WO1998041664A1 - Tole d'acier biphase a haute resistance ayant d'excellentes proprietes de deformation dynamique et son procede de preparation - Google Patents

Tole d'acier biphase a haute resistance ayant d'excellentes proprietes de deformation dynamique et son procede de preparation Download PDF

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Publication number
WO1998041664A1
WO1998041664A1 PCT/JP1998/001101 JP9801101W WO9841664A1 WO 1998041664 A1 WO1998041664 A1 WO 1998041664A1 JP 9801101 W JP9801101 W JP 9801101W WO 9841664 A1 WO9841664 A1 WO 9841664A1
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Prior art keywords
steel sheet
strength
deformation
dual
temperature
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PCT/JP1998/001101
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English (en)
Japanese (ja)
Inventor
Akihiro Uenishi
Manabu Takahashi
Yukihisa Kuriyama
Yasuharu Sakuma
Osamu Kawano
Junichi Wakita
Hidesato Mabuchi
Original Assignee
Nippon Steel Corporation
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First worldwide family litigation filed litigation Critical https://patents.darts-ip.com/?family=27524972&utm_source=google_patent&utm_medium=platform_link&utm_campaign=public_patent_search&patent=WO1998041664(A1) "Global patent litigation dataset” by Darts-ip is licensed under a Creative Commons Attribution 4.0 International License.
Priority claimed from JP19029797A external-priority patent/JP3530347B2/ja
Priority claimed from JP22300897A external-priority patent/JP3936440B2/ja
Priority claimed from JP25893897A external-priority patent/JP3839928B2/ja
Application filed by Nippon Steel Corporation filed Critical Nippon Steel Corporation
Priority to CA002283924A priority Critical patent/CA2283924C/fr
Priority to EP98907247.5A priority patent/EP0969112B2/fr
Priority to AU63118/98A priority patent/AU717294B2/en
Publication of WO1998041664A1 publication Critical patent/WO1998041664A1/fr

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    • C—CHEMISTRY; METALLURGY
    • C22—METALLURGY; FERROUS OR NON-FERROUS ALLOYS; TREATMENT OF ALLOYS OR NON-FERROUS METALS
    • C22C—ALLOYS
    • C22C38/00—Ferrous alloys, e.g. steel alloys
    • C22C38/02—Ferrous alloys, e.g. steel alloys containing silicon
    • C—CHEMISTRY; METALLURGY
    • C22—METALLURGY; FERROUS OR NON-FERROUS ALLOYS; TREATMENT OF ALLOYS OR NON-FERROUS METALS
    • C22C—ALLOYS
    • C22C38/00—Ferrous alloys, e.g. steel alloys
    • C—CHEMISTRY; METALLURGY
    • C21—METALLURGY OF IRON
    • C21D—MODIFYING THE PHYSICAL STRUCTURE OF FERROUS METALS; GENERAL DEVICES FOR HEAT TREATMENT OF FERROUS OR NON-FERROUS METALS OR ALLOYS; MAKING METAL MALLEABLE, e.g. BY DECARBURISATION OR TEMPERING
    • C21D8/00—Modifying the physical properties by deformation combined with, or followed by, heat treatment
    • C21D8/02—Modifying the physical properties by deformation combined with, or followed by, heat treatment during manufacturing of plates or strips
    • C—CHEMISTRY; METALLURGY
    • C21—METALLURGY OF IRON
    • C21D—MODIFYING THE PHYSICAL STRUCTURE OF FERROUS METALS; GENERAL DEVICES FOR HEAT TREATMENT OF FERROUS OR NON-FERROUS METALS OR ALLOYS; MAKING METAL MALLEABLE, e.g. BY DECARBURISATION OR TEMPERING
    • C21D9/00—Heat treatment, e.g. annealing, hardening, quenching or tempering, adapted for particular articles; Furnaces therefor
    • C21D9/46—Heat treatment, e.g. annealing, hardening, quenching or tempering, adapted for particular articles; Furnaces therefor for sheet metals
    • C—CHEMISTRY; METALLURGY
    • C22—METALLURGY; FERROUS OR NON-FERROUS ALLOYS; TREATMENT OF ALLOYS OR NON-FERROUS METALS
    • C22C—ALLOYS
    • C22C38/00—Ferrous alloys, e.g. steel alloys
    • C22C38/002—Ferrous alloys, e.g. steel alloys containing In, Mg, or other elements not provided for in one single group C22C38/001 - C22C38/60
    • C—CHEMISTRY; METALLURGY
    • C22—METALLURGY; FERROUS OR NON-FERROUS ALLOYS; TREATMENT OF ALLOYS OR NON-FERROUS METALS
    • C22C—ALLOYS
    • C22C38/00—Ferrous alloys, e.g. steel alloys
    • C22C38/04—Ferrous alloys, e.g. steel alloys containing manganese
    • C—CHEMISTRY; METALLURGY
    • C22—METALLURGY; FERROUS OR NON-FERROUS ALLOYS; TREATMENT OF ALLOYS OR NON-FERROUS METALS
    • C22C—ALLOYS
    • C22C38/00—Ferrous alloys, e.g. steel alloys
    • C22C38/06—Ferrous alloys, e.g. steel alloys containing aluminium
    • C—CHEMISTRY; METALLURGY
    • C23—COATING METALLIC MATERIAL; COATING MATERIAL WITH METALLIC MATERIAL; CHEMICAL SURFACE TREATMENT; DIFFUSION TREATMENT OF METALLIC MATERIAL; COATING BY VACUUM EVAPORATION, BY SPUTTERING, BY ION IMPLANTATION OR BY CHEMICAL VAPOUR DEPOSITION, IN GENERAL; INHIBITING CORROSION OF METALLIC MATERIAL OR INCRUSTATION IN GENERAL
    • C23C—COATING METALLIC MATERIAL; COATING MATERIAL WITH METALLIC MATERIAL; SURFACE TREATMENT OF METALLIC MATERIAL BY DIFFUSION INTO THE SURFACE, BY CHEMICAL CONVERSION OR SUBSTITUTION; COATING BY VACUUM EVAPORATION, BY SPUTTERING, BY ION IMPLANTATION OR BY CHEMICAL VAPOUR DEPOSITION, IN GENERAL
    • C23C2/00—Hot-dipping or immersion processes for applying the coating material in the molten state without affecting the shape; Apparatus therefor
    • C23C2/02—Pretreatment of the material to be coated, e.g. for coating on selected surface areas
    • C—CHEMISTRY; METALLURGY
    • C23—COATING METALLIC MATERIAL; COATING MATERIAL WITH METALLIC MATERIAL; CHEMICAL SURFACE TREATMENT; DIFFUSION TREATMENT OF METALLIC MATERIAL; COATING BY VACUUM EVAPORATION, BY SPUTTERING, BY ION IMPLANTATION OR BY CHEMICAL VAPOUR DEPOSITION, IN GENERAL; INHIBITING CORROSION OF METALLIC MATERIAL OR INCRUSTATION IN GENERAL
    • C23C—COATING METALLIC MATERIAL; COATING MATERIAL WITH METALLIC MATERIAL; SURFACE TREATMENT OF METALLIC MATERIAL BY DIFFUSION INTO THE SURFACE, BY CHEMICAL CONVERSION OR SUBSTITUTION; COATING BY VACUUM EVAPORATION, BY SPUTTERING, BY ION IMPLANTATION OR BY CHEMICAL VAPOUR DEPOSITION, IN GENERAL
    • C23C2/00—Hot-dipping or immersion processes for applying the coating material in the molten state without affecting the shape; Apparatus therefor
    • C23C2/02—Pretreatment of the material to be coated, e.g. for coating on selected surface areas
    • C23C2/022—Pretreatment of the material to be coated, e.g. for coating on selected surface areas by heating
    • C23C2/0224—Two or more thermal pretreatments
    • C—CHEMISTRY; METALLURGY
    • C23—COATING METALLIC MATERIAL; COATING MATERIAL WITH METALLIC MATERIAL; CHEMICAL SURFACE TREATMENT; DIFFUSION TREATMENT OF METALLIC MATERIAL; COATING BY VACUUM EVAPORATION, BY SPUTTERING, BY ION IMPLANTATION OR BY CHEMICAL VAPOUR DEPOSITION, IN GENERAL; INHIBITING CORROSION OF METALLIC MATERIAL OR INCRUSTATION IN GENERAL
    • C23C—COATING METALLIC MATERIAL; COATING MATERIAL WITH METALLIC MATERIAL; SURFACE TREATMENT OF METALLIC MATERIAL BY DIFFUSION INTO THE SURFACE, BY CHEMICAL CONVERSION OR SUBSTITUTION; COATING BY VACUUM EVAPORATION, BY SPUTTERING, BY ION IMPLANTATION OR BY CHEMICAL VAPOUR DEPOSITION, IN GENERAL
    • C23C2/00—Hot-dipping or immersion processes for applying the coating material in the molten state without affecting the shape; Apparatus therefor
    • C23C2/02—Pretreatment of the material to be coated, e.g. for coating on selected surface areas
    • C23C2/024—Pretreatment of the material to be coated, e.g. for coating on selected surface areas by cleaning or etching
    • C—CHEMISTRY; METALLURGY
    • C21—METALLURGY OF IRON
    • C21D—MODIFYING THE PHYSICAL STRUCTURE OF FERROUS METALS; GENERAL DEVICES FOR HEAT TREATMENT OF FERROUS OR NON-FERROUS METALS OR ALLOYS; MAKING METAL MALLEABLE, e.g. BY DECARBURISATION OR TEMPERING
    • C21D2211/00—Microstructure comprising significant phases
    • C21D2211/005—Ferrite
    • C—CHEMISTRY; METALLURGY
    • C21—METALLURGY OF IRON
    • C21D—MODIFYING THE PHYSICAL STRUCTURE OF FERROUS METALS; GENERAL DEVICES FOR HEAT TREATMENT OF FERROUS OR NON-FERROUS METALS OR ALLOYS; MAKING METAL MALLEABLE, e.g. BY DECARBURISATION OR TEMPERING
    • C21D2211/00—Microstructure comprising significant phases
    • C21D2211/008—Martensite

Definitions

  • the present invention relates to a dual-phase high-strength steel sheet for automobiles having excellent dynamic deformation characteristics and excellent collision safety, which is intended to be mainly used for structural members of automobiles and reinforcing materials. It is about methods. Background art
  • high-strength steel has been expanding for the purpose of reducing vehicle body weight in the context of automobile fuel efficiency regulations, but recently, laws and regulations regarding collision safety assuming an automobile accident have been rapidly expanding and strengthening in Japan and overseas.
  • Expectations for high-strength steel are increasing. For example, in a frontal collision of a passenger car, if a material with high shock absorption performance is applied to a member called the front side member, the shock energy is absorbed by the crushing of this member, which affects the occupant. Shock can be reduced.
  • a collision safety member when forming a collision safety member, it has excellent shape freezing properties, excellent stretchability (tensile strength X total elongation ⁇ 18,800), and excellent elongation flangeability (hole expansion ratio ⁇ It is desired that the combination of 1.2) is satisfied, but it has not been found that there is a material that has both excellent collision safety and excellent formability. Disclosure of the invention
  • the present invention has been proposed to solve the above-described problems, and provides a dual-fused high-strength steel sheet for an automobile having excellent collision safety and excellent dynamic deformation characteristics, and a method for producing the same. is there.
  • the present invention relates to a high-strength steel sheet used for a molded automotive part such as a front side member and the like, which is selected based on appropriate characteristics and criteria for absorbing impact energy in a collision.
  • Another object of the present invention is to provide a dual-phase high-strength steel sheet for automobiles having excellent dynamic deformation characteristics that can surely contribute to ensuring safety and a method for producing the same.
  • the present invention provides a dual-fuse type vehicle having excellent dynamic deformation characteristics having excellent shape freezing properties, excellent overhanging properties, and excellent elongation flangeability suitable for forming a collision safety member. It provides high-strength steel sheets and methods for manufacturing them.
  • the present invention has been made to achieve the above object, and specific means thereof are as follows.
  • the main phase is flat and the second phase is 5% with the equivalent strain of the steel sheet.
  • the martensite is reduced to 3 to 50% by volume fraction.
  • This is a composite structure with other low-temperature-producing phases containing, and after applying a pre-deformation of more than 0% to 10% or less at equivalent strain, 5 X 10 " 4 to 5 X 10 — 3 (s — ')
  • the difference ( ⁇ ) between the shape strength s and the dynamic deformation strength ⁇ d when deformed in the strain rate range of 5 ⁇ 10 2 to 5 ⁇ 10 3 (s ′′ ′) after the pre-deformation is applied.
  • (3- ⁇ s) satisfies 6 OMPa or more, and a work hardening index at a strain of 5 to 10% satisfies 0.13 or more.
  • the main phase is ferrite and the second phase is 5% with the equivalent strain of the steel sheet.
  • the martensite is converted to a volume fraction of 3 to 50%. This is a composite structure with other low-temperature generation phases containing 5% after applying a predeformation of more than 0% to 10% or less at equivalent strain.
  • the average crystal grain size of the martensite satisfies 5 m or less and the average crystal grain size of the fly satisfies 10 m or less.
  • Dual-pipe high-strength steel sheet with excellent dynamic deformation characteristics ⁇ ⁇ ⁇ ⁇ In any of 1, 2, 3 or 2 above, tensile strength (MPa) X total elongation (%) ⁇ 18,000 and hole expansion ratio (d / do) ⁇ 1.2
  • MPa tensile strength
  • X total elongation (%) ⁇ 18,000
  • a dual-phase high-strength steel sheet with excellent dynamic deformation characteristics characterized by satisfying
  • the amount of plastic deformation (T) at the time of pre-deformation by either or both of the temper rolling and the tension leveler is expressed by the following formula:
  • a dual-phase high-strength steel sheet having excellent dynamic deformation characteristics characterized by satisfying the following requirements.
  • the dual-phase high-strength steel sheet having excellent dynamic deformation characteristics according to the present invention is characterized in that, in the above-mentioned 1 to 6, C: 0.02 to 0.25% by weight as a material component, 0.15 to 3.5% in total of one or more of Mn and Cr, 0.02 to 4.0 in total of one or more of Si, Al, P %, And if necessary, one or more of Ni, Cu and Mo in a total of 3.5% or less, and one or more of Nb, Ti and V in total 0.3% or less, one or more of Ca and REM, 0.05 to 0.01% for Ca, and 0.05 to 0.05 for REM %, With the balance being Fe as the main component.
  • the dual-phase high-strength steel sheet having excellent dynamic deformation characteristics according to the present invention further comprises B ⁇ 0.0I%, S ⁇ 0.01 N ⁇ 0.0 A dual-phase high-strength steel sheet with excellent dynamic deformation characteristics characterized by the addition of one or more of 2% or more as required.
  • ⁇ ⁇ ⁇ ⁇ As a method for producing a dual-phase high-strength hot-rolled steel sheet having excellent dynamic deformation characteristics in the present invention, a continuous forged slab is directly sent to a hot-rolling process as it is, or after being cooled once.
  • the metallurgical parameters A force The hot rolling that satisfies the formulas (1) and (2) is performed, and in the subsequent runtable The average cooling rate was set to 5 ° C / sec or more, and the relationship between the above-mentioned metal parameter: A and the winding temperature (CT) was (
  • a continuous production slab is directly sent to a hot-rolling process as it is produced.
  • hot-rolled, hot-rolled and rolled hot-rolled steel sheet is pickled, cold-rolled, and annealed in a continuous annealing process to obtain a final product, A c, ⁇
  • cooling is performed at a cooling rate of 5 ° C./second or more.
  • the cold-rolled steel sheet is heated to a temperature of A c, to A c 3 (T o), and annealed for more than 10 seconds within this temperature range.
  • FIG. 1 is a view showing the relationship between the absorbed energy (E ab) of the molded member and the material strength (S) at the time of collision in the present invention.
  • Fig. 2 Perspective view showing the molded member for measuring the shock absorption energy in Fig. 1.
  • Fig. 3 Diagram showing the relationship between the work hardening index of steel sheets and the amount of dynamic energy absorption.
  • Fig. 4 A graph showing the relationship between the yield strength of a steel sheet X work hardening index and the amount of dynamic energy absorption.
  • Fig. 5 Schematic view of the (hat model) used in the impact crush test method related to Figs.
  • Fig. 6 Sectional view of the test piece shape of Fig. 5.
  • Fig. 7 Schematic diagram of the impact crush test method related to Figs.
  • Fig. 8 Equivalent strain of 3 to 10% when deformed at a strain rate of 5 ⁇ 10 2 to 5 ⁇ 10 3 (1ZS), which is an index of the impact energy absorption capacity at the time of collision in the present invention.
  • the figure which shows the relationship between the average value of deformation stress dyn-TS and TS in the range.
  • Fig. 9 Shows the change in static-dynamic ratio due to temper rolling in the present invention example and the comparative example. Graph.
  • FIG. 10 is a view showing the relationship between ⁇ ⁇ ⁇ ⁇ ⁇ and metal parameter: A in the hot rolling process according to the present invention.
  • FIG. 11 is a view showing the relationship between the winding temperature and the metallurgical parameter: A in the hot rolling process according to the present invention.
  • FIG. 12 is a schematic view showing an annealing cycle of continuous annealing according to the present invention.
  • Shock absorbing members such as front side members of automobiles are manufactured by bending and pressing steel plates. Since the impact at the time of vehicle collision is applied to these formed members, it is necessary to have a high shock absorbing capacity in a state after pre-deformation corresponding to such forming.
  • attempts have been made to obtain a high-strength steel sheet having excellent shock absorption properties as a real member by simultaneously considering the increase in deformation stress due to forming and the increase in deformation stress due to increase in strain rate. That is not described above.
  • the present inventors have conducted various experiments and studies in order to achieve the above object, and as a result, as a high-strength steel sheet having excellent shock absorption characteristics in the above-formed real member, a dual phase steel plate (DP)
  • a steel sheet with a structure was optimal.
  • the steel sheet having this dual-phase structure is a composite structure with the ferrite phase, which plays a role in increasing the deformation resistance due to the increase in deformation speed, as the main phase, and the second phase including a hard martensite phase. It was found to be excellent in dynamic deformation characteristics.
  • the microstructure of the finally obtained steel sheet has a ferrite phase as a main phase and a hard martensite phase with a volumetric equivalent of the above steel sheet of 3% by volume after forming by 5%. It was found that the composite showed high dynamic deformation resistance when it had a composite structure with other low-temperature generation phases containing up to 50%.
  • the volume fraction of the hard martensite phase 3 to 50%, if the martensite phase is less than 3%, a high-strength steel sheet cannot be obtained, and the dynamic deformation strength cannot be increased. Since a high steel sheet cannot be obtained, the volume fraction of the martensite phase must be 3% or more.
  • the volume fraction of the ferrite phase which should be responsible for the increase in deformation resistance due to the increase in deformation speed, decreases, and the dynamic deformation strength becomes smaller than the static deformation strength. It has also been found that it is not possible to obtain a steel sheet excellent in quality and the formability is impaired, so that the volume fraction of the martensite phase must be 3 to 50%.
  • the present inventors found that the amount of pre-deformation corresponding to the forming process of a shock absorbing member such as a front side member was up to 2 parts depending on the part.
  • the force can reach 0% or more, and it is also found that the equivalent strain is mostly in the range of 0% to 10%, and by grasping the effect of pre-deformation in this range, We also found that it was possible to estimate the behavior after pre-deformation as a whole. Therefore, in the present invention, a deformation of 0% to 10% was selected as an equivalent strain as an amount of pre-deformation to be given to the member during processing.
  • FIG. 1 shows the relationship between the absorbed energy (E ab) of the formed member and the material strength (S) at the time of collision for each of the steel types in Table 5 in the examples described later.
  • the material strength S is the tensile strength (TS) from a normal tensile test.
  • the material absorption energy (E ab) is calculated by colliding a weight of 400 kg with a velocity of 15 m / s in the length direction (the direction of the arrow) of the molded member as shown in Fig. 2 and crushing it. Absorbed energy up to 100 mm.
  • the formed member shown in Fig. 2 is made by joining a steel plate with a thickness of 2.0 mm to the hat-shaped part 1 and a steel sheet 2 of the same thickness and the same steel type by spot welding.
  • the work hardening index of the steel specifically, 0.13 or more, preferably 0.16 or more.
  • the work hardening index and the work hardening index By controlling the work hardening index and the work hardening index to a specific range, it is possible to achieve excellent collision safety, and to improve the formability, effects such as incorporating the volume fraction and the particle size of the martensite in a specific range. There is.
  • Figure 3 shows the relationship between the dynamic energy absorption, which is an index of the collision safety of the member, and the work hardening index of the steel sheet, for the same yield strength class.
  • the collision safety (dynamic energy absorption) of the members is improved due to the increase in the work hardening index of the steel sheet, and the work hardening of the steel sheet with the same yield strength class is used as an index of the collision safety of the member. This indicates that the index is valid.
  • the yield strength X work hardening index can be used as an index of the collision safety of the member.
  • the work hardening index is represented by an n value of 5% to 10% in consideration of the fact that the member is subjected to distortion during molding. From the viewpoint of improving the dynamic energy absorption, the work hardening index is expressed as 5%. It is preferable that the work hardening index is less than 10% and the work hardening index is more than 10%.
  • Figure 7 shows a schematic diagram of the test method. In Fig.
  • the steel sheet used was 1.2 mm in thickness, and the composition of the steel sheet was C: 0.02 to 0.25% by weight, and the total of one or more of 1 ⁇ 1 and ⁇ r was 0.15%. To 3.5% by weight, the total amount of one or two of Si, Al, and P is from 0.02 to 4.0% by weight, and the balance is Fe.
  • FIG. 8 is an index of the impact energy absorbing ability at the time of collision according to the present invention, which is equivalent to 3 to 10% when deformed in a strain rate range of 5 ⁇ 10 2 to 5 ⁇ 10 3 (s- 1 ).
  • TS maximum stress
  • MPa maximum stress
  • the shock absorbing member such as the front side member has a hat-shaped cross-sectional shape
  • the present inventors have analyzed the deformation of such a member during high-speed collision crushing.
  • deformation is progressing up to a high strain of 40% or more at the maximum, 70% or more of the total absorbed energy is absorbed in the strain range of 10% or less in the high-speed stress-strain diagram. I found it. Therefore, the dynamic deformation resistance at the time of high-speed deformation of 10% or less was adopted as an index of the absorption capacity of the collision energy at high speed.
  • CT dyn are the static tensile strength of the steel sheet before pre-deformation and baking treatment is carried out (5 X 1 0 "4 ⁇ 5 X 1 0 - 3 ( s'), which generally increases with an increase in the maximum stress (TS: MPa) ⁇ in the static tensile test measured in the strain rate range of Increasing the tensile strength (which is synonymous with the static material strength) directly contributes to the improvement of the impact energy absorption capacity of the member. Deterioration of the formability makes it difficult to obtain the required member shape, therefore, it is desirable to use a steel plate with the same tensile strength: TS and a high CT dyn.
  • the dynamic deformation strength is usually expressed as a power of the static deformation strength. As the static deformation strength increases, the difference between the dynamic deformation strength and the static deformation strength decreases. It becomes bad. However, when considering the weight reduction by increasing the strength of the material, it is not expected that if the difference between the dynamic deformation strength and the static deformation strength becomes smaller, the improvement in the shock absorption capacity by replacing the material will not increase. It is difficult to achieve weight reduction.
  • the (d — CTS) value is (d — CTS) ⁇ 4.1 X CT S. ' 8 — It is preferable that the range satisfy s.
  • the martensite has a volume fraction of 3 to 50%, preferably 3 to 30%.
  • the average crystal grain size of the martensite is preferably 5 m or less, and the average crystal grain size of the ferrite is preferably 10 zm or less.
  • martensite is hard and contributes to the reduction of the yield ratio and the improvement of the work hardening index by generating mobile dislocations mainly in the surrounding ferrite. It is possible to disperse fine martensite, and the effect of improving its properties extends to the entire steel sheet.
  • the volume fraction of the martensite When the volume fraction of the martensite is less than 3%, the yield ratio is increased and the work hardening ability (the work hardening index ⁇ 0.130) when the molded member is subjected to collision deformation is increased. It is not possible to exert it, the deformation resistance (load) remains at a low level, and the deformation work becomes small, so that the dynamic energy absorption is low and the improvement in impact safety cannot be achieved.
  • the volume fraction of the martensite exceeds 50%, the yield ratio increases and the work hardening index decreases, and further, the tensile strength X total elongation and the hole expansion ratio deteriorate. From the viewpoint of moldability, it is preferable that the volume fraction of the martensite be 30% or less.
  • ferrite is contained in a volume fraction of preferably 50% or more, more preferably 70% or more, and its average crystal grain size (average equivalent circle diameter) is preferably 10% or more. It is preferred that the length be less than 2 m, more preferably less than 5 m, and that the martensite be adjacent to the ferrite. This not only promotes the fine dispersion of the martensite in the ground, but also works effectively so that the above-mentioned effect of improving the properties extends not only to the local influence but also to the entire steel sheet.
  • the remaining structure other than martensite-filled light may be one or a combination of two or more of perlite, bainite, residual iron, etc., but when hole-expanding properties are required Although it is preferable to mainly use bainite, it is preferable that a small amount (5% However, experiments have shown that this is effective.
  • the ratio of the particle size of the martensite to the ferrite be 0.6 or less and the hardness ratio be 1.5 or more.
  • the dual-phase high-strength steel sheet having excellent dynamic deformation characteristics used in the present invention has a C: 0.02 to 0.25% by weight as a material component, and a content of Mn and Cr. 0.15 to 3.5% in total of 1 or 2 or more, 0.02 to 4.0% in total of 1 or 2 or more of Si, A1, P
  • one or more of Ni, Cu, and Mo are 3.5% or less in total
  • one or more of Nb, Ti, and V are 0.30% or less in total
  • C a, REM one or more of them
  • C a is 0.0 0 0 5 to 0 .01%
  • the length is 0.05 to 0.05. %, With the balance being Fe.
  • B ⁇ 0.01% S ⁇ 0.01% and N ⁇ 0.02% dual phase type with excellent dynamic deformation characteristics It is a high strength steel plate.
  • C is an element that strongly affects the structure of the steel sheet, and when its content is low, it becomes difficult to obtain the desired amount and strength of the martensite phase. If the amount of addition increases, unnecessary precipitation of carbides is caused, which hinders an increase in deformation resistance due to an increase in strain rate, increases the strength too much, and further deteriorates formability and weldability. ⁇ 0.25% by weight.
  • Mn, Cr Since Mn and Cr act to stabilize austenite and secure martensite and are also strengthening elements, the lower additive amount is 0.15% by weight. On the other hand, excessive addition saturates the above effects and adversely affects ferrite transformation, etc., so the upper limit is 3.5% by weight.
  • S i, A l, P S i, A l are useful elements for forming martensite, and promote martensite formation by promoting ferrite formation and suppressing carbide formation. It has the effect of securing and has the effect of strengthening the solid solution and the effect of deoxidation. P, like Al and Si, also has the ability to promote martensite formation and strengthen solid solution.
  • the lower limit of the addition of Si + A1 + P needs to be 0.02% by weight or more.
  • the upper limit of the addition is set to 4.0% by weight or less.
  • the Si content is reduced to 0.1% by weight or less to avoid the Si scale, and conversely to 1.0% by weight or more. Therefore, it is desirable that the Si scale be generated over the entire surface to make it inconspicuous.
  • the P content should be 0.05% or less, preferably 0.02% or less. I do.
  • Ni, Cu, Mo These elements are austenite stabilizing elements as well as the force Mn that is added as needed, enhance the hardenability of steel, facilitate the formation of martensite, It is also an effective element for adjusting the strength. From the viewpoint of weldability and chemical conversion treatment, it can be used when there are restrictions on the amounts of C, S i, A 1, and M n, but the total amount of these elements added is 3.5% by weight. Exceeding this causes the ferrite phase, which is the parent phase, to be hardened, hinders the increase in deformation resistance due to the increase in strain rate, hardens the parent phase, and also increases the cost of steel sheets. 50% by weight or less.
  • Nb, Ti, V These elements are added as necessary, but form carbides, nitrides, and carbonitrides, and are effective elements for increasing the strength of steel sheets.
  • carbides, nitrides, and carbonitrides are formed in the ferrite phase, which is the parent phase, or in the grain boundaries. It precipitates and becomes a source of mobile dislocations during high-speed deformation, hindering an increase in deformation resistance due to an increase in strain rate.
  • the upper limit of the addition amount is set to 0.3% by weight.
  • B is an element that is effective for increasing the strength because it improves the hardenability of steel by suppressing the formation of frit, but the effect is saturated when the added amount exceeds 0.01% by weight. Therefore, the upper limit of the amount of B added is set to 0.01% by weight.
  • Ca is added in an amount of 0.0005% by weight or more in order to further improve the formability (particularly the hole expansion ratio) by controlling the shape (spheroidization) of sulfide-based inclusions.
  • the upper limit of the addition amount is set to 0.01% by weight from the viewpoint of saturation of the effect and adverse effects (deterioration of the hole expansion ratio) due to the increase of inclusions.
  • the addition amount of REM is set to 0.005 to 0.05% by weight.
  • S should be 0.01% by weight or less, preferably 0.03% by weight or less, from the viewpoint of deterioration of formability (particularly hole expansion ratio) by sulfide-based inclusions and deterioration of spot weldability. .
  • the pre-deformation may be a forming process for forming a member, or may be a temper rolling applied to a steel sheet material before the forming process or a process performed by a tension leveler.
  • one or both of the temper rolling and the tension leveler can be used. That is, any of the means of the temper rolling, the tension leveler, the temper rolling and the tension leveler may be used.
  • a forming process may be added to the steel sheet material processed by the temper rolling or the tension leveler.
  • the amount of plastic deformation ( ⁇ ) is the yield strength: YS (0) and the static deformation after the pre-deformation of 5% at the equivalent strain or after further baking hardening treatment ( ⁇ ⁇ treatment). It was also found that the maximum strength in the tensile test was determined according to the ratio to TS ′ (5), ⁇ S (0) / TS ′ (5).
  • YS (0) ZT S ′ (5) is an index indicating the sum of the initial dislocation density and the dislocation density introduced by the 5% deformation, and the amount of solid-solution elements. It can be said that the smaller the value of S ′ (5), the higher the initial dislocation density and the more solid solution elements. Therefore, YS (0) / TS '(5) is set to 0.7 or less, and the following equation:
  • the upper limit of T is determined from the viewpoint of formability such as impact absorption capacity and bendability.
  • the as-fabricated product is directly sent to a hot rolling step, or is cooled once and then heated again, and then hot-rolled.
  • a hot rolling step in addition to normal continuous forming, thin-wall continuous forming and hot-rolling continuous forming technology (end rolling) can be applied, but the volume fraction of the light is reduced, and Considering the coarsening of the average crystal grain size of the structure, it is preferable that the slab ( ⁇ ) thickness (initial slab thickness) on the hot-rolled side of the finish be 25 mm or more.
  • the thickness is less than 25 mm, the space factor of the steel sheet decreases and the average equivalent circle diameter of the microstructure of the steel sheet becomes coarse, and it is disadvantageous to obtain a desired martensite.
  • the final pass rolling speed was 500 mpm or more due to the above problem.
  • hot rolling is performed at 600 mpm or more. If it is less than 50 O mpm, a decrease in the space factor of the light and an increase in the average equivalent circle diameter of the microstructure of the steel sheet occur, and it is disadvantageous to obtain a desired martensite.
  • the average cooling rate of hot run staples should be 5 ° C Z seconds or more. If it is less than 5 ° C Z seconds, it is difficult to obtain a desired martensite.
  • the winding temperature shall be 350 ° C or less. Above 350 ° C, it is difficult to obtain the desired martensite.
  • the finishing temperature in the hot rolling process there is a correlation between the finishing temperature in the hot rolling process, the finishing inlet temperature and the winding temperature. That is, as shown in FIGS. 10 and 11, there are specific conditions uniquely determined between the finishing temperature, the finishing inlet temperature, and the winding temperature.
  • the finishing temperature of hot rolling is in the temperature range of Ar 3 — 50 ° C to Ar 3 + 120 ° C
  • the metallurgical parameter: A is strong, and the equations (1) and (2) are Hot rolling is performed to satisfy the condition.
  • the above-mentioned meta-parameter: A can be expressed as follows.
  • Thickness of the final pass entrance side h 2 Thickness of the final pass exit side r: (hi-h) / h, R: Roll diameter
  • Finishing temperature finish final pass outlet temperature
  • finishing inlet temperature finish final pass outlet temperature
  • a r 90 1-32 5 C% + 33 S i%-92 M n eq Then, set the average cooling rate in the run-out table to 5 ° C / sec or more, and furthermore, One: It is preferable to wind under the condition that the relationship between A and the winding temperature (CT) satisfies the expression (3).
  • the winding temperature does not satisfy the relationship of the formula (3), there is an adverse effect on securing the amount of martensite. Even when a residual 7 is obtained, the residual resistance becomes excessively stable, the desired martensite during the deformation cannot be obtained, and the dynamic deformation resistance dyn, 5 to 10% work hardening Deterioration of performance.
  • the limit of the winding temperature is relaxed by increasing 10 gA.
  • the cold-rolled steel sheet according to the present invention is subjected to cold rolling and annealing of the steel sheet that has undergone each step of hot rolling and winding.
  • continuous annealing having an annealing cycle as shown in Fig. 12 is optimal.
  • a c, ⁇ A c 3 It is necessary to hold for 10 seconds or more in the temperature range. Since A c, the Osutenai I below does not generate, then it is impossible to obtain martensite, since the single phase structure of coarse austenite Bok in A c 3 greater, then the desired Marte Nsai Bok of occupying Ratio and its average particle size cannot be obtained.
  • the upper limit of the staying time is preferably 200 seconds or less from the viewpoint of avoiding lengthening of equipment and coarsening of microstructure.
  • the average cooling rate must be 5 ° C / sec or more. If it is less than 5 ° C / sec, the desired martensite space factor cannot be obtained.
  • the upper limit is not particularly set, but is preferably 300 ° C./sec from the viewpoint of temperature controllability during cooling.
  • the steel sheet after cold rolling is heated to a temperature To of A c, to A c 3 , and the cooling conditions are as follows. Cool at the primary cooling rate of 1 to 10 ° CZ seconds to the secondary cooling start temperature Tq in the range of 550 to T0, and then at the secondary cooling rate of 10 to 200 ° C / sec. Temperature determined by steel material composition and annealing temperature T 0: This is a method of cooling to the secondary cooling end temperature Te below T em. This is due to the quenching end point temperature T e in the continuous annealing cycle shown in Fig. 12.
  • T 1 is a temperature calculated by the concentration of a solid solution element other than C
  • T 2 is a temperature determined by A c, and A c 3 determined by the composition of the steel sheet, and a TQ determined by the annealing temperature T o. This is the temperature calculated from the C concentration in the residual austenite.
  • C eq * is the carbon equivalent in the austenite remaining at the annealing temperature To. Therefore, T 1 is
  • T 1 5 6 1 — 3 3 X ⁇ M n% + (N i + C r + C u + M o) / 2 ⁇ ,
  • a c, 7 2 3-0.7 X M n%-1 6.9 x N i% + 2 9.1 x S i% + 1 6.9 x C r%, and
  • a c 3 9 1 0-2 0 3 x (C%) , 2-1 5.2 x N i% + 4
  • T 2 4 7 4 x (A c-A c,) x C / (T o-A c.),
  • the microstructure of the steel sheet has a main phase of ferrite, and a volumetric fraction of 3% after forming with 5% with equivalent strain. It is a composite structure with other low-temperature generation phases containing 50% martensite, and after giving a predeformation of more than 0% and 10% or less with equivalent strain, 5X10 to 5X10 — Quasi-static deformation strength ( ⁇ s) when deformed within the strain rate range of 3 (1 / s) and 5 X 10 2 to 5 X 10 3 (1 / s) ) With the dynamic deformation strength (CT d) measured in the strain rate range (d – CTS) of 60 MPa or more, and a work hardening index of 0.1% at a strain of 5 to 10%.
  • CT d dynamic deformation strength
  • the steel sheet according to the present invention can be subjected to annealing, temper rolling, electric plating, etc. to obtain a target product.
  • the 26 types (steel numbers 1-26) shown in Table 1 were heated to 150-125 ° C and hot rolled, cooled, and wound under the manufacturing conditions shown in Table 2.
  • Table 3 the steel sheet satisfying the component conditions and the production conditions according to the present invention has a dual-phase structure containing a martensite volume fraction of 3% or more and 50% or less.
  • the mechanical properties of the steel sheet are such that the work hardening index at a strain of 5 to 10% is 0.13 or more, CT d — CT S force is 6 OMPa or more, ⁇ dy ⁇ ⁇ 0.76 It is clear that it has excellent impact resistance of 6 x TS + 250 and also has both formability and weldability.
  • the 22 types (steel numbers 27-48) shown in Table 5 were heated to 105-125 ° C, hot-rolled, cooled, rolled up, and pickled.
  • Cold rolled steel sheets were produced by cold rolling under the conditions shown in Table 6. After that, the temperatures of A c, A c 3 were determined from the components of each steel, and heating, cooling, and holding were performed under the annealing conditions shown in Table 6, and then cooled to room temperature.
  • the steel sheet satisfying the component conditions and the production conditions according to the present invention has a dual-phase structure containing 3% to 50% by martensite volume fraction as shown in Table 7, As shown in Table 8, the mechanical properties of the rolled steel sheet are such that the work hardening index at a strain of 5 to 10% is 0.13 or more, (7 d — ⁇ s force is more than 60 MPa, and dyn ⁇ It is clear that it has excellent impact resistance of 0.766 XTS + 250 and also has both formability and weldability.
  • Dynamic tension (strain rate 0.000 ⁇ ) Pre-deformation and BH treatment Pre-deformation ⁇ Static after BH treatment.
  • Dynamic tension (strain rate 100 plastic deformation Steel No. TS YS T. ⁇ 5-103 ⁇ 4
  • Pre-deformation form-equivalent strain BH 5XWH t] ⁇ YS * 2 ⁇ sad ⁇ ⁇ - as cr dyn
  • WH indicates the rise S of YS by giving 5X pre-deformation with the equivalent strain in the table.
  • AYS gives the pre-deformation shown in the table and indicates the amount of increase in YS when heat treatment equivalent to paint baking is performed at 170 ° C for 20 minutes.
  • the microstructure was evaluated by the following method.
  • the characteristic evaluation was performed by the following method.
  • Tensile tests were conducted using JIS No. 5 (gauge length 50 mm, parallel part width 25 mm) at a strain rate of 0.001 Zs.
  • Tensile strength (TS), yield strength (YS), total elongation ( T. El) and work hardening index (n value of strain 1% to 5%) were calculated, and YSX work hardening index, TSX T. E1 was calculated.
  • Stretch flangeability is obtained by pushing a 20-nun punched hole out of a burr-free surface with a 30-degree circular cone punch, and when the crack penetrates the plate thickness (d) and initial hole diameter (d) , 20 mm) and the spot weldability was found to be 0.9 times the current generated by dust with an electrode having a tip diameter 5 times the square root of the steel sheet thickness. If so-called peel rupture occurs when the spot welding test piece joined by
  • the present invention makes it possible to provide high-strength hot-rolled steel sheets and cold-rolled steel sheets for automobiles, which have both unprecedented excellent collision safety and formability, at low cost and stably. As a result, the uses and conditions of use of high-strength steel sheets will be greatly expanded.

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Abstract

L'invention se rapporte à une tôle d'acier biphasé à haute résistance pour automobiles, qui présente d'excellentes propriétés de résistance en cas de collision et de déformation dynamique et qui est utilisée principalement pour les éléments structurels et les renforts d'automobiles, ainsi qu'à un procédé de préparation de ladite tôle. La tôle d'acier se caractérise en ce que sa microstructure, lorsqu'elle à l'état fini, est une texture composite comprenant une phase principale de ferrite et une autre phase secondaire formée à basse température, contenant de 3 à 50 % fractions de volume de martensite après le formage à 5 % de ladite tôle, en ce que la différence entre la résistance à la déformation quasi statique σs en cas de déformation dans la plage de contrainte de 5 x 10-4 à 5 x 10-3 (s-1), après l'application d'une prédéformation de plus de 0 à au plus 10 % en termes de contrainte correspondante, et la résistance à la déformation dynamique σd, en cas de déformation dans la plage de contrainte de 5 x 102 à 5 x 103 (s-1), après l'application de la prédéformation, c'est-à-dire σd-σs, n'est pas inférieure à 60 MPa, et en ce que l'indice d'écrouissage avec une contrainte de 5 à 10 % n'est pas inférieur à 0,13.
PCT/JP1998/001101 1997-03-17 1998-03-16 Tole d'acier biphase a haute resistance ayant d'excellentes proprietes de deformation dynamique et son procede de preparation WO1998041664A1 (fr)

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CA002283924A CA2283924C (fr) 1997-03-17 1998-03-16 Tole d'acier biphase a haute resistance ayant d'excellentes proprietes absorbant l'energie d'un impact et procede de preparation de la tole d'acier biphase
EP98907247.5A EP0969112B2 (fr) 1997-03-17 1998-03-16 Procede de preparation des toles d'acier biphasees a haute resistance mécanique et a haute capacité d'absorption d'energie de chock
AU63118/98A AU717294B2 (en) 1997-03-17 1998-03-16 Dual-phase high-strength steel sheet having excellent dynamic deformation properties and process for preparing the same

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JP8243497 1997-03-17
JP9/82434 1997-03-17
JP9/190299 1997-07-15
JP19029797A JP3530347B2 (ja) 1997-07-15 1997-07-15 動的変形特性に優れた高強度鋼板の選定方法
JP9/190297 1997-07-15
JP19029997 1997-07-15
JP22300897A JP3936440B2 (ja) 1997-08-06 1997-08-06 耐衝突安全性と成形性に優れた自動車用高強度鋼板とその製造方法
JP9/223008 1997-08-06
JP25893897A JP3839928B2 (ja) 1997-07-15 1997-09-24 動的変形特性に優れたデュアルフェーズ型高強度鋼板
JP9/258938 1997-09-24

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EP1001041A1 (fr) * 1998-11-10 2000-05-17 Kawasaki Steel Corporation Tôle d'acier laminé à chaud ayant une structure granulaire ultrafine et procédé de sa production
EP1052301A1 (fr) * 1998-11-30 2000-11-15 Nippon Steel Corporation Acier ferritique presentant une excellente dependance dans la vitesse de deformation, et automobile utilisant ledit acier ferritique
EP1052301A4 (fr) * 1998-11-30 2002-03-13 Nippon Steel Corp Acier ferritique presentant une excellente dependance dans la vitesse de deformation, et automobile utilisant ledit acier ferritique
US6432228B1 (en) 1998-11-30 2002-08-13 Nippon Steel Corporation Ferritic steel sheet excellent at strain rate sensitivity of the flow stress, and automobile utilizing it
WO2001009396A1 (fr) * 1999-07-31 2001-02-08 Thyssen Krupp Stahl Ag Feuille ou tole d'acier tres resistante et procede de fabrication de ladite feuille ou tole
US6743307B1 (en) 1999-07-31 2004-06-01 Thyssen Krupp Stahl Ag High resistance steel band or sheet and method for the production thereof
KR100796819B1 (ko) * 1999-07-31 2008-01-22 티센크루프 스틸 악티엔게젤샤프트 고강도 강 스트립 또는 강 시트 및 그의 제조방법
CZ299072B6 (cs) * 1999-07-31 2008-04-16 Thyssen Krupp Stahl Ag Ocelový pás nebo plech se zvýšenou pevností a zpusob jeho výroby

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AU6311898A (en) 1998-10-12
AU717294B2 (en) 2000-03-23
KR100334949B1 (ko) 2002-05-04
CA2283924C (fr) 2006-11-28
EP2314729B1 (fr) 2012-02-08
KR20000076372A (ko) 2000-12-26
EP0969112B2 (fr) 2017-03-08
EP0969112A1 (fr) 2000-01-05
EP0969112A4 (fr) 2003-05-21
EP2314729B2 (fr) 2017-03-08
CN1251140A (zh) 2000-04-19
CA2283924A1 (fr) 1998-09-24
TW426742B (en) 2001-03-21
CN1080321C (zh) 2002-03-06
EP0969112B1 (fr) 2011-08-17
EP2314729A1 (fr) 2011-04-27

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