65m5 vs. stp24nm60n dv/dt at turn-off @ 4 a/8 a, 400 v . . . . . . . . . . . . . . . . . 30 figure 37. stp16n65m5 vs. stp18nm60n eon @ 3 a/6 a, 400 v . . . . . . . . . . . . . . . . . . . . . . . . . . 30 figure 38. stp16n65m5 vs. stp18nm60n di/dt at turn-on @ 3 a/ 6 a, 400 v . . . . . . . . . . . . . . . . . 31 figure 39. stp16n65m5 vs. stp18nm60n dv/dt at turn-on @ 3 a/6 a, 400 v . . . . . . . . . . . . . . . . . 31 figure 40. stp16n65m5 vs. stp18nm60n eoff @ 3 a/6 a, 400 v . . . . . . . . . . . . . . . . . . . . . . . . . . 32 figure 41. stp16n65m5 vs. stp18nm60n di/dt at turn-off @ 3 a/6 a, 400 v . . . . . . . . . . . . . . . . . 32 figure 42. stp16n65m5 vs. stp18nm60n dv/dt at turn-off @ 3 a/6 a, 400 v . . . . . . . . . . . . . . . . . 33 figure 43. equivalent capacitive model of a mosfet with parasitic inductances at turn-on . . . . . . . 36 figure 44. turn-on of stw77n65m5@400 v, 13 a, 25 c . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 37 figure 45. equivalent driving circuit of a mosfet at turn-on with parasitic source inductance . . . . . 38 figure 46. simplified equivalent series resonant model of the driving circuit of a mosfet . . . . . . . . 39 figure 47. gate driving and main switching loops for a mosfet in a boost-like topology . . . . . . . 40 figure 48. stw77 energy on difference between the standard layout and the optimized layout . . . 41 figure 49. stw77 energy off difference between the standard layout and the optimized layout. . . 41
list of figures AN3994 4/53 doc id 022380 rev 1 figure 50. stw77n65m5 eoff @ 20 a, 2.2 w with non-optimized common path. . . . . . . . . . . . . . . . 42 figure 51. stw77n65m5 eoff @ 20 a, 2.2 w with non-optimized common path. . . . . . . . . . . . . . . . 42 figure 52. stw77n65m5 eoff @ 20 a, 2.2 w with optimized common path . . . . . . . . . . . . . . . . . . . 42 figure 53. stw77n65m5 eoff @ 40 a, 2.2 w with non-optimized common path. . . . . . . . . . . . . . . . 43 figure 54. stw77n65m5 eoff @ 40 a, 2.2 w with non-optimized common path. . . . . . . . . . . . . . . . 43 figure 55. stw77n65m5 eoff @ 40 a, 2.2 w, 400 v with optimized common path . . . . . . . . . . . . . 43 figure 56. stw77n65m5 eon@20 a, 2.2 w with no n-optimized common path . . . . . . . . . . . . . . . . 44 figure 57. stw77n65m5 eon@20 a, 2.2 w with non-optimized common path. . . . . . . . . . . . . . . . . 44 figure 58. stw77n65m5 eon@20 a, 2.2 w with optimized common path . . . . . . . . . . . . . . . . . . . . 44 figure 59. stw77n65m5 eon@20 a, 2.2 w with optimized common path . . . . . . . . . . . . . . . . . . . . 44 figure 60. stw77n65m5 eon@40 a, 2.2 w with non-optimized common path. . . . . . . . . . . . . . . . . 45 figure 61. stw77n65m5 eon@40 a, 2.2 w with non-optimized common path. . . . . . . . . . . . . . . . . 45 figure 62. stw77n65m5 eon@40 a, 2.2 w with optimized common path . . . . . . . . . . . . . . . . . . . . 45 figure 63. stw77n65m5 eon@40 a, 2.2 w with optimized common path . . . . . . . . . . . . . . . . . . 45 figure 64. schematic of 4-pin solution . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 46 figure 65. stw77n65m5 energy on difference betw een the optimized layout (3-pin) and 4-pin solution . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 46 figure 66. stw77n65m5 energy on difference betw een the optimized layout (3-pin) and 4-pin solution . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 47 figure 67. stw77n65m5 energy off difference between the optimized layout (3-pin) and 4-pin solution . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 47 figure 68. stw77n65m5 eoff@20 a, 2.2 w, 400 v 4-pin solution. . . . . . . . . . . . . . . . . . . . . . . . . . . 48 figure 69. stw77n65m5 eon@20 a, 2.2 w 4-pin solution . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 48 figure 70. stw77n65m5 eon @20 a, 2.2 w 4-pin solution . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 48 figure 71. stw77n65m5 eon@40 a, 2.2 w 4-pin solution . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 49 figure 72. stw77n65m5 eon@40 a, 2.2 w 4-pin solution . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 49 figure 73. basic driving stage of a power mosfet at turn-off with negative vgm . . . . . . . . . . . . . . 49 figure 74. stw77n65m5 eoff@52 a, 4.7 w, 400 v, vgmoff=-5 v . . . . . . . . . . . . . . . . . . . . . . . . . . 50 figure 75. stw77n65m5 eoff@52 a, 4.7 w, 400 v, vgmoff=-5 v . . . . . . . . . . . . . . . . . . . . . . . . . . 50
AN3994 st multidrain technology evolution doc id 022380 rev 1 5/53 1 st multidrain technology evolution at the beginning of 2000, stmicroelectronics introduced the super junction mosfet technology to the market, the basic structure of which is clear from figure 1 : figure 1. standard hv mosfet device cross section figure 2. md device cross section as concerns standard mosfet technology, designers understand that r ds(on) * area and breakdown voltage are associated with a theoretical limit which strictly depends on the material and can not be overcome. development efforts of the major suppliers have mainly focused on making the r ds(on) * area as close as possible to this physical limit, by reducing the most important contributions of a high voltage power mosfet to the total r ds(on) . !-v 3ource -etal "ody . region ! $rain 3ubstrate " !-v 3ource -etal "ody 3ubstrate " ! $rain 1sfhjpo /sfhjpo -$mesh?
st multidrain technology evolution AN3994 6/53 doc id 022380 rev 1 figure 3. silicon ideal limit, sj limit and st md v position r jfet and r channel were significantly lowered by increasing the cell density and optimizing their structure, and by also reducing, at the same time, the channel length. thanks to the continuos optimization of resistivity and the thickness of n-drift, the r epy contribution has been lowered, but the need to guarantee the same breakdown voltage and avalanche capability establishes the well kn own ?silicon ideal limit?, as shown in figure 3 . the md concept, based on sj technology, has overcome this limit: through the p-doped column insertion under the devi ce strips, it has been possible to significantly lower the resistivity of the epitaxial n region without compromising the breakdown capability and enabling a dramatic reduction in r ds(on) : the particular p-column geometry and the alternating of p regions with n regions allows a constant electric field in the whole drain volume despite the low resistivity in the conducting region: as a direct consequence, it was possible to achieve an r ds(on) * area reduction, previously not possible, by keeping the same voltage capability. from this starting point, md technology moved towards r ds(on) continuous optimization, as seen in figure 4 . !-v 0' 6l ,*%7 6l ,*%7 6l6- 3/lplw "reakdownvoltage6 2
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AN3994 st multidrain technology evolution doc id 022380 rev 1 7/53 figure 4. st?s hv technology evolution the md ii generation has already optimized the r ds(on) * area of about 40% compared to the first md version, with an average value of about 30 m *cm 2 . the excellent achievement of the md ii enabled stmicroelectronics to establish a new milestone in the power switch arena with the last md v generation. thanks to a proprietary st technology, an extremely low value of p-column distance has been reached, therefore overcoming the physical limit imposed by the diffusion process. additionally, the geometry of the p-columns was also optimized by a more effective diffusion process which enabled up to 40% reduction of r ds(on) * area if compared to the previous md ii generation. !-v 2
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parasitic capacitances overview AN3994 8/53 doc id 022380 rev 1 2 parasitic capacitances overview when dealing with high speed switching applications, the most critical mosfet parameters limiting its dynamic response are the parasitic capacitances. figure 5 shows the physical origin of the parasitic component in an n-channel power mosfet: figure 5. n-channel power mosfet structure and intrinsic capacitances figure 6. equivalent model of power mosfet intrinsic capacitances c gs is mainly due to the overlap between the ga te and the source meta llization (?3? and ?4? components in figure 5 and 6 ). capacitors ?5? and ?6? are mis (metal-insulator- semiconductor) capacitors between the gate and the p-body. the c gs value is linked to the geometry of the device and it's almost independent of the voltage applied. am1076 8 v1 s o u rce met a l s o u rce met a l 4 intermedi a te dielectric 4 intermedi a te dielectric 2 1 5 6 4 3 poly s ilicon g a te g a te oxide n ++ s o u rce n ++ s o u rce 2 1 5 6 4 3 poly s ilicon g a te g a te oxide n ++ s o u rce n ++ s o u rce 2 5 p/p + body p/p + body 2 5 p/p + body p/p + body 7 n - dr a in 7 n - dr a in !-v $ ' 3 he # ht # et #
AN3994 parasitic capacitances overview doc id 022380 rev 1 9/53 c gd is the sum of two contributions: the first one is related to the overlap of the jfet region and the gate electrode (?1? component in figure 5 and 6 ). the second component is the capacitance of the depletion region under the gate (?2? component in figure 5 and 6 ). the equivalent capacitance c gd decreases as the drain source voltage applied increases. c ds capacitance is the junction capacitance of the body-drain diode (?7? components in figure 5 and 6 ). its value varies as the p-body / n-drift junction thickness changes with the v ds applied, according to the following formula: equation 1 the relevant datasheets report the static equivalent capacitance values in the electrical characteristics as the following: equation 2 equation 3 equation 4 c gd is also called ?miller capacitance?, as it?s pl aced in the feedback loop between the input and the output of the device. it's value can be much larger in switching operations, contributing to the achievement of a dynamic input capacitance of the mosfet larger than the sum of the static capacitances. in order to simplify the switching performance comparison among mosfets from different manufacturers or even different mosfet technologies of the same brand, it can be useful to consider the gate charge parameters instead of capacitances. figure 7 shows a clamped inductive load switching test circuit which helps to analyze the parasitic capacitance behavior during the mosfet switching. the considerations reported in the following sections are valid if the driving source is supposed to provide any ig current to the mosfet input capacitances and the circuit is ideal with no stray inductances. ) v ( c ds ds measured @ v gs =0 v, v ds =25 v ? gd gs iss c c c = measured @ v gs =0 v, v ds =25 v ? gd rss c c = measured @ v gs =0 v, v ds =25 v ? gd ds oss c c c =
parasitic capacitances overview AN3994 10/53 doc id 022380 rev 1 figure 7. clamped inductive load test circuit used to carry out the dynamic tests on the mosfets !-v 6 '- 6 6 $$ 6 ) , $ , 2 'on 2 'off ) $
AN3994 mosfet standard turn-on and turn-off analysis doc id 022380 rev 1 11/53 3 mosfet standard turn-on and turn-off analysis the turn-on event of the mosfet can be split into four time intervals, as figure 8 shows. the analysis starts from the hypoth esis of a constant load current i l flowing through the inductor l and the diode d before the commutation (turn-on) process. after the mosfet input has been connected to the voltage source (v source =v gm ), the v gs voltage starts to increase (phase ?1?), but no drain current can flow till the v gs reaches the v th value. the mosfet is still in off st ate, while the diode is conducting the load current. the gate current i gon is charging the c iss capacitance. the on gate current during the t 0 to t 2 time interval follows the exponential trend of equation 5 : equation 5 r gtot theoretically includes the r gon value (see figure 7 ) and the other resistive components of the driving circuit. equation 6 assumes that the c iss (v ds ) is constant during this time interval, which is a correct hypothesis, due to a very low dependence of the input capacitances on the v ds applied. phase ?2? is the phase of i d rise. when v gs reaches the threshold value, i d begins to rise and at the same time, the load current begi ns to be shared between the diode and the mosfet. until the i d is lower than the load current and the diode is in an on state, the v ds stays constant at the maximum value except for a little drop in the real voltage waveform due to the stray inductances along the switching circuit. the i gon current is still charging the c gs +c gd capacitances. at t 2 instant the v gs reaches the plateau value. the rate of i d current during the t 1 to t 2 time interval satisfies equation 6 : equation 6 during phase ?3? and phase ?4? v gs is at a constant value, i d has reached the full load condition and the diode is turned off. this enables the v ds to decrease. the mosfet is in the active region and the i g current is now flowing only through the c gd capacitance that?s discharging from a starting value of (v ds -v pl ), while the c ds capacitance is discharging from v ds down to the v ds(on) value. the on gate current during the time interval (t 2 to t 4 ) is a fixed value and it satisfies equation 7 : equation 7 iss gtot 2 0 c r t gtot gm ) t , t ( gon e r v ) t ( i ? = iss ) t , t ( gon m d c i g dt di 2 1 = gtot pl gm ) t , t ( gon r v v i 4 2 ? =
mosfet standard turn-on and turn-off analysis AN3994 12/53 doc id 022380 rev 1 figure 8. turn-on of a mosfet in a clamped inductive load figure 9. equivalent capacitive model of a mosfet falling rate of v ds during the (t 2 to t 4 ) time interval is shown in equation 8 : equation 8 !-v 6 0(!3%hv 0(!3% h v )6 6 $3 ) $ 0(!3% 0(!3%hv 0(!3% hv 0(!3%hv $ 6 '- 6 '3 1 1 th 1 t 1 1 t t t t t t ) ' 6 '3th 1 1 1 1 1 t h 1 1 !-v 6 $$ $ , 2 ' # '$ # $3 ) $' 6 '$ 6 $3 ) $3 ' $ # '3 6 '- ) $ 3 ) '3 6 '3 ' '- gd gtot pl gm gd ) t , t ( gon ds c r v v c i dt dv 4 2 ? ? = =
AN3994 mosfet standard turn-on and turn-off analysis doc id 022380 rev 1 13/53 during phase ?4? the voltage acro ss the mosfet has reached the i d *r ds(on) =v ds(on) value, and the device has entered the ohmic region. the v gs increases up to the maximum value v gm . figure 10. turn-off of a mosfet in a clamped inductive load similarly, the turn-off event can be split into four time intervals, as shown in figure 10 . phase ?1? is the time interval needed to discharge the input capacitance c iss from its initial value (+v gm ) down to the plateau level. the gate current is supplied by both c gs and c gd capacitors. the i goff current during the time interval (t' 0 to t' 1 ) follows the same exponential trend of the turn-on during the (t 0 , t 2 ) time interval according to equation 9 : equation 9 during phase ?2? the gate voltage has reached a fixed value (the plateau level) and the v ds rises from i d *r ds(on) =v ds(on) up to the final value, where it is clamped by the diode. as v gs is constant in this time interval, the off gate current flowing through the r gtot is the charging current of the c gd that is charging from a nega tive starting voltage value (see figure 8 for reference) up to the v ds value, while the c ds capacitor is charging up to v ds . i goff current during this phase follows equation 10 : equation 10 phase ?3? is the phase of the diode turn-on: load current begins to be shared between the mosfet and the diode while the v gs decreases from the plateau down to the v th value. !-v 0(!3%hv )6 6 $3 ) $ ) g 0(!3%hv 0(!3%hv 0(!3%hv )g 6 '- 6 '3 6 th 1 t 1 t t t t t t t 1 1 ) t , t ( gon ) t , t ( goff 2 0 ' 1 ' 0 i i ? = gtot pl ) t , t ( goff r v i ' 3 ' 1 =
mosfet standard turn-on and turn-off analysis AN3994 14/53 doc id 022380 rev 1 this causes the lowering of the drain current down to zero. during this time interval, the gate current is mainly coming from the c gs capacitor. i goff current during this phase has the following expression: equation 11 during phase ?4?, the c iss fully discharges and the v gs reaches the zero value. t>t? 3 iss gtot ' 3 ' 4 ' 3 c r t t gtot pl ) t , t ( goff e r v ) t ( i ? ? =
AN3994 gate charge curve impact on dynamic responses doc id 022380 rev 1 15/53 4 gate charge curve impact on dynamic responses when generally dealing with mosfet turn-on and turn-off, it implies the charging or discharging of its input capacitances. the charge transfer needed to change the voltage across these capacitors leads to unavoidable po wer losses which are dissipated on the gate resistors in the driving path during each switching cycle. a second but not less significant aspect is that the amount of charge direct ly impacts how fast th e mosfet response is during transients. for this reason, the gate c harge curve analysis displayed in the datasheet is quite important in order to obtain a first outlook of the mosfet dynamics. as for the turn-on event, the q th charge supplied during the t 0 to t 1 ( figure 8 ) time interval is approximately: equation 12 as v gs reaches the threshold value, v th and i d start to flow. the charge to be provided during the (t 1 to t 2 ) time interval can be calculated by integrating the i gon (t 1 to t 2 ) current as follows: equation 13 if we assume: equation 14 equation 13 can be solved and the value of t can be calculated as: equation 15 the total charge supplied to the gate during the time interval (t 2 to t 3 ) can be easily calculated by multiplying the constant i gon value with the time interval (t 2 to t 3 ) as follows: equation 16 equation 17 th iss th v c q ? = dt e r v q iss gtot 2 1 c r t t t gtot gm 12 ? = t t t 1 2 + = ? ) q q 1 ln( c r t t t th 12 iss gtot 1 2 ? ? ? ? = ? = ? ) t t ( r v v ) t t ( i q 2 3 gtot pl gm 2 3 ) t , t ( gon 3 2 3 2 ? ? ? = ? ? = gtot pl gm 23 2 3 r ) v v ( q t t ? = ?
gate charge curve impact on dynamic responses AN3994 16/53 doc id 022380 rev 1 time intervals (t 2 - t 1 ) and (t 3 - t 2 ) theoretically calculated by equation 5 and 17 are the two ones mainly involved in the turn-on event. as similarly done for the turn-on, once the q' 23 +q' 34 = q 23 +q 12 (if referred to the turn-off, see figure 10 ) portion of the gate charge has been read from the gate charge curve, the two time intervals (t' 3 - t' 2 ) and (t' 4 - t' 3 ) which are mainly involved in the turn-off event can be theoretically calculated as follows: equation 18 equation 19 time intervals of equation 15 , 17 and equation 18 , 19 have been calculated by assuming that the mosfet works at t j =25 c. if the mosfet is supposed to work in a real application, the v th dependence on temperature must be considered. having read the total gate charge q g =q th +q 12 +q 23 +q 34 +q 4 (value at the v gm voltage level which is usually 10 v) (the curve v gs vs. q g is displayed in the mosfet datasheet), the total power loss needed to charge the gate is: equation 20 so, by comparing the total gate charge of two mosfets, measured under the same test conditions of i d , v ds , i g , it is possible to understand which of them requires the lowest driving energy if the same v gm and f sw is considered. ta bl e 1 shows the total q g values of four couples of md v/md ii power mosfets with similar r ds(on) . the q g value of each device has been calculated from the v gs (t) curve of each device (see figure 11 and 12 for reference) and measured on bench at the same i d and v ds levels at t c =25 c. the newest md v guarantees a lower q g value than its equivalent md ii part, this leads to less effort in terms of driving energy requirements. table 1. experimentally measured q g of four couples of md v/md ii part number r ds(on)max @10 v, 25c q g @400 v, i d (a) stp16n65m5 279 m 28.4 nc@6 a stp18nm60n 285 m 31.2 nc@6 a stp21n65m5 179 m 40.4 nc@8 a stp24nm60n 190 m 42.3 nc@8 a stp35n65m5 98 m 77.4 nc@15 a stb36nm60n 105 m 80.1 nc@15 a stb42n65m5 79 m 96 nc@16 a stw48nm60n 70 m 122 nc@16 a pl gtot 23 ' 2 ' 3 v r * ' q ) t t ( = ? ? ) c * v ' q 1 ln( * c * r ) t t ( iss pl 34 iss gtot ' 3 ' 4 ? ? = ? sw gm g gate f * v * q p =
AN3994 gate charge curve impact on dynamic responses doc id 022380 rev 1 17/53 in addition to the gate drive power losses, another contribution to the total switching loss is due to the i d -v ds cross. if the turn-on event is considered, the main contribution over the total power dissipation is provided during phase ?2? (current rise) and ?3? (voltage lowering) of figure 8 , so the time intervals mainly involved are (t 1 to t 2 ), when the gate voltage is between v th and v pl , and the time interval (t 2 to t 3 ) when the gate voltage is at the miller value. both of them have been calculated by equation 15 and 17 . as for turn-off, the two time intervals mainly involved in the event are (t' 2 to t' 3 ) when the voltage rises up to the clamp value, and (t' 3 to t' 4 ) when the i d current falls (refer to figure 10 ). both of them have been theoretically calculated by equation 18 and 19 . the correspondence between the gate charge curve and the switching times involved in the turn-on/off event is verified until no other external phenomenon arises to change the i-v cross time duration (negligible layout parasitic inductances/capacitors, no/negligible peak recovery current of the clamp diode). figure 13 , 15 and figure 14 , 16 show the turn-on and the turn-off of the fourth compared couple of ta b l e 1 , experimentally measured at the same current/voltage conditions of the gate charge test in figure 11 and 12 with an external r gon =47 . the effect of these parameters is shown in ta b l e 2 which reports the theoretical turn-on and turn-off switching times calculated by equation 15 , 17 and equation 18 , 19 compared to the turn-on and turn- off times experimentally measured on the same devices. figure 11. vg(t) curve measured on stb42nm60n @16 a, 400 v, i g =1.5 ma figure 12. vg(t) curve measured on stw48nm60n @16 a, 400 v, i g =1.5 ma table 2. experimentally and theoretically measured switching times and related static parameters v pl @16 a q 12 q ?34 q 23 q ?23 experimental t sw(on) (tot) theoretical t sw(on) (tot) experimental t sw(off) (tot) theoretical t sw(off) (tot) stb42n65m5 5.6v 5.2nc 5nc 115ns 133ns 80ns 89ns stw48nm60n 4.8v 4.5nc 4.5nc 105ns 114ns 90ns 96ns
gate charge curve impact on dynamic responses AN3994 18/53 doc id 022380 rev 1 referring to equation 15 , 17 and equation 18 , 19 , it's clear that q 12 +q 23 and the v pl are the two main actors impacting on the turn-on switching times. similarly, q' 23 +q' 34 and v pl mainly influence the turn-off switching times. it's important to note that a device with higher v pl than another, also exhibits higher v th at the same i d current. as far as the md v and md ii devices in ta bl e 2 are concerned, the stb42n65m5 shows slightly higher q 12 and q 23 charge portions than the stw 48nm60n. if the other static parameters are supposed to be the same for both devices, this should be enough to have both turn-on times and turn-off times of the md v device which are wider than md ii ones. additionally, the md v part exhibits a higher v pl value than the md ii: this further worsens both (t 2 - t 1 ) and (t 3 - t 2 ) contributions (see equation 15 and 17 ) on the turn-on switching times. on the other hand, a higher v pl helps to reduce turn-off switching times, as can be verified by inspecting equation 18 and 19 . in the end, turn-on times of the md v are wider than the md ii device due to a higher gate charge portion and v pl , while the same static parameters favor the md v at turn-off. the different impact of the v pl on turn-on and turn-off is also evident from equation 7 , 10 , 11 , as a higher plateau level of the md v is directly linked to a lower i gon charging current during the entire turn-on event; the same higher v pl of the md v results in a higher i goff discharging current which helps to speed up the turn-off event. the theoretical switchin g times calculated by equation 15 , 17 and equation 18 , 19 can also be used to obtain a preliminary idea of what value of r gtot in the driving stage must be adopted to guarantee a specific time interval for the turn-on or turn-off. it is anyway important to remark that the on and off energy losses depend on several factors, like: 1. the circuit the mosfet is working in (the test circuit considered in this work is a simple single ended clamped inductive load circuit); 2. the output capacita nce of the mosfet which exhibits a different voltage dependence if different sj mosfet families are cons idered (this impacts on the voltage raising/lowering of the mosfet during the transients); 3. the parasitic capacitances and inductors of the layout wh ich can significantly impact on the current and voltage slopes. all these ef fects sometimes modify the energy loss wave, and this is the reason why there is not always an exact correspondence between the switching time interval comparison and the energy value comparison in the same match.
AN3994 gate charge curve impact on dynamic responses doc id 022380 rev 1 19/53 so, v gs vs. q g curve is very important for at least two reasons: it provides information on the energy required to turn on/off the mosfet and at the same time, it gives a rough idea of the mosfet dynamics. figure 13. turn-on of stb42n65m5 @16 a, 400 v, 47 figure 14. turn-on of stw48nm60n @16 a, 400 v, 47 figure 15. turn-off of stb42n65m5 @16 a, 400 v, 47 figure 16. turn-off of stw48nm60n @16 a, 400 v, 47
latest st md ii and md v technology at a glance AN3994 20/53 doc id 022380 rev 1 5 latest st md ii and md v technology at a glance with the mdmesh v family, stmicroelectronics reaches the lowest r ds(on) value per package among its hv sj mosfet technology product range. for example, figure 17 reports the lowest r ds(on)max achievable by the last two md ii and md v product families. figure 17. minimum r ds(on) per package achievable by md ii and md v the md v shows lower specific r ds(on) if compared to its predecessor. as a consequence of this improvement, the r ds(on) per package is also lowered, therefore allowing the same device to be housed in a smaller package, which was not possible before. besides the r ds(on) , it is important to take into account the driving energy required to turn on/off the device. in order to satisfy this requirement, the md v guarantees lower total gate charge than the md ii at the same i d ,v ds and r ds(on) values (as shown in ta b l e 1 ), allowing to significantly reduce the driving losses and increase the total system efficiency. the reduced r ds(on) values per package of md v leads to a slight increase in thermal resistance, but this is counterbalanced by an overall static and dynamic energy loss improvement if compared to the previous md ii generation. some except ions on this last statement arise when small devices of the two families are compared at very low current levels, as is shown in the next section. !-v -$)) -$6 $0! + 4/ 4/ -!8 34$.-. 340.-. 340.- 347.-. 347.- 349.-. 349 .- 2 $3on m/hm 34$.-
AN3994 md ii and md v: which is the lowest loss one? doc id 022380 rev 1 21/53 6 md ii and md v: which is the lowest loss one? a dynamic on bench comparison has been ca rried out on four different md v/md ii mosfet couples in order to provide a reliable idea of their dynamic performances. all tests have been issued by the same simple clamped inductive load test circuit (refer to figure 7 ) where the effects of parasitic elements have been reduced in order to make the effective mosfet behavior more understandable. a 600 v,10 a sic diode has been used as the clamp diode. the matches obtained under evaluation are those displayed in ta b l e 1 . the following graphs show the energy on, the energy off, the di/dt, the dv/dt both at turn-on and turn-off of each compared match for different r g values, and two i d current levels. 6.1 stb42n65m5 vs. stw48nm60n figure 18. stb42n65m5 vs. stw48nm60n e on @ 8 a/16 a, 400 v figure 19. stb42n65m5 vs. stw48nm60n di/dt at turn-on @ 8 a/16 a, 400 v !-v (?- (#$97f ?& 67%10yv67:101 67%10$ 67:101$ 67%10$ 67:101$ 52kp &rqglwlrqv 9 99 9 $$ '3 ' on on !-v glg7$?v 52kp glgwdwwxuqrq#$97f ?# 67%10yv67:101 67%10$ 67:101$ 67%10$ 67:101$ &rqglwlrqv 9 99 9 $$ '3 '
md ii and md v: which is the lowest loss one? AN3994 22/53 doc id 022380 rev 1 figure 20. stb42n65m5 vs. stw48nm60n dv/dt at turn-on @ 8 a/16 a 400 v figure 21. stb42n65m5 vs. stw48nm60n zoom of dv/dt at turn-on @ 8 a/16 a 400 v !-v gyg79qv dvdtatturn on !64c ?# 34".-vs347.-. 67%10$ 67:101$ 67%10$ 67:101$ 52kp &rqglwlrqv 9 99 9 $$ '3 ' !-v gyg79qv gygwdwwxuqrq#$97f ?& 67%10yv67:101 67%1 0$ 67:101$ 67%1 0$ 67:101$ 52kp &rqglwlrqv 9 99 9 $$ '3 '
AN3994 md ii and md v: which is the lowest loss one? doc id 022380 rev 1 23/53 figure 22. stb42n65m5 vs. stw48nm60n e off @ 8 a/16 a, 400 v figure 23. stb42n65m5 vs. stw48nm60n di/dt at turn-off @ 8 a/16 a, 400 v !-v (?- % !64c ?# 34".-vs347.-. 67%10$ 67:101$ 67%10$ 67:101$ 52kp &rqglwlrqv 9 99 9 $$ '3 ' off off !-v glg7$?v didtatturn off !64c ?# 34".-vs347.-. 67%10$ 67:101$ 67%10$ 67:101$ 52kp &rqglwlrqv 9 99 9 $$ '3 '
md ii and md v: which is the lowest loss one? AN3994 24/53 doc id 022380 rev 1 figure 24. stb42n65m5 vs. stw48nm60n dv/dt at turn-off @ 8 a/ 16 a, 400 v 6.2 stp35n65m5 vs. stb36nm60n figure 25. stp35n65m5 vs. stb36nm60n e on @ 7.5 a/15 a, 400 v !-v gyg79qv dvdtatturn off !64c ?# 34".-vs347.-. 67%10$ 67:101$ 67%10$ 67:101$ 52kp &rqglwlrqv 9 99 9 $$ '3 ' !-v (?- % !!64c ?# 340.-vs34".-. 67310$ 673101$ 67310$ 673101$ 52kp &rqglwlrqv 9 99 9 $$ '3 ' on on
AN3994 md ii and md v: which is the lowest loss one? doc id 022380 rev 1 25/53 figure 26. stp35n65m5 vs. stb36nm60n di/dt at turn-on @ 7.5 a/15 a, 400 v figure 27. stp35n65m5 vs. stb36nm60n dv/dt at turn-on @ 7.5 a/15 a 400 v !-v glg7$?v didtatturn on !!64c ?# 340.-vs34".-. 67310$ 67%101$ 67310$ 67%101$ 52kp &rqglwlrqv 9 99 9 $$ '3 ' !-v gyg79qv dvdtatturn on !!64c ?# 340.-vs34".-. 67310$ 67%101$ 67310$ 67%101$ 52kp &rqglwlrqv 9 99 9 $$ '3 '
md ii and md v: which is the lowest loss one? AN3994 26/53 doc id 022380 rev 1 figure 28. stp35n65m5 vs. stb36nm60n e off @ 7.5 a/15 a, 400 v figure 29. stp35n65m5 vs. stb36nm60n di/dt at turn-off @ 7.5 a/15 a, 400 v !-v (?- % !!64c ?# 340.-vs34".-. 67310$ 67%101$ 67310$ 67%101$ 52kp &rqglwlrqv 9 99 9 $$ '3 ' off pgg !-v glg7$?v didtatturn off !!64c ?# 340.-vs34".-. 67310$ 67%101$ 67310$ 67%101$ 52kp &rqglwlrqv 9 99 9 $$ '3 '
AN3994 md ii and md v: which is the lowest loss one? doc id 022380 rev 1 27/53 figure 30. stp35n65m5 vs. stb36nm60n dv/dt at turn-off @ 7.5 a/15 a, 400 v 6.3 stp21n65m5 vs. stp24nm60n figure 31. stp21n65m5 vs. stp24nm60n e on @ 4 a/ 8 a, 400 v !-v gyg79qv dvdtatturn off !!64c ?# 340.-vs34".-. 67310$ 67%101$ 67310$ 67%101$ 52kp &rqglwlrqv 9 99 9 $$ '3 ' !-v (?- % !!64c ?# 340.-vs340.-. 67310$ 673101$ 67310$ 673101$ 52kp &rqglwlrqv 9 99 9 $$ '3 ' on on
md ii and md v: which is the lowest loss one? AN3994 28/53 doc id 022380 rev 1 figure 32. stp21n65m5 vs. stp24nm60n di/dt at turn-on @ 4 a/8 a, 400 v figure 33. stp21n65m5 vs. stp24nm60n dv/dt at turn-on @ 4 a/8 a, 400 v !-v glg7$?v didtatturn on !!64c ? # 340.-vs340.-. 67310$ 673101$ 67310$ 673101$ 52kp &rqglwlrqv 9 99 9 $$ '3 ' !-v gyg79qv dvdtatturn on !!64c ?# 340.-vs340.-. 67310$ 673101$ 67310$ 673101$ 52kp &rqglwlrqv 9 99 9 $$ '3 '
AN3994 md ii and md v: which is the lowest loss one? doc id 022380 rev 1 29/53 figure 34. stp21n65m5 vs. stp24nm60n e off @ 4 a/8 a, 400 v figure 35. stp21n65m5 vs. stp24nm60n di/dt at turn-off @ 4 a/8 a, 400 v !-v (?- % !!64c ? # 340.-vs340.-. 67310$ 673101$ 67310$ 673101$ 52kp &rqglwlrqv 9 99 9 $$ '3 ' off off !-v glg7$?v didtatturn off !!64c ? # 340.-vs340.-. 67310$ 673101$ 67310$ 673101$ 52kp &rqglwlrqv 9 99 9 $$ '3 '
md ii and md v: which is the lowest loss one? AN3994 30/53 doc id 022380 rev 1 figure 36. stp21n65m5 vs. stp24nm60n dv/dt at turn-off @ 4 a/8 a, 400 v 6.4 stp16n65m5 vs. stp18nm60n figure 37. stp16n65m5 vs. stp18nm60n e on @ 3 a/6 a, 400 v !-v 52kp &rqglwlrqv 9 99 9 $$ '3 ' gyg79qv dvdtatturn off !!64c ? # 340.-vs340.-. 67310$ 673101$ 67310$ 673101$ !-v (?- 52kp % !!64c ?# 340.-vs340.-. 67310$ 673101$ 67310$ 673101$ on on '
AN3994 md ii and md v: which is the lowest loss one? doc id 022380 rev 1 31/53 figure 38. stp16n65m5 vs. stp18nm60n di/dt at turn-on @ 3 a/ 6 a, 400 v figure 39. stp16n65m5 vs. stp18nm60n dv/dt at turn-on @ 3 a/6 a, 400 v !-v glg7$?v 52kp didtatturn on !!64c ?# 340.-vs340.-. 67310$ 673101$ 67310$ 673101$ ' !-v gyg79qv 52kp dvdtatturn on !!64c ? # 340.-vs340.-. 67310$ 673101$ 67310$ 673101$ '
md ii and md v: which is the lowest loss one? AN3994 32/53 doc id 022380 rev 1 figure 40. stp16n65m5 vs. stp18nm60n e off @ 3 a/6 a, 400 v figure 41. stp16n65m5 vs. stp18nm60n di/dt at turn-off @ 3 a/6 a, 400 v !-v %?* % !!64c ?# 340.-vs340.-. 340.-! 340.-.! 340.-! 340.-.! 52kp &rqglwlrqv 9 99 9 $$ '3 ' pgg pgg !-v did4!?s didtatturn off !!64 # ?# 340.-vs340.-. 340.-! 340.-.! 340.-! 340.-.! 52kp &rqglwlrqv 9 99 9 $$ '3 '
AN3994 md ii and md v: which is the lowest loss one? doc id 022380 rev 1 33/53 figure 42. stp16n65m5 vs. stp18nm60n dv/dt at turn-off @ 3 a/6 a, 400 v 6.5 comments about energy on comparison considerations about energy comparison between the md v and the md ii depend on the gate resistor selected by the user. as for turn-on energy, the bigger sizes of the md v list considered in this work (stp42n65m5 and stp35n65m5) perform worse than their equivalent md ii parts in the entire r g range at the two current levels selected for the tests. this is due to the negative gate charge impact (the q 12 +q 23 portion, as explained in section 4 ) together with the higher threshold and plateau value of these parts if compared to the md ii devices. smaller sizes show a slightly different dynamic behavior: md v parts (stp21n65m5 and stp16 n65m5) perform worse than their equivalent md ii parts at relative medium/high r g values (i.e. r g >10 for the stp21n65m5, and r g >22 for the stp16n65m5). this situation changes if low r g values are used. under the latter driving condition, the md v performs better than the md ii but, it is not advised to adopt very low r g values in most common situations due to the increased voltage /current slopes of these small devices and the consequent increased risk of spurious oscillations. anyway, if an md v part (belonging to the list in ta b l e 1 ) is used in any circuit with a specific r gon value, and it needs to be replaced with an equivalent md ii part by keeping the same e on energy, this can be easily obtained by increasing its r gon value according to the charts showing the e on comparison reported in this work. the same way of proceeding can be adopted if an md v device must be used instead of an md ii equivalent part. 6.6 comments about energy off comparison as for turn-off, all md v devices show better performances than their equivalent md ii parts. some exceptions arise for the smaller sizes (stp21n65m5 and stp16n65m5) when current levels are significantly lower than the nominal current (see figure 34 and 40 ). the slightly worse md v energy at very low cu rrent levels is linked to the behavior of the mosfet intrinsic capacitances. output capacitance is charged up to v clamp during !-v dvd46ns dvdtatturn off !!64 # ?# 340.-vs340.-. 340.-! 340.-.! 340.-! 340.-.! 52kp &rqglwlrqv 9 99 9 $$ '3 '
md ii and md v: which is the lowest loss one? AN3994 34/53 doc id 022380 rev 1 turn-off and the energy stored during this event is added to the effective energy dissipated at turn-on in the next cycle in hard switching conditions, according to equation 21 : equation 21 as the current becomes lower and lower, the effective energy dissipated by the mosfet decreases and the measured off energy is only the energy required by the output capacitance to enable the turn-off. this is the reason why all e off curves exhibit a flat trend at low current/low r goff values. if the energy required by the md v output capacitances is higher than that of the md ii, this leads to a higher measured e off value for the md v if compared to the md ii at the same i d , v clamp values. a specific test was performed on all md v/md ii matches analyzed in this work to confirm the different output capacitance behavior. as output capacitance of a mosfet is voltage dependant, a constant equivalent capacitance which stores the same energy of the output switch capacitance in the entire (0 v to v clamp =0 v to 400 v) excursion has been calculated. the mosfet is really being turned off in an unclamped inductive load test circuit and the total energy stored in the inductor is: equation 22 this inductive energy is supposed to be app lied to a constant capaci tance which charges up to v clamp : equation 23 ta bl e 3 shows the c oav measured on all md v/md ii devices: table 3. c oav experimentally measured on md v/md ii devices part number c 0av @400 v stp16n65m5 67 pf stp18nm60n 64 pf stp21n65m5 79 pf stp24nm60n 75 pf stp35n65m5 131 pf stb36nm60n 109 pf stb42n65m5 155 pf stw48nm60n 162 pf ) c ( e ) measured ( e ) diss ( e ) c ( e ) measured ( e ) diss ( e 0 on on o off off + = ? = 2 i * l 2 1 ) inductive ( e ? = 2 cla mp 2 av 0 i l 2 1 v c 2 1 ? ? = ? ?
AN3994 md ii and md v: which is the lowest loss one? doc id 022380 rev 1 35/53 ta bl e 3 explains why the measured e off energies of md v stp16n65m5, stp21n65m5 and stp35n65m5 are slightly worse than the md ii at very low current values and low r goff values. anyway, the difference in terms of e off between the small sizes of md v and md ii is so small that the two families ca n be considered as having the same dynamic performances under the above specified co nditions of current and r g .
mosfet critical parameters in high switching environments AN3994 36/53 doc id 022380 rev 1 7 mosfet critical parameters in high switching environments 7.1 parasitic inductance in fluence on switching losses when considering the power mosfet switching characteristics, the influence of parasitic inductances must be carefully considered. among the three main actors in a power circuit (the gate loop inductance, the common source inductance, and the main switching loop inductance) the common source inductance and the main switching loop inductance are the most critical and their respective action can not always be identified. anyway, in most practical cases it is possible to understand what kind of parasitic inductance has the greater contribution over the other one by directly inspecting the switching waveforms. if mosfet transient is considered, the instantaneous drain current i d (t) and the instantaneous gate to source voltage v gs (t) satisfies equation 24 : equation 24 the drain to source voltage v ds changes its value due to the voltage across the parasitic inductances according to the formula: equation 25 (see figure 43 .) gate to source voltage v gs (t) satisfies equation 26 : equation 26 figure 43. equivalent capacitive model of a mosfet with parasitic inductances at turn-on ) v ) t ( v ( g ) t ( i th gs fs d ? ? = ) l l ( dt di v v d s d dd ds ? ? = ? dt ) i i ( d l ) t ( v ) dt dv c dt dv c ( r v gs d s gs gd gd gs gs tot g gm + + + ? = !-v 2 ' # '$ # '3 # $3 6 '- ) $ 6 $$ 3 ) $' ) '3 6 '$ 6 '3 6 $3 ) $3 , $ ' $ , 3
AN3994 mosfet critical parameters in high switching environments doc id 022380 rev 1 37/53 both parasitic inductances (drain and common source) impact on the v gs (t) and i g (t) waveforms, as the voltage across the ls is di rectly subtracted (or added in the case of a turn-off event) from the input v gm , while the voltage induced across the l d changes the voltage value of the c ds capacitance. the effect of both inductances on the v gs (t), i d (t) and v ds depends on the relative values of l d and l s , rather than r g and the internal mosfet capacitances c gd and c gs . under high current levels and low l s values, the mosfet experiences high voltage overshoot during turn-off. additionally, the voltage across the l d during the positive di/dt at turn-on is subtracted from the v ds voltage across the switch and this is evident as a ?missing step? in the voltage waveform. figure 44. turn-on of stw77n65m5@400 v, 13 a, 25 c figure 44 shows the turn-on of the stw77n65m5 working in the steval-isf001v1 3 kw pfc, where the parasitic source inductance has been dramatically cut thanks to the 4-pin solution (explained in section 7.2 ). nevertheless, the parasitic drain component is still present, causing the typical ?missing step? in the voltage waveform. on the contrary, as the l s value becomes significant if compared to the l d value, the driving loop circuit has a relevant impact on the switching behavior, slowing down the i d current. this implies an energy loss which worsens both at turn-on and at turn-off. in the following sections, the impact of common source inductance and the main switching loop inductance is analyzed by making the hy pothesis of neglecting one of the two contributors. 7.2 common source inductance the source inductance plays the most important role in influencing the switching performances of a power mosfet, especially when high current levels need to be commutated. when dealing with source inductance, it is necessary to split it between an internal component (the source bond wire inside the mosfet package) and external components including the inductance wiring between the source pin and the common ground of the pcb. am10 8 07v1 v d s ?mi ss ing s tep ? a t t u rn-on d d u e to high p a r as itic l
mosfet critical parameters in high switching environments AN3994 38/53 doc id 022380 rev 1 since no optimization can be done over the internal component, particular care must be taken in controlling and reduci ng the external source induct ance as much as possible. the source inductance is involved in two different phenomena during the switching transient; the most visible one arises during phase ?2? of turn-on and phase ?3? of turn-off (see figure 8 and 10 ). if the turn-on event is considered, phase ?2? is the phase of drain current rising. the v gs voltage is between the v th and the plateau level v pl , as the c iss capacitor is being charged by the gate current ig. figure 45 shows the equivalent driving circuit referred to in this specific phase: figure 45. equivalent driving circuit of a mosfet at turn-on with parasitic source inductance the high di/dt during turn-on (positive rate of i d ) induces a voltage v ls across the source inductor (positive value, as shown in figure 45 ) whose value satisfies equation 27 : equation 27 this induced v ls causes a lack of gate current due to less available voltage across the total gate resistor causing a di/dt reduction and, as a negative consequence, a worsening i-v cross. the source inductance, on the other hand, acts as a negative feedback in the gate driving loop, as the reduced di/dt results in a smaller v ls , this reduced voltage across ls leads to an increase in di/dt. a balance is therefore established thanks to the source inductor, between the gate current and the drain current. as far as the turn-off (phase ?3?) is concerned, the l s acts in a similar way by inducing a voltage v ls over the source inductor which is negative if referred to figure 45 as the drain current is falling down. this volt age leads to a positiv e ig which has the unavoidable effect of slowing down the drain current. as long as the v ls across the inductor is considerably less than the gate source voltage value in the commutation time interval, the effect of l s can be neglected. !-v / v 5 *727 9 /v * 6 9 *0 dt ) i ( d l dt ) i i ( d l v d s gs d s ls =
AN3994 mosfet critical parameters in high switching environments doc id 022380 rev 1 39/53 on the contrary, when high drain currents/high i/dt are involved, the induced voltage v ls becomes large enough to significantly interfere with the gate bias. a second order effect related to the source inductance is that r gtot , l s , and c iss (at turn-on) are the rlc components of a series resonant circuit, as shown in figure 46 . figure 46. simplified equivalent series reso nant model of the driving circuit of a mosfet as far as the resonance aspect is conc erned, the phenomenon is due to the l s inductor and the mosfet input capacitor energy exchange (if turn-off is considered, the capacitor involved is the drain source c ds ). this results in the output current (gate current i g ) and voltage oscillatory spikes which can lead to unwanted turn-on if the v gs voltage reaches the threshold value. the q factor of the resonant circui t which is also related to the l s value and is responsible of the output signal time response, can be reduced by increasing the total gate resistor components along the driving loop (which comprises the external r g , the mosfet intrinsic r g and the driver output impedance). if especially small sizes are involved, a higher gate resistor causes under damped oscillations in the gate drive voltage waveforms but results in turn-on/tu rn-off time widening. on the other hand, if r g values need to be lowered to optimize the energy losses at turn-on and turn-off, the user must accept the possib ility of spurious gate driving waveforms. 7.3 minimizing common source inductance: layout optimization and kelvin source conn ection on stw77n65m5 the negative impact on turn-on and turn-off energy losses, due to the source inductance, can be minimized by taking particular care of the layout during the design phase: the gate driving loop should be as short as possible to minimize the total parasitic loop inductance and more precisely, the common source wiring between the commutation loop and the gate loop should be as short as possible (ideally zero) to minimize the slowing action of the ls on the drain current. this could be accomplished by placing the driving stage gnd directly connected to the source pin of the switch or very close to it, as shown in figure 47 . !-v 6 '- # iss ' 3 , s 2 'tot
mosfet critical parameters in high switching environments AN3994 40/53 doc id 022380 rev 1 figure 47. gate driving and main switchi ng loops for a mosfet in a boost-like topology a simple clamped inductive load circuit test was adopted to evaluate the differences between two layout configurations and their respec tive effect on the switch performance. it's important to remark that all layout options described in the following sections have been implemented on the same test circuit. all tests have been carried on the stw77n65m5 , as the advantage offered by the layout optimization and the 4-pin solution (which is described shortly) is as important as high current levels are involved. in the first layout configuration, the common source path between the main switching loop and the driving loop is a few cm long, while in the second layout configuration, the common source path has been shortened to the length of the source pin. in both cases, the drain parasitic loop inductance has been neglected thanks to a very short distance between the bus capacitors and the switch. the following curves show the e on and the e off energies of stw77n65m5 which were issued with the same r g , gate driving signal (0 v to 10 v), and v dd =400 v conditions. !-v $2 '!4%$2)6).',//0 #/--54!4)/.,//0 , $
AN3994 mosfet critical parameters in high switching environments doc id 022380 rev 1 41/53 figure 48. stw77 energy on difference between the standard layout and the optimized layout figure 49. stw77 energy off difference between the standard layout and the optimized layout !-v %?* )! 3witchingon 347.- 6666 2ohm optimizedcommonpath notoptimizedcommonpath $ $$ '3 ' on !-v 6zlwfklqjrii 67:10 rswlpl]hgfrpprqsdwk qrwrswlpl]hgfrpprqsdwk )! $ %?* 6666 2ohm $$ '3 ' off
mosfet critical parameters in high switching environments AN3994 42/53 doc id 022380 rev 1 figure 52. stw77n65m5 e off @ 20 a, 2.2 with optimized common path figure 50. stw77n65m5 e off @ 20 a, 2.2 with non-optimized common path figure 51. stw77n65m5 e off @ 20 a, 2.2 with non-optimized common path !-v 0ositive)causedbytheinduced voltageovertheparasitic,during thenegativedidt4heeffectisan undesiredturn onandthe% worsening pgg 3 ' !-v 0 /&&
AN3994 mosfet critical parameters in high switching environments doc id 022380 rev 1 43/53 figure 55. stw77n65m5 e off @ 40 a, 2.2 , 400 v with optimized common path figure 53. stw77n65m5 e off @ 40 a, 2.2 with non-optimized common path figure 54. stw77n65m5 e off @ 40 a, 2.2 with non-optimized common path
mosfet critical parameters in high switching environments AN3994 44/53 doc id 022380 rev 1 figure 56. stw77n65m5 e on @20 a, 2.2 with no n-optimized c o m m o n p a t h figure 57. stw77n65m5 e on @20 a, 2.2 with non-optimized common p a t h figure 58. stw77n65m5 e on @20 a, 2.2 w i t h o p t i m i z e d c o m m o n p a t h figure 59. stw77n65m5 e on @20 a, 2.2 w i t h o p t i m i z e d c o m m o n p a t h !-v )lackduetotheinduced voltageovertheparasitic ,duringthepositivedidt 3 (po
AN3994 mosfet critical parameters in high switching environments doc id 022380 rev 1 45/53 the impact of the parasitic inductance becomes heavier as the current increases, as clearly shown by the trend of e on and e off in figure 50 and 63 . the turn-on is impacted more by the parasitic ls rather than the e off , as the di/dt starts at the very beginning of the turn-on phase, just after the v gs has reached the threshold. in this situation the di/dt and the v gs are severely slowed down and the plateau region is greatly widened even if low r g values are used. so, as evident from figure 60 , the main contribution over the iv cross is provided by the di/dt portion. as for turn-off, the first part of the iv cross du ring the plateau region is not affected by the l s , and can be sped up by adopting a proper r g value. additionally, the voltage across the switch rises in the last portion of the plateau region, due to the particular output capacitance dependence with voltage; so, this first contribution on the total energy off is negligible and independent of l s . as voltage across the switch reaches the clamp value, the i d drops down: the ls acts during this phase, but its impact is not heavy, as clear from the waveforms in figure 54 . figure 60. stw77n65m5 e on @40 a, 2.2 with n o n - o p t i m i z e d c o m m o n p a t h figure 61. stw77n65m5 e on @40 a, 2.2 with n o n - o p t i m i z e d c o m m o n p a t h figure 62. stw77n65m5 e on @40 a, 2.2 w i t h o p t i m i z e d c o m m o n p a t h figure 63. stw77n65m5 e on @40 a, 2.2 w i t h o p t i m i z e d c o m m o n p a t h
mosfet critical parameters in high switching environments AN3994 46/53 doc id 022380 rev 1 figure 64. schematic of 4-pin solution the best way to minimize the inductance influence is to adopt the kelvin source connection (see figure 64 ); this solution dramatically cuts the common path between the drain current and the gate current as the kelvin pin is dire ctly referenced to the driving stage gnd. the result is that the energy losses are reduced and the rate of drain current during transients is sped up. figure 65 and 66 , showing the differences in terms of energy on and energy off between a standard 3-pin with an optimized layout and the 4-pin, refer to the same pcb circuit of the previous sets of experimental waveforms of figure 48 and 49 : this leads to the obvious conclusion that the 4-pin solution allows the user to speed up the sj mosfet with excellent results, not reachable by the 3-pin solution even if optimized in terms of layout configuration. figure 65. stw77n65m5 energy on difference between the optimized layout (3-pin) and 4-pin solution !-v gate pin drain pin driversource pin po wersource pin !-v 3witchingon 347.- slq slqrswlpl]hgod\rxw 6666 2ohm $$ '3 ' %?* )! $ on
AN3994 mosfet critical parameters in high switching environments doc id 022380 rev 1 47/53 figure 66. stw77n65m5 energy on difference between the optimized layout (3-pin) and 4-pin solution figure 67. stw77n65m5 energy off differen ce between the optimized layout (3-pin) and 4-pin solution !-v 3witchingoff 347.- slq slqrswlpl]hgod\rxw 6666 2ohm $$ '3 ' %?* )! $ on !-v 0 /&& ) 'off ) $ 6 $3
mosfet critical parameters in high switching environments AN3994 48/53 doc id 022380 rev 1 figure 68. stw77n65m5 e off @20 a, 2.2 , 400 v 4-pin solution figure 69. stw77n65m5 e on @20 a, 2.2 4 - p i n s o l u t i o n figure 70. stw77n65m5 e on @20 a, 2.2 4-pin solution !-v ) '/. ) $ 6 $3
AN3994 mosfet critical parameters in high switching environments doc id 022380 rev 1 49/53 7.4 minimizing common source in ductance impact at turn-off: negative v gmoff threshold voltage for the power mosfet has a negative temperature coefficient and this aspect must be carefully considered especially at turn-off, when parasitic inductances resonate with the outp ut mosfet capacitor and lead to oscillations in gate to source voltage waveforms. if threshold voltage is lo wered because of high operation temperature, the risk of unwanted turn-on significantly increases. in order to improve the mosfet immunity against noise, a negative v gm during turn-off is suggested. the negative bias at turn-off also counterbalances the induced voltage vls across the common source inductance (which is negative if referred to figure 73 ). if the negative v gmoff is properly chosen to avoid any gate oxide damages, it contributes to the reduction of the positive gate charge amount injected during the i d falling down and consequently to the reduction of the negative l s impact on energy losses. figure 73. basic driving stage of a power mosfet at turn-off with negative v gm figure 71. stw77n65m5 e on @40 a, 2.2 4 - p i n s o l u t i o n figure 72. stw77n65m5 e on @40 a, 2.2 4-pin solution !-v , s 2 'tot 6 ,s ' 3 6 '-off
mosfet critical parameters in high switching environments AN3994 50/53 doc id 022380 rev 1 figure 74 shows the stw77n65m5 turn-off at the test conditions below: v ds =400 v i d =52 a v gmoff =0 v r goff =4.7 figure 74. stw77n65m5 e off @52 a, 4.7 , 400 v, v gmoff =-5 v figure 75 shows the stw77n65m5 turn-off when the negative bias voltage is adopted under the same test conditions and the same layout configuration: v ds =400 v i d =52 a v gmoff =-5 v r goff =4.7 figure 75. stw77n65m5 e off @52 a, 4.7 , 400 v, v gmoff =-5 v by comparing the two turn-off waveforms, it's clear that negative bias contributes to the speeding-up of the drain current falling down and to drastically reduce the energy losses at turn-off. in this specific test, the energy off with negative v gm is about half of the standard zero gate bias. !-v ) '/&& ) $ 6 '3 6 $3
AN3994 mosfet critical parameters in high switching environments doc id 022380 rev 1 51/53 7.5 switching loop inductance the main switching loop inductance comprises several components along the power circuit, including the internal inductances of the mosfet and the diode packages, rather than the pcb interconnections. the voltage across ls during turn-off transient (phase of the negative di/dt) results in high voltage v ds overshoot which can exceed the bus voltage and lead to mosfet failure. additionally, the drain inductance resonates with the mosfet or diode capacitance, causing severe ringing over the voltage and current waveforms. the l d impact on the turn-on waveform has been analyzed in section 7.1 . it's not easy to control the parasitic component of the switching loop as it is commonly wider than the other paths. anyway, it is best to take care of it during the design phase in order to further improve the mosfet dynamic performances.
revision history AN3994 52/53 doc id 022380 rev 1 8 revision history table 4. document revision history date revision changes 02-dec-2011 1 initial release.
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