US20240026479A1 - Hot press-formed member having excellent crack propagation resistance and ductility, and method for producing same - Google Patents
Hot press-formed member having excellent crack propagation resistance and ductility, and method for producing same Download PDFInfo
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- US20240026479A1 US20240026479A1 US18/375,764 US202318375764A US2024026479A1 US 20240026479 A1 US20240026479 A1 US 20240026479A1 US 202318375764 A US202318375764 A US 202318375764A US 2024026479 A1 US2024026479 A1 US 2024026479A1
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- hot press
- formed member
- steel sheet
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- 238000004519 manufacturing process Methods 0.000 title description 18
- 229910000831 Steel Inorganic materials 0.000 claims abstract description 82
- 239000010959 steel Substances 0.000 claims abstract description 82
- 239000011572 manganese Substances 0.000 claims abstract description 54
- 229910001566 austenite Inorganic materials 0.000 claims abstract description 45
- 238000007747 plating Methods 0.000 claims abstract description 42
- 230000000717 retained effect Effects 0.000 claims abstract description 31
- 229910052725 zinc Inorganic materials 0.000 claims abstract description 23
- XEEYBQQBJWHFJM-UHFFFAOYSA-N Iron Chemical compound [Fe] XEEYBQQBJWHFJM-UHFFFAOYSA-N 0.000 claims abstract description 21
- PWHULOQIROXLJO-UHFFFAOYSA-N Manganese Chemical compound [Mn] PWHULOQIROXLJO-UHFFFAOYSA-N 0.000 claims abstract description 20
- 229910052748 manganese Inorganic materials 0.000 claims abstract description 20
- IJGRMHOSHXDMSA-UHFFFAOYSA-N Atomic nitrogen Chemical compound N#N IJGRMHOSHXDMSA-UHFFFAOYSA-N 0.000 claims abstract description 16
- 229910001297 Zn alloy Inorganic materials 0.000 claims abstract description 13
- OKTJSMMVPCPJKN-UHFFFAOYSA-N Carbon Chemical compound [C] OKTJSMMVPCPJKN-UHFFFAOYSA-N 0.000 claims abstract description 11
- XUIMIQQOPSSXEZ-UHFFFAOYSA-N Silicon Chemical compound [Si] XUIMIQQOPSSXEZ-UHFFFAOYSA-N 0.000 claims abstract description 11
- 229910052782 aluminium Inorganic materials 0.000 claims abstract description 11
- 229910052799 carbon Inorganic materials 0.000 claims abstract description 11
- 229910052710 silicon Inorganic materials 0.000 claims abstract description 11
- 239000010703 silicon Substances 0.000 claims abstract description 11
- 239000012535 impurity Substances 0.000 claims abstract description 10
- 229910052717 sulfur Inorganic materials 0.000 claims abstract description 10
- NINIDFKCEFEMDL-UHFFFAOYSA-N Sulfur Chemical compound [S] NINIDFKCEFEMDL-UHFFFAOYSA-N 0.000 claims abstract description 9
- XAGFODPZIPBFFR-UHFFFAOYSA-N aluminium Chemical compound [Al] XAGFODPZIPBFFR-UHFFFAOYSA-N 0.000 claims abstract description 9
- 229910052698 phosphorus Inorganic materials 0.000 claims abstract description 9
- 239000011593 sulfur Substances 0.000 claims abstract description 9
- OAICVXFJPJFONN-UHFFFAOYSA-N Phosphorus Chemical compound [P] OAICVXFJPJFONN-UHFFFAOYSA-N 0.000 claims abstract description 8
- 229910052757 nitrogen Inorganic materials 0.000 claims abstract description 8
- 239000011574 phosphorus Substances 0.000 claims abstract description 8
- PXHVJJICTQNCMI-UHFFFAOYSA-N nickel Substances [Ni] PXHVJJICTQNCMI-UHFFFAOYSA-N 0.000 claims description 22
- 239000010936 titanium Substances 0.000 claims description 16
- 239000010949 copper Substances 0.000 claims description 15
- 229910000734 martensite Inorganic materials 0.000 claims description 14
- 239000011651 chromium Substances 0.000 claims description 12
- 239000010955 niobium Substances 0.000 claims description 12
- 229910052742 iron Inorganic materials 0.000 claims description 9
- ZOXJGFHDIHLPTG-UHFFFAOYSA-N Boron Chemical compound [B] ZOXJGFHDIHLPTG-UHFFFAOYSA-N 0.000 claims description 8
- 229910001563 bainite Inorganic materials 0.000 claims description 8
- 229910052796 boron Inorganic materials 0.000 claims description 8
- 229910052759 nickel Inorganic materials 0.000 claims description 8
- RYGMFSIKBFXOCR-UHFFFAOYSA-N Copper Chemical compound [Cu] RYGMFSIKBFXOCR-UHFFFAOYSA-N 0.000 claims description 7
- 229910052802 copper Inorganic materials 0.000 claims description 7
- VYZAMTAEIAYCRO-UHFFFAOYSA-N Chromium Chemical compound [Cr] VYZAMTAEIAYCRO-UHFFFAOYSA-N 0.000 claims description 6
- ZOKXTWBITQBERF-UHFFFAOYSA-N Molybdenum Chemical compound [Mo] ZOKXTWBITQBERF-UHFFFAOYSA-N 0.000 claims description 6
- RTAQQCXQSZGOHL-UHFFFAOYSA-N Titanium Chemical compound [Ti] RTAQQCXQSZGOHL-UHFFFAOYSA-N 0.000 claims description 6
- 229910052804 chromium Inorganic materials 0.000 claims description 6
- 229910052750 molybdenum Inorganic materials 0.000 claims description 6
- 239000011733 molybdenum Substances 0.000 claims description 6
- 229910052758 niobium Inorganic materials 0.000 claims description 6
- GUCVJGMIXFAOAE-UHFFFAOYSA-N niobium atom Chemical compound [Nb] GUCVJGMIXFAOAE-UHFFFAOYSA-N 0.000 claims description 6
- 229910052719 titanium Inorganic materials 0.000 claims description 6
- LEONUFNNVUYDNQ-UHFFFAOYSA-N vanadium atom Chemical compound [V] LEONUFNNVUYDNQ-UHFFFAOYSA-N 0.000 claims description 6
- 230000000149 penetrating effect Effects 0.000 claims description 5
- 239000011248 coating agent Substances 0.000 claims description 2
- 238000000576 coating method Methods 0.000 claims description 2
- 229910052751 metal Inorganic materials 0.000 claims description 2
- 239000002184 metal Substances 0.000 claims description 2
- 239000011701 zinc Substances 0.000 abstract description 39
- 239000010410 layer Substances 0.000 abstract description 29
- HCHKCACWOHOZIP-UHFFFAOYSA-N Zinc Chemical compound [Zn] HCHKCACWOHOZIP-UHFFFAOYSA-N 0.000 abstract description 21
- 239000002344 surface layer Substances 0.000 abstract description 4
- 238000010438 heat treatment Methods 0.000 description 34
- 238000001816 cooling Methods 0.000 description 30
- 230000000694 effects Effects 0.000 description 18
- 229910045601 alloy Inorganic materials 0.000 description 16
- 239000000956 alloy Substances 0.000 description 16
- 238000000034 method Methods 0.000 description 16
- 230000000052 comparative effect Effects 0.000 description 14
- 239000000463 material Substances 0.000 description 13
- 239000000203 mixture Substances 0.000 description 13
- 238000005496 tempering Methods 0.000 description 11
- 239000010960 cold rolled steel Substances 0.000 description 10
- 230000015572 biosynthetic process Effects 0.000 description 8
- 238000005097 cold rolling Methods 0.000 description 7
- 230000001965 increasing effect Effects 0.000 description 7
- 238000000137 annealing Methods 0.000 description 6
- 238000005244 galvannealing Methods 0.000 description 6
- 238000005098 hot rolling Methods 0.000 description 5
- 230000009466 transformation Effects 0.000 description 5
- 229910000859 α-Fe Inorganic materials 0.000 description 5
- 238000005260 corrosion Methods 0.000 description 4
- 230000007797 corrosion Effects 0.000 description 4
- 238000005554 pickling Methods 0.000 description 3
- 238000009864 tensile test Methods 0.000 description 3
- 238000012360 testing method Methods 0.000 description 3
- 235000014692 zinc oxide Nutrition 0.000 description 3
- RNWHGQJWIACOKP-UHFFFAOYSA-N zinc;oxygen(2-) Chemical class [O-2].[Zn+2] RNWHGQJWIACOKP-UHFFFAOYSA-N 0.000 description 3
- KRHYYFGTRYWZRS-UHFFFAOYSA-N Fluorane Chemical compound F KRHYYFGTRYWZRS-UHFFFAOYSA-N 0.000 description 2
- 238000002441 X-ray diffraction Methods 0.000 description 2
- 238000004458 analytical method Methods 0.000 description 2
- QVGXLLKOCUKJST-UHFFFAOYSA-N atomic oxygen Chemical compound [O] QVGXLLKOCUKJST-UHFFFAOYSA-N 0.000 description 2
- 230000015556 catabolic process Effects 0.000 description 2
- 230000003749 cleanliness Effects 0.000 description 2
- 238000006731 degradation reaction Methods 0.000 description 2
- 230000000593 degrading effect Effects 0.000 description 2
- 239000011777 magnesium Substances 0.000 description 2
- AMWRITDGCCNYAT-UHFFFAOYSA-L manganese oxide Inorganic materials [Mn].O[Mn]=O.O[Mn]=O AMWRITDGCCNYAT-UHFFFAOYSA-L 0.000 description 2
- PPNAOCWZXJOHFK-UHFFFAOYSA-N manganese(2+);oxygen(2-) Chemical class [O-2].[Mn+2] PPNAOCWZXJOHFK-UHFFFAOYSA-N 0.000 description 2
- 230000003287 optical effect Effects 0.000 description 2
- 230000003647 oxidation Effects 0.000 description 2
- 238000007254 oxidation reaction Methods 0.000 description 2
- 229910052760 oxygen Inorganic materials 0.000 description 2
- 239000001301 oxygen Substances 0.000 description 2
- 239000002244 precipitate Substances 0.000 description 2
- 239000012779 reinforcing material Substances 0.000 description 2
- 238000009628 steelmaking Methods 0.000 description 2
- 238000005728 strengthening Methods 0.000 description 2
- 229910018084 Al-Fe Inorganic materials 0.000 description 1
- 229910018192 Al—Fe Inorganic materials 0.000 description 1
- 229910001021 Ferroalloy Inorganic materials 0.000 description 1
- 229910000914 Mn alloy Inorganic materials 0.000 description 1
- 229910000611 Zinc aluminium Inorganic materials 0.000 description 1
- HXFVOUUOTHJFPX-UHFFFAOYSA-N alumane;zinc Chemical compound [AlH3].[Zn] HXFVOUUOTHJFPX-UHFFFAOYSA-N 0.000 description 1
- 238000005452 bending Methods 0.000 description 1
- 238000009749 continuous casting Methods 0.000 description 1
- 238000007796 conventional method Methods 0.000 description 1
- 238000005336 cracking Methods 0.000 description 1
- 238000005530 etching Methods 0.000 description 1
- 239000000446 fuel Substances 0.000 description 1
- 238000010191 image analysis Methods 0.000 description 1
- 230000001939 inductive effect Effects 0.000 description 1
- 229910052749 magnesium Inorganic materials 0.000 description 1
- 150000001247 metal acetylides Chemical class 0.000 description 1
- 238000001556 precipitation Methods 0.000 description 1
- 239000002994 raw material Substances 0.000 description 1
- 238000005096 rolling process Methods 0.000 description 1
- 238000010583 slow cooling Methods 0.000 description 1
- 239000006104 solid solution Substances 0.000 description 1
- 239000000243 solution Substances 0.000 description 1
- 230000000087 stabilizing effect Effects 0.000 description 1
- -1 zinc-aluminum-manganese Chemical compound 0.000 description 1
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- C21D8/02—Modifying the physical properties by deformation combined with, or followed by, heat treatment during manufacturing of plates or strips
- C21D8/0221—Modifying the physical properties by deformation combined with, or followed by, heat treatment during manufacturing of plates or strips characterised by the working steps
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- C21D2211/002—Bainite
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- 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 disclosure relates to a hot press-formed member suitable for use as an automotive material, and more specifically, to a hot press-formed member having excellent crack propagation resistance and ductility, and to a method for producing the same.
- hot press-formed members have been widely used as automotive structural members for purposes such as reducing the weight of a vehicle and improving the fuel efficiency of a vehicle, and a great deal of research has been conducted for such purposes.
- Patent Document 1 may provide a member having an ultra-high strength in the range of 1,500 MPa or greater in tensile strength, by hot press forming and rapid cooling an aluminum-plated steel sheet after heating the same to 850° C. or higher.
- a steel sheet having excellent corrosion resistance may be provided due to the formation of an Al—Fe alloy layer.
- the main phase of a coated steel sheet is formed by aluminum, so it may be difficult to exploit the sacrificial effects of aluminum, and ductility cannot be improved.
- Patent Document 2 discloses a technique to effectively achieve the sacrificial effects of a hot press-formed member, the technique characterized in that after a Zn-plated steel material is heated at 880-980° C. for 6-15 minutes, a buffer layer is formed at boundaries between a base steel sheet and a plating layer.
- the hot press-formed members For hot press-formed members to be suitable for use as impact-resistant members of vehicles, the hot press-formed members not only require ultra-high strength, but also need to have improved corrosion resistance and crack propagation resistance, as well as fatigue properties and crashworthiness, and therefore, it is necessary to develop a hot press-formed member that satisfies the aforementioned properties.
- An aspect of the present disclosure is to provide a hot press-formed member having excellent crack propagation resistance and ductility, which may be suitably used for automotive structural members or reinforcing materials that require corrosion resistance and crashworthiness, and a method for producing the same.
- An aspect of the present disclosure provides a hot press-formed member having excellent crack propagation resistance and ductility.
- the hot press-formed member comprising a base steel sheet and a plating layer comprising Zn or Zn alloy plating layer on the base steel sheet,
- a Mn(wt %)/Zn(wt %) content ratio measured at a point 1 ⁇ m from a surface of the plating layer is 0.1 or more
- a maximum crack depth penetrating the base steel sheet from an interface between the base steel sheet and the plating layer is 10 ⁇ m or less.
- a hot press-formed member having excellent ductility and crack propagation resistance while having a tensile strength of 1,300 MPa or more, may be provided.
- hot press-formed member of the present disclosure may be suitably used for automotive structural members or reinforcing materials that require corrosion resistance and crashworthiness.
- FIG. 1 is a cross-sectional view of a hat-shaped hot press-formed member according to an embodiment of the present disclosure.
- FIG. 2 is photographs of cross-sections of Inventive Example and Comparative Example according to an embodiment of the present disclosure.
- the present inventors In manufacturing a hot press-formed member using a coated steel sheet, the present inventors have investigated on improving ductility and crack propagation resistance, as well as strength, of the hot press-formed member.
- the present inventors have confirmed that when heating and hot forming temperatures, post-heating process conditions, and the like, are optimized, a hot press-formed member having desired properties may be provided.
- the plated material is heated at a high temperature and formed at the high temperature, and when heating at the high temperature, a large quantity of soft zinc oxides are formed on the surface of the plated material, which generate microcracks when forming, so fatigue properties and bending properties of the hot press-formed member deteriorate.
- coarse-grained prior austenite may be formed, and it may be difficult to achieve sufficient retained austenite as a microstructure of a final hot press-formed member, so the hot press-formed member thus produced may be unsuitable for use as crashworthy and impact-absorbing members.
- a content of manganese (Mn) in the plated material is increased, so when heating to a high temperature for hot forming, hard manganese oxides may be formed on the surface relatively more than zinc oxides, resulting in an increased number of microcracks on a wall part of the plating layer (for example, the observed surface shown in FIG. 1 ), the part to which shear deformation is applied when forming, thus distributing shear deformation stress.
- the present disclosure may improve microcrack propagation resistance.
- the present disclosure may reduce a prior austenite grain size and ensure a sufficient retained austenite phase to improve crashworthy properties.
- the present disclosure may further stabilize the retained austenite phase, further improve yield strength, and further improve crashworthiness by reducing dislocation density within martensite.
- An aspect of the present disclosure provides a hot press-formed member having excellent crack propagation resistance and ductility, comprising a base steel sheet and a zinc or zinc alloy plating layer on at least one surface of the base steel sheet.
- the base steel sheet may be a hot-rolled steel sheet or cold-rolled steel sheet containing a certain percentage of manganese (Mn), and more particularly, the base steel sheet preferably contains, by wt %, carbon (C): 0.08 to 0.30%, silicon (Si): 0.01 to 2.0%, manganese (Mn): 3.1-8.0%, aluminum (Al): 0.001-0.5%, phosphorus (P): 0.001-0.05%, sulfur (S): 0.0001-0.02%, and nitrogen (N): 0.02% or less.
- C carbon
- Si silicon
- Mn manganese
- Al aluminum
- P phosphorus
- S sulfur
- N nitrogen
- Carbon (C) is an essential element for improving the strength of a hot press-formed member, and in the present disclosure, is useful for securing retained austenite that needs to be formed to achieve excellent ductility, and therefore, should be added in a proper amount.
- the content of carbon (C) is less than 0.08%, it may be difficult to achieve sufficient strength and ductility, so it may be preferable that carbon (C) be added in an amount of 0.08% or more. However, if the content of carbon (C) exceeds 0.30%, the cold rolling property of a hot-rolled steel sheet may be markedly lowered in a cold rolling process because the strength of the hot-rolled steel sheet may be too high, and spot weldability may be markedly lowered as well.
- the content of carbon (C) be limited to 0.08-0.30%.
- Silicon (Si) is added to remove oxygen in a steel making process, suppress the formation of carbides, which markedly affects the strength of a hot press-formed member, and is an element useful for securing retained austenite by concentrating carbon (C) along grain boundaries of lath martensite after martensite is formed when hot forming.
- the content of silicon (Si) is less than 0.01%, the above-described effects may not be achieved, and it may be difficult to achieve a high degree of cleanliness of steel, moreover, controlling the content of silicon (Si) may be costly. Meanwhile, the content of silicon (Si) exceeding 2.0% may markedly lower coatability when plating with zinc or a zinc alloy, and thus may not be preferable.
- the content of silicon (Si) be limited to 0.01-2.0%. It may be more preferable that silicon (Si) be added in an amount of 1.5% or less, and even more preferable that silicon (Si) be added in an amount of 0.7% or less.
- Manganese (Mn) is an extremely important element in the present disclosure.
- Manganese (Mn) serves to provide solid solution strengthening effects, serves to lower an Ac3 temperature (the temperature at which 100% transformation to austenite takes place during heating), and serves to lower an Ms temperature (the temperature at which martensitic transformation begins).
- the hot forming is performed in relatively low temperature regions, and when the heated material, after being extracted from the heating furnace, is cooled to a temperature for the hot forming, the manganese (Mn) suppresses the formation of ferrite which causes degradations in strength, and therefore, needs to be added in a sufficient amount.
- the content of manganese (Mn) is less than 3.1%, the above-described effects may not be sufficiently achieved, and if the content of manganese (Mn) exceeds 8.0%, the strength of the steel sheet before performing the hot forming becomes excessively high, thus degrading workability, and even when the temperature of the material is increased, hot forming properties may deteriorate, and the manufacturing costs of alloy components may be increased, thus lowering manufacturing competitiveness.
- the content of manganese (Mn) be limited to 3.1-8.0%, and more preferably, to 3.5-8.0%.
- Aluminum (Al) is an element effective in removing oxygen in a steel making process, along with the silicon (Si), to increase a degree of cleanliness of steel.
- the content of aluminum (Al) is less than 0.001%, the above-described effect may be difficult to achieve, and if the content of aluminum (Al) exceeds 0.5%, the Ac3 temperature may be excessively elevated, so that a heating temperature for the hot forming may need to be increased even further.
- the content of aluminum (Al) be limited to 0.001-0.5%.
- Phosphorus (P) exists as an impurity in steel, and high manufacturing costs may be incurred to keep the content of phosphorus (P) less than 0.001%, whereas a content of phosphorus (P) exceeding 0.05% may markedly decrease the weldability of a hot press-formed member, and thus may not be preferable.
- the content of phosphorus (P) be limited to 0.001-0.05%, and more preferably, to 0.02% or less.
- Sulfur (S) exists as an impurity in steel, and is an element negatively affecting the ductility, impact properties, and weldability of a hot press-formed member, and thus, it may be preferable that the content of sulfur (S) be limited to 0.02% or less. However, manufacturing costs may markedly increase to keep the content of sulfur (S) less than 0.0001%, so it may be preferable that a lower limit of the content of sulfur (S) be limited to 0.0001%.
- the content of sulfur (S) be limited to 0.0001-0.02%, and more preferably, to 0.01% or less.
- Nitrogen (N) is an element contained as an impurity in steel, and if the content of nitrogen (N) exceeds 0.02%, a slab may become prone to cracking during continuous casting, and impact properties may deteriorate as well.
- the content of nitrogen (N) be limited to 0.02% or less.
- manufacturing costs may drastically increase for keeping the content of nitrogen (N) less than 0.0001%, so it may be preferable that a lower limit of the content of nitrogen (N) be limited to 0.0001%.
- the base steel sheet of the present disclosure in addition to the above-described alloy composition, may further contain the following elements, which will be described below. Particularly, the base steel sheet may further contain, preferably, at least one group selected from the following groups (1) to (4), and reasons for limiting the alloy composition of each group will be fully described in detail hereinbelow.
- Chromium (Cr) and molybdenum (Mo) are elements useful for achieving strength and grain refinement through improving hardenability and precipitation strengthening effects. If the total content of at least one of chromium (Cr) and molybdenum (Mo) is less than 0.001%, the above-described effects may not be achieved, however, the total content thereof exceeding 2.0% may saturate these effects, and also cause weldability to deteriorate and manufacturing costs to increase, and thus may not be preferable.
- Titanium (Ti), niobium (Nb), and vanadium (V) have the effect of improving the strength of a hot press-formed member by forming fine precipitates, as well as the effect of stabilizing retained austenite and improving impact toughness by inducing grain refinement. If the total content of at least one among titanium (Ti), niobium (Nb), and vanadium (V) is less than 0.001%, the above-described effects may be difficult to achieve; however, a total content thereof exceeding 0.2% may saturate these effects, and incur an increase in the cost for ferro-alloys, and thus may not be preferable.
- the total content of at least one among titanium (Ti), niobium (Nb), and vanadium (V) may be preferable to limit the total content of at least one among titanium (Ti), niobium (Nb), and vanadium (V) to 0.001-0.2%.
- Copper (Cu) may be added as an element improving strength by forming fine precipitates, and nickel (Ni) may be optionally added, as needed, since hot brittleness may be caused when copper (Cu) is added alone. If the total content of at least one of copper (Cu) and nickel (Ni) is less than 0.005%, the above-described effects may be difficult to achieve, however, the total content thereof exceeding 2.0% may incur an excessive increase in the cost.
- the total content of at least one of copper (Cu) and nickel (Ni) added may be preferable to limit the total content of at least one of copper (Cu) and nickel (Ni) added to 0.005-2.0%.
- boron (B) may improve hardenability, and boron (B) segregates along prior-austenite grain boundaries to suppress embrittlement of a hot press-formed member caused by phosphorus (P) and/or sulfur (S) segregating along grain boundaries. If the content of boron (B) is less than 0.0001%, the above-described effects may be difficult to achieve; however, the content of boron (B) exceeding 0.01% may saturate these effects, causing brittleness when hot rolling.
- boron (B) added it may be preferable to limit the content of boron (B) added to 0.0001-0.01%, and more preferably, to 0.005% or less.
- the remainder component is iron (Fe).
- Fe iron
- the hot press-formed member of the present disclosure comprises a plating layer on at least one surface of a base steel sheet having the above-described composition, wherein the plating layer is a zinc or zinc alloy plating layer, and may be, for example, a zinc (Zn)-plated layer, a zinc (Zn)-iron (Fe) plated layer, a zinc (Zn)-aluminum (Al) alloy plated layer, or a zinc (Zn)-aluminum (Al)-magnesium (Mg) alloy plated layer.
- the plating layer is not limited thereto.
- the hot press-formed member of the present disclosure may preferably comprise 1-30 area % of retained austenite in microstructures thereof.
- phase fraction of the retained austenite is less than 1%, a desired level of ductility may not be achieved.
- the phase fraction of retained austenite exceeding 30% may guarantee excellent ductility, however, this may require carbon (C) or manganese (Mn) to be added in larger amounts, significantly degrading the spot weldability and impact properties of a hot press-formed member, and thus may not be preferable.
- phase fraction of retained austenite may be controlled through hot forming conditions, and when hot forming and the subsequent cooling are performed in the conditions proposed in the present disclosure, 1-20 area % of retained austenite phase may be formed, and when a tempering process after the cooling is further performed, 1-30 area % of retained austenite phase may be guaranteed.
- the phase fraction of retained austenite may be derived by calculating the area under an austenite peak, through an X-ray diffraction test.
- the remaining part other than the remained austenite phase may be preferably at least one of martensite and bainite, or at least one of tempered martensite and bainite.
- the hot press-formed member of the present disclosure has preferably a prior austenite grain size (PAGS) of 10 ⁇ m or less. If the PAGS exceeds 10 ⁇ m, the amount of impurities per unit area, such as P or S segregating along grain boundaries, increases during a heat treatment, and microcrack propagation may be difficult to suppress, so crashworthy characteristics may deteriorate.
- PAGS prior austenite grain size
- the PAGS be 10 ⁇ m or less, more preferably, 7 ⁇ m or less, and even more preferably, 5 ⁇ m or less.
- a ratio of manganese to zinc (Mn (wt %)/Zn (wt %)) in an oxide layer of 0.5-1.2 ⁇ m in a thickness direction from the surface layer of a plating layer be 0.1 or more.
- An upper limit of the ratio of manganese to zinc (Mn/Zn) in the oxide layer is not limited to any particular value, however, for the upper limit to exceed 2.0, the content of manganese (Mn) needs to exceed 8%, in which case manufacturing costs may increase and operationality may suffer. Accordingly, it may be preferable to limit the upper limit of the ratio of manganese to zinc to 2.0.
- a base steel sheet containing the above-described alloy composition it may be preferable to prepare a base steel sheet containing the above-described alloy composition and then, to plate the base steel sheet with zinc or a zinc alloy to produce a coated steel sheet.
- the base steel sheet as described above, may be a hot-rolled steel sheet or a cold-rolled steel sheet, and may be produced by the method described below.
- the hot-rolled steel sheet may preferably be produced by re-heating a steel slab having the above-described alloy components, and subjecting the steel slab to a finish hot-rolling process and a coiling process.
- the steel slab be heated to a heating temperature of 1,000-1,300° C. If the heating temperature is less than 1,000° C., it may be difficult to homogenize the structure and composition of the slab, however, the heating temperature exceeding 1,300° C. may give rise to excessive oxidation and equipment degradation, and thus, may not be preferable.
- the reheated slab may be finish hot rolled to produce a hot-rolled steel sheet.
- the finish hot rolling may be performed preferably at a temperature of Ar3 to 1,000° C., and if the finish hot rolling temperature is Ar3 or less, the rolling may occur in a two-phase region, and thus, it may be difficult to control the structure of surface mixed grains and the shape of a steel sheet. If the finish hot rolling temperature exceeds 1,000° C., the grains of the hot-rolled material may become coarse.
- the hot-rolled steel sheet produced above may be coiled into the shape of a coil, preferably at a temperature of 750° C. or less while exceeding Ms. If the coiling temperature is Ms or less, the strength of the hot-rolled material may become excessively high, thus increasing the load for subsequently performed cold rolling. If the coiling temperature exceeds 750° C., the oxidation of grain boundaries of the hot-rolled material may be excessive, thereby causing pickling properties to deteriorate.
- the cold-rolled steel sheet may be produced, preferably by pickling, cold rolling, and annealing the hot-rolled steel sheet produced above.
- the cold rolling is to manufacture a cold-rolled steel sheet having a desired thickness, and may be preferably performed at a reduction ratio of 10-80%.
- the cold-rolled steel sheet obtained above may be preferably annealed in a continuous annealing furnace to lower the strength thereof.
- the strength of the steel sheet may be effectively lowered by performing continuous annealing at a temperature of 600-900° C. for 1-1000 seconds.
- the hot-rolled steel sheet before or after performing the pickling treatment, prior to performing the cold rolling may be subjected to a batch annealing process. This is to lower the strength of the hot-rolled material, and may preferably be performed at a temperature of 400-700° C. for 1-100 hours, in particular.
- the hot-rolled steel sheet or cold-rolled steel sheet produced as described above be subjected to a plating process to produce a coated steel sheet.
- the plating process is not limited to any particular process, but may be zinc or zinc alloy plating.
- hot dip zinc plating, hot dip zinc alloy plating, or electrical zinc plating may all be applicable.
- the base steel sheet is a cold-rolled steel sheet, it may be preferable that electrical zinc plating be performed.
- the hot dip zinc alloy plating may be zinc-aluminum alloy plating, zinc-aluminum-manganese alloy plating, or the like.
- Such plating processes may be performed to their respective conventional conditions, so such conditions are not limited to particular conditions.
- metal coating with iron (Fe), nickel (Ni), or the like may be performed for the purpose of improving plating adhesion.
- the coated steel sheet obtained according to an embodiment of the present disclosure may be hot formed to produce a hot press-formed member.
- the coated steel sheet be heated to and maintained at a temperature equal to or greater than a certain temperature.
- the coated steel sheet be introduced in a heating furnace and heated to a temperature equal to or greater than Ac3, which is equal to or greater than a single phase of austenite, at a heating rate of 1-1,000° C./s, and be maintained for 5-10,000 seconds.
- a maximum heating temperature is preferably within a temperature range from more than Ac3+10° C. to less than Ac3+200° C.
- the maximum heating temperature is Ac3+10° C. or less, even if heated to a temperature equal to or greater than Ac3, local regions may exist where carbon (C) and/or manganese (Mn) are not segregated, thus, complete transformation to austenite may not take place, causing prior-ferrite to remain, and thus, yield strength may not be sufficiently improved.
- springback of the hot press-formed member may be excessive, making it difficult to achieve shape fixability.
- the maximum heating temperature is Ac3+200° C. or more, it may be easy to achieve sufficient strength and shape fixability, but spot weldability may deteriorate due to an excessive formation of oxides on the surface of the plating layer.
- the coated steel sheet be maintained in the above-described temperature regions, however, if the maintaining time is less than 5 seconds, complete austenization may not take place, and also, it may be difficult to achieve a Mn/Zn content ratio of 0.1 or more in surface oxides.
- the maintaining time exceeding 10,000 seconds may reduce spot weldability due to an excessive formation of oxides on the surface.
- a cooling rate be controlled to be less than 50° C./s, since in order to keep the cooling rate to be 50° C./s or more, separate cooling equipment may be required, undesirably incurring an increase in manufacturing costs. Therefore, it may be more preferable that the cooling be performed at a cooling rate less than 30° C./s, and even more preferably, at a cooling rate less than 15° C./s.
- the cooling rate less than 1° C./s may cause ferrite to be formed during the cooling, thus undesirably lowering the strength of the hot press-formed member. Accordingly, when performing the cooling, it may be preferable that a lower limit of the cooling rate be limited to 1° C./s.
- the hot forming temperature is controlled to 400-650° C.
- the hot forming be performed at a temperature of 650° C. or less, and not at conventional temperatures.
- the hot forming temperature is 650° C. or less, although it may vary depending on the heating temperature, the composition of the base iron, or the like, the strength of grain boundaries may become greater than the strength of the base iron, thus, it may be possible to improve microcrack formation and propagation resistance in the hot press-formed member.
- the hot forming temperature is too low, below 400° C., martensitic or bainitic transformation may occur prior to hot forming, causing hot forming properties to deteriorate.
- the hot forming be performed at a temperature of 400-650° C.
- cooling be performed to a temperature of 100° C. or less at a cooling rate of 1° C./s or more, to produce a final hot press-formed member.
- ferrite may be formed as a final microstructure, making it undesirably difficult to achieve ultra-high strength.
- the critical cooling rate is 25° C./s or higher; however, in the present disclosure, manganese (Mn), a component of the steel composition, is added in an amount of 3.1% or more, so even at a slow cooling rate of 1° C./s higher, ferrite may not be formed.
- the cooling may preferably be performed at a cooling rate of 5° C./s or higher, and more preferably, at a cooling rate of 10° C./s or higher.
- the upper limit of the cooling rate is not limited to any particular value; however, with regard to equipment costs, it is preferable to limit the upper limit of the cooling rate to 1,000° C./s.
- a hot press-formed member comprising 1-20 area % of retained austenite, and remaining at least one of martensite and bainite, as a microstructure, may be obtained.
- a tempering step of heating the hot press-formed member cooled as described above to a temperature of 150-600° C. and maintaining the hot press-formed member for 1-100,000 seconds may be further comprised. This is to increase the stability of retained austenite, a microstructure of the hot press-formed member.
- a hot press-formed member comprising 1-30 area % of retained austenite, and remaining at least one of tempered martensite and bainite, as a microstructure, may be obtained.
- the tempering temperature is less than 150° C. or the maintaining time is less than one second, it may be undesirably difficult to achieve a sufficient stability of retained austenite phase.
- the tempering temperature exceeds 600° C., the strength of the hot press-formed member may be markedly lowered, and the prior austenite grain size may grow to be coarse, thus lowering impact toughness and causing heat-induced deformation, and consequently, lowering precision in the shape of a member.
- the maintaining time exceeding 100,000 seconds may markedly reduce the strength of the hot press-formed member and may consume time excessively, thus undesirably reducing the productivity of the member.
- the hot-rolled steel sheets were pickled and cold-rolled at a cold reduction rate of 50% to produce cold-rolled steel sheets. Only when the hot-rolled steel sheet had a tensile strength of 1,500 MPa or greater, batch annealing was performed prior to the cold rolling. The batch annealing was performed by heating to 600° C. at a rate of 30° C./hour, maintaining for 10 hours, and cooling to room temperature at a cooling rate of 30° C./hour. Thereafter, the cold-rolled steel sheets were continuously annealed at 780° C., and were subjected to hot-dip galvanization (GI) or galvannealing (GA) to produce coated steel sheets. Some of the cold-rolled steel sheets were subjected to electrogalvanization (EG) to produce coated steel sheets. The GI, the GA, and the EG were performed under respective conventional conditions.
- GI hot-dip galvanization
- GA galvannealing
- the coated steel sheets produced above were each produced as a hat-shaped hot pressed formed member as shown in FIG. 1 .
- the coated steel sheets were introduced into a heating furnace maintained under air atmosphere, and were heated to a maximum target temperature and maintained for a target time, and then extracted from the heating furnace. Subsequently, the coated steel sheets were cooled to a hot forming temperature, and then hot formed and rapid cooled at the hot forming temperature to produce hat-shaped hot press-formed members.
- the conditions for the heating, cooling, and hot forming are shown in Table 2.
- V ⁇ ⁇ ⁇ ( % ) [ 1 2.429 ( 1 ⁇ ⁇ 200 1 ⁇ ⁇ 200 ) + 1 ] + [ 1 1.279 ( 1 ⁇ ⁇ 200 1 ⁇ ⁇ 220 ) + 1 ] + [ 1 1.464 ( 1 ⁇ ⁇ 200 1 ⁇ ⁇ 311 ) + 1 ] + [ 1 1.328 ( 1 ⁇ ⁇ 211 1 ⁇ ⁇ 200 ) + 1 ] + [ 1 0.699 ( 1 ⁇ ⁇ 211 1 ⁇ ⁇ 220 ) + 1 ] + [ 1 0.801 ( 1 ⁇ ⁇ 211 1 ⁇ ⁇ 311 ) + 1 ] 6 ⁇ 100
- a prior austenite grain size was calculated as an average value of average grain sizes measured at 5 different points at a 1 ⁇ 4 point of thickness of each base iron by using an image analyzing program, and the results are shown in Table 2.
- Some of the hat-shaped hot press-formed members were introduced in a heating furnace preheated to a target temperature, and were tempered and air-cooled.
- the tempering conditions were as shown in Table 3.
- TS represents tensile strength
- El represents elongation
- fractions other than the fraction of a retained austenite phase are of one or more types selected from bainite and martensite.
- Steel G in Table 1 has the alloy composition of 22MnB5 steel, and has a low content of manganese (Mn) of 1.2%. Meanwhile, Steels A to F all have a content of manganese (Mn) in the range of 3.1-8.0%, all satisfying the alloy composition of the present disclosure.
- Steels A-1 to A-5 are Inventive Examples satisfying the hot press forming conditions proposed in the present disclosure, all of which have a retained austenite phase fraction of 1% or more, a PAGS of 10 ⁇ m or less, a Mn/Zn content ratio of 0.1 or more, and a maximum crack depth of 10 ⁇ m or less. Also, these Inventive Examples have achieved excellent ductility as well as ultra-high strength.
- Steels A-6 and A-7 are the cases with a high hot forming temperature of 710° C., and maximum crack depths exceeding 10 ⁇ m were observed even when the retained austenite phase fraction was 1% or more.
- Steel A-8 is the case with too short a maintaining time after heating, and it failed to achieve a Mn/Zn content ratio of 0.1 or more, thus, the maximum crack depth exceeded 10 ⁇ m.
- Steels B-1, C-1, D-1, E-1, and F-1 all have satisfied the hot press forming conditions proposed in the present disclosure, and thus, all have a retained austenite phase fraction of 1% or more, a PAGS of 10 ⁇ m or less, and a Mn/Zn content ratio of 0.1 or more, and had no observable microcracks.
- these Inventive Examples have achieved excellent ductility as well as ultra-high strength.
- Steel G-1 has, not only an insufficient alloy composition, but also, due to a high hot forming temperature, an insufficiently formed retained austenite phase, a coarse PAGS, and a Mn/Zn content ratio of less than 0.1, and thus, an extremely large maximum crack depth of 28.5 ⁇ m was observed.
- the hot forming temperature satisfied the present disclosure, it had a coarse PAGS and a Mn/Zn content ratio of less than 0.1, and thus, the maximum crack depth exceeded 10 ⁇ m, and the tensile strength was 631 MPa, thus failing to achieve ultra-high strength.
- FIG. 2 shows microcracks observed in hot press-formed members of Steel B-1 (Inventive Example 6) and Steel A-6 (Comparative Example 1).
- Comparative Examples 6 to 9 (G-1-1 to G-1-4), even after the tempering, the retained austenite phase was not sufficiently formed, thus resulting in inferior ductility, and Comparative Example 10 (G-1-5) failed to achieve ultra-high strength.
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Abstract
Provided is a hot press-formed member having excellent crack propagation resistance and ductility. The hot press-formed member includes: a base steel sheet and a zinc or zinc alloy plating layer on at least one surface of the base steel sheet. The base steel sheet contains, by wt %, carbon (C): 0.08-0.30%, silicon (Si): 0.01-2.0%, manganese (Mn): 3.1-8.0%, aluminum (Al): 0.001-0.5%, phosphorus (P): 0.001-0.05%, sulfur (S): 0.0001-0.02%, nitrogen (N): 0.02% or less, and a balance of iron (Fe) and other impurities. The hot press-formed member comprises 1-30 area % of retained austenite as a microstructure, and a Mn(wt %)/Zn(wt %) content ratio in an oxide layer of 0.5-1.2 μm in a thickness direction from a surface layer of the plating layer is 0.1 or more.
Description
- This application is a Continuation patent application of U.S. patent application Ser. No. 16/315,767, filed on Jan. 7, 2019, which is the U.S. National Phase under 35 U.S.C. § 371 of International Patent Application No. PCT/KR2017/007328, filed on Jul. 17, 2017, which in turn claims the benefit of Korean Application No. 10-2016-0086248, filed on Jul. 7, 2016, the disclosures of which applications are incorporated by reference herein.
- The present disclosure relates to a hot press-formed member suitable for use as an automotive material, and more specifically, to a hot press-formed member having excellent crack propagation resistance and ductility, and to a method for producing the same.
- Recently, hot press-formed members have been widely used as automotive structural members for purposes such as reducing the weight of a vehicle and improving the fuel efficiency of a vehicle, and a great deal of research has been conducted for such purposes.
- For example, the invention disclosed in Patent Document 1 may provide a member having an ultra-high strength in the range of 1,500 MPa or greater in tensile strength, by hot press forming and rapid cooling an aluminum-plated steel sheet after heating the same to 850° C. or higher. In addition, due to the formation of an Al—Fe alloy layer, a steel sheet having excellent corrosion resistance may be provided.
- However, according to the patent document, the main phase of a coated steel sheet is formed by aluminum, so it may be difficult to exploit the sacrificial effects of aluminum, and ductility cannot be improved.
- In this context, Patent Document 2 discloses a technique to effectively achieve the sacrificial effects of a hot press-formed member, the technique characterized in that after a Zn-plated steel material is heated at 880-980° C. for 6-15 minutes, a buffer layer is formed at boundaries between a base steel sheet and a plating layer.
- However, in this case, as a heating temperature becomes 880° C. or greater, spot weldability deteriorates due to zinc oxides formed on a zinc surface, and ductility cannot be improved, and due to an inferior crack propagation resistance, it is difficult to control the depths of microcracks to be 10 μm or less.
- For hot press-formed members to be suitable for use as impact-resistant members of vehicles, the hot press-formed members not only require ultra-high strength, but also need to have improved corrosion resistance and crack propagation resistance, as well as fatigue properties and crashworthiness, and therefore, it is necessary to develop a hot press-formed member that satisfies the aforementioned properties.
- (Patent Document 1) U.S. Pat. No. 6,296,805
- (Patent Document 2) Korean Laid-Open Patent Application No. 2014-0035033
- An aspect of the present disclosure is to provide a hot press-formed member having excellent crack propagation resistance and ductility, which may be suitably used for automotive structural members or reinforcing materials that require corrosion resistance and crashworthiness, and a method for producing the same.
- An aspect of the present disclosure provides a hot press-formed member having excellent crack propagation resistance and ductility.
- According to an aspect of the present disclosure, the hot press-formed member comprising a base steel sheet and a plating layer comprising Zn or Zn alloy plating layer on the base steel sheet,
- wherein a Mn(wt %)/Zn(wt %) content ratio measured at a point 1 μm from a surface of the plating layer is 0.1 or more,
- wherein a maximum crack depth penetrating the base steel sheet from an interface between the base steel sheet and the plating layer is 10 μm or less.
- According to the present disclosure, a hot press-formed member having excellent ductility and crack propagation resistance while having a tensile strength of 1,300 MPa or more, may be provided.
- In addition, the hot press-formed member of the present disclosure may be suitably used for automotive structural members or reinforcing materials that require corrosion resistance and crashworthiness.
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FIG. 1 is a cross-sectional view of a hat-shaped hot press-formed member according to an embodiment of the present disclosure. -
FIG. 2 is photographs of cross-sections of Inventive Example and Comparative Example according to an embodiment of the present disclosure. - In manufacturing a hot press-formed member using a coated steel sheet, the present inventors have investigated on improving ductility and crack propagation resistance, as well as strength, of the hot press-formed member.
- As a result, the present inventors have confirmed that when heating and hot forming temperatures, post-heating process conditions, and the like, are optimized, a hot press-formed member having desired properties may be provided.
- In a conventional hot forming method using a zinc or zinc alloy plating material, the plated material is heated at a high temperature and formed at the high temperature, and when heating at the high temperature, a large quantity of soft zinc oxides are formed on the surface of the plated material, which generate microcracks when forming, so fatigue properties and bending properties of the hot press-formed member deteriorate. In addition, coarse-grained prior austenite may be formed, and it may be difficult to achieve sufficient retained austenite as a microstructure of a final hot press-formed member, so the hot press-formed member thus produced may be unsuitable for use as crashworthy and impact-absorbing members.
- In light of the above, when manufacturing a hot press-formed member using a zinc or zinc alloy plating material, in the present disclosure, a content of manganese (Mn) in the plated material is increased, so when heating to a high temperature for hot forming, hard manganese oxides may be formed on the surface relatively more than zinc oxides, resulting in an increased number of microcracks on a wall part of the plating layer (for example, the observed surface shown in
FIG. 1 ), the part to which shear deformation is applied when forming, thus distributing shear deformation stress. In addition, by having a hot forming temperature in a lower temperature region than in the conventional method, the present disclosure may improve microcrack propagation resistance. In addition, the present disclosure may reduce a prior austenite grain size and ensure a sufficient retained austenite phase to improve crashworthy properties. In addition, through a post-heat treatment process (referring to a tempering process in the present disclosure), the present disclosure may further stabilize the retained austenite phase, further improve yield strength, and further improve crashworthiness by reducing dislocation density within martensite. - Hereinbelow, the present disclosure will be more fully described in detail.
- An aspect of the present disclosure provides a hot press-formed member having excellent crack propagation resistance and ductility, comprising a base steel sheet and a zinc or zinc alloy plating layer on at least one surface of the base steel sheet.
- The base steel sheet may be a hot-rolled steel sheet or cold-rolled steel sheet containing a certain percentage of manganese (Mn), and more particularly, the base steel sheet preferably contains, by wt %, carbon (C): 0.08 to 0.30%, silicon (Si): 0.01 to 2.0%, manganese (Mn): 3.1-8.0%, aluminum (Al): 0.001-0.5%, phosphorus (P): 0.001-0.05%, sulfur (S): 0.0001-0.02%, and nitrogen (N): 0.02% or less.
- Hereinbelow, reasons for limiting the alloy composition of the base steel sheet will be described in detail, and the content of each component is provided in wt % unless otherwise specified.
- C: 0.08 to 0.30%
- Carbon (C) is an essential element for improving the strength of a hot press-formed member, and in the present disclosure, is useful for securing retained austenite that needs to be formed to achieve excellent ductility, and therefore, should be added in a proper amount.
- If the content of carbon (C) is less than 0.08%, it may be difficult to achieve sufficient strength and ductility, so it may be preferable that carbon (C) be added in an amount of 0.08% or more. However, if the content of carbon (C) exceeds 0.30%, the cold rolling property of a hot-rolled steel sheet may be markedly lowered in a cold rolling process because the strength of the hot-rolled steel sheet may be too high, and spot weldability may be markedly lowered as well.
- Accordingly, in the present disclosure, it may be preferable that the content of carbon (C) be limited to 0.08-0.30%.
- Si: 0.01 to 2.0%
- Silicon (Si) is added to remove oxygen in a steel making process, suppress the formation of carbides, which markedly affects the strength of a hot press-formed member, and is an element useful for securing retained austenite by concentrating carbon (C) along grain boundaries of lath martensite after martensite is formed when hot forming.
- If the content of silicon (Si) is less than 0.01%, the above-described effects may not be achieved, and it may be difficult to achieve a high degree of cleanliness of steel, moreover, controlling the content of silicon (Si) may be costly. Meanwhile, the content of silicon (Si) exceeding 2.0% may markedly lower coatability when plating with zinc or a zinc alloy, and thus may not be preferable.
- Accordingly, in the present disclosure, it may be preferable that the content of silicon (Si) be limited to 0.01-2.0%. It may be more preferable that silicon (Si) be added in an amount of 1.5% or less, and even more preferable that silicon (Si) be added in an amount of 0.7% or less.
- Mn: 3.1-8.0%
- Manganese (Mn) is an extremely important element in the present disclosure. Manganese (Mn) serves to provide solid solution strengthening effects, serves to lower an Ac3 temperature (the temperature at which 100% transformation to austenite takes place during heating), and serves to lower an Ms temperature (the temperature at which martensitic transformation begins). Particularly, in the present disclosure, the hot forming is performed in relatively low temperature regions, and when the heated material, after being extracted from the heating furnace, is cooled to a temperature for the hot forming, the manganese (Mn) suppresses the formation of ferrite which causes degradations in strength, and therefore, needs to be added in a sufficient amount.
- If the content of manganese (Mn) is less than 3.1%, the above-described effects may not be sufficiently achieved, and if the content of manganese (Mn) exceeds 8.0%, the strength of the steel sheet before performing the hot forming becomes excessively high, thus degrading workability, and even when the temperature of the material is increased, hot forming properties may deteriorate, and the manufacturing costs of alloy components may be increased, thus lowering manufacturing competitiveness.
- Accordingly, in the present disclosure, it may be preferable that the content of manganese (Mn) be limited to 3.1-8.0%, and more preferably, to 3.5-8.0%.
- Al: 0.001-0.5%
- Aluminum (Al) is an element effective in removing oxygen in a steel making process, along with the silicon (Si), to increase a degree of cleanliness of steel.
- If the content of aluminum (Al) is less than 0.001%, the above-described effect may be difficult to achieve, and if the content of aluminum (Al) exceeds 0.5%, the Ac3 temperature may be excessively elevated, so that a heating temperature for the hot forming may need to be increased even further.
- Accordingly, in the present disclosure, it may be preferable that the content of aluminum (Al) be limited to 0.001-0.5%.
- P: 0.001-0.05%
- Phosphorus (P) exists as an impurity in steel, and high manufacturing costs may be incurred to keep the content of phosphorus (P) less than 0.001%, whereas a content of phosphorus (P) exceeding 0.05% may markedly decrease the weldability of a hot press-formed member, and thus may not be preferable.
- Accordingly, in the present disclosure, it may be preferable that the content of phosphorus (P) be limited to 0.001-0.05%, and more preferably, to 0.02% or less.
- S: 0.0001-0.02%
- Sulfur (S) exists as an impurity in steel, and is an element negatively affecting the ductility, impact properties, and weldability of a hot press-formed member, and thus, it may be preferable that the content of sulfur (S) be limited to 0.02% or less. However, manufacturing costs may markedly increase to keep the content of sulfur (S) less than 0.0001%, so it may be preferable that a lower limit of the content of sulfur (S) be limited to 0.0001%.
- Accordingly, in the present disclosure, it may be preferable that the content of sulfur (S) be limited to 0.0001-0.02%, and more preferably, to 0.01% or less.
- N: 0.02% or less
- Nitrogen (N) is an element contained as an impurity in steel, and if the content of nitrogen (N) exceeds 0.02%, a slab may become prone to cracking during continuous casting, and impact properties may deteriorate as well.
- Accordingly, in the present disclosure, it may be preferable that the content of nitrogen (N) be limited to 0.02% or less. However, manufacturing costs may drastically increase for keeping the content of nitrogen (N) less than 0.0001%, so it may be preferable that a lower limit of the content of nitrogen (N) be limited to 0.0001%.
- The base steel sheet of the present disclosure, in addition to the above-described alloy composition, may further contain the following elements, which will be described below. Particularly, the base steel sheet may further contain, preferably, at least one group selected from the following groups (1) to (4), and reasons for limiting the alloy composition of each group will be fully described in detail hereinbelow.
- (1) At least one of chromium (Cr) and molybdenum (Mo), a total content thereof being 0.001-2.0%.
- (2) At least one among titanium (Ti), niobium (Nb), and vanadium (V), a total content thereof being 0.001-0.2%.
- (3) At least one of copper (Cu) and nickel (Ni), a total content thereof being 0.005-2.0%.
- (4) Boron (B): 0.0001-0.01%.
- The total content of at least one of chromium (Cr) and molybdenum (Mo): 0.001-2.0%
- Chromium (Cr) and molybdenum (Mo) are elements useful for achieving strength and grain refinement through improving hardenability and precipitation strengthening effects. If the total content of at least one of chromium (Cr) and molybdenum (Mo) is less than 0.001%, the above-described effects may not be achieved, however, the total content thereof exceeding 2.0% may saturate these effects, and also cause weldability to deteriorate and manufacturing costs to increase, and thus may not be preferable.
- Accordingly, in the present disclosure, it may be preferable to limit the total content of at least one of chromium (Cr) and molybdenum (Mo) added, to 0.001-2.0%.
- The total content of at least one among titanium (Ti), niobium (Nb), and vanadium (V): 0.001-0.2%
- Titanium (Ti), niobium (Nb), and vanadium (V) have the effect of improving the strength of a hot press-formed member by forming fine precipitates, as well as the effect of stabilizing retained austenite and improving impact toughness by inducing grain refinement. If the total content of at least one among titanium (Ti), niobium (Nb), and vanadium (V) is less than 0.001%, the above-described effects may be difficult to achieve; however, a total content thereof exceeding 0.2% may saturate these effects, and incur an increase in the cost for ferro-alloys, and thus may not be preferable.
- Accordingly, in the present disclosure, it may be preferable to limit the total content of at least one among titanium (Ti), niobium (Nb), and vanadium (V) to 0.001-0.2%.
- The total content of at least one of copper (Cu) and nickel (Ni): 0.005-2.0%
- Copper (Cu) may be added as an element improving strength by forming fine precipitates, and nickel (Ni) may be optionally added, as needed, since hot brittleness may be caused when copper (Cu) is added alone. If the total content of at least one of copper (Cu) and nickel (Ni) is less than 0.005%, the above-described effects may be difficult to achieve, however, the total content thereof exceeding 2.0% may incur an excessive increase in the cost.
- Accordingly, in the present disclosure, it may be preferable to limit the total content of at least one of copper (Cu) and nickel (Ni) added to 0.005-2.0%.
- Boron (B): 0.0001-0.01%
- The addition of even a small amount of boron (B) may improve hardenability, and boron (B) segregates along prior-austenite grain boundaries to suppress embrittlement of a hot press-formed member caused by phosphorus (P) and/or sulfur (S) segregating along grain boundaries. If the content of boron (B) is less than 0.0001%, the above-described effects may be difficult to achieve; however, the content of boron (B) exceeding 0.01% may saturate these effects, causing brittleness when hot rolling.
- Accordingly, in the present disclosure, it may be preferable to limit the content of boron (B) added to 0.0001-0.01%, and more preferably, to 0.005% or less.
- Other than the above-described alloy components, the remainder component is iron (Fe). However, since in a conventional manufacturing process, inevitable impurities may be introduced from raw materials or surrounding environments, these impurities should not be excluded. Since these impurities are well known to anyone skilled in the conventional manufacturing process, they will not be described in the present description.
- The hot press-formed member of the present disclosure comprises a plating layer on at least one surface of a base steel sheet having the above-described composition, wherein the plating layer is a zinc or zinc alloy plating layer, and may be, for example, a zinc (Zn)-plated layer, a zinc (Zn)-iron (Fe) plated layer, a zinc (Zn)-aluminum (Al) alloy plated layer, or a zinc (Zn)-aluminum (Al)-magnesium (Mg) alloy plated layer. However, the plating layer is not limited thereto.
- The hot press-formed member of the present disclosure may preferably comprise 1-30 area % of retained austenite in microstructures thereof.
- If a phase fraction of the retained austenite is less than 1%, a desired level of ductility may not be achieved. However, the phase fraction of retained austenite exceeding 30% may guarantee excellent ductility, however, this may require carbon (C) or manganese (Mn) to be added in larger amounts, significantly degrading the spot weldability and impact properties of a hot press-formed member, and thus may not be preferable.
- Meanwhile, the phase fraction of retained austenite, as will be described below, may be controlled through hot forming conditions, and when hot forming and the subsequent cooling are performed in the conditions proposed in the present disclosure, 1-20 area % of retained austenite phase may be formed, and when a tempering process after the cooling is further performed, 1-30 area % of retained austenite phase may be guaranteed.
- The phase fraction of retained austenite may be derived by calculating the area under an austenite peak, through an X-ray diffraction test.
- The remaining part other than the remained austenite phase may be preferably at least one of martensite and bainite, or at least one of tempered martensite and bainite.
- In addition, the hot press-formed member of the present disclosure has preferably a prior austenite grain size (PAGS) of 10 μm or less. If the PAGS exceeds 10 μm, the amount of impurities per unit area, such as P or S segregating along grain boundaries, increases during a heat treatment, and microcrack propagation may be difficult to suppress, so crashworthy characteristics may deteriorate.
- Accordingly, it may be preferable that the PAGS be 10 μm or less, more preferably, 7 μm or less, and even more preferably, 5 μm or less.
- The smaller the PAGS, the smaller the amount of impurities segregating along grain boundaries, and the easier it is to suppress the propagation of microcracks, however, manufacturing costs may markedly increase for keeping the PAGS under 0.1 μm, and thus, it may be preferable to limit the lower limit thereof to 0.1 μm.
- Further, in the hot press-formed member of the present disclosure, it may be preferable that a ratio of manganese to zinc (Mn (wt %)/Zn (wt %)) in an oxide layer of 0.5-1.2 μm in a thickness direction from the surface layer of a plating layer be 0.1 or more.
- As described above, by increasing the amount of manganese oxides in the oxide layer in a surface layer region of the plating layer, it is possible to effectively suppress the generation of microcracks in a side surface portion (for example, the observed surface shown in
FIG. 1 ) which mainly receives the effects of shear transformation during hot forming. - An upper limit of the ratio of manganese to zinc (Mn/Zn) in the oxide layer is not limited to any particular value, however, for the upper limit to exceed 2.0, the content of manganese (Mn) needs to exceed 8%, in which case manufacturing costs may increase and operationality may suffer. Accordingly, it may be preferable to limit the upper limit of the ratio of manganese to zinc to 2.0.
- Hereinbelow, a method for producing a hot press-formed member, another aspect of the present disclosure, will be described in detail.
- First, it may be preferable to prepare a base steel sheet containing the above-described alloy composition and then, to plate the base steel sheet with zinc or a zinc alloy to produce a coated steel sheet.
- The base steel sheet, as described above, may be a hot-rolled steel sheet or a cold-rolled steel sheet, and may be produced by the method described below.
- The hot-rolled steel sheet may preferably be produced by re-heating a steel slab having the above-described alloy components, and subjecting the steel slab to a finish hot-rolling process and a coiling process.
- For example, it may be preferable that in the re-heating process, the steel slab be heated to a heating temperature of 1,000-1,300° C. If the heating temperature is less than 1,000° C., it may be difficult to homogenize the structure and composition of the slab, however, the heating temperature exceeding 1,300° C. may give rise to excessive oxidation and equipment degradation, and thus, may not be preferable.
- Subsequently, the reheated slab may be finish hot rolled to produce a hot-rolled steel sheet. The finish hot rolling may be performed preferably at a temperature of Ar3 to 1,000° C., and if the finish hot rolling temperature is Ar3 or less, the rolling may occur in a two-phase region, and thus, it may be difficult to control the structure of surface mixed grains and the shape of a steel sheet. If the finish hot rolling temperature exceeds 1,000° C., the grains of the hot-rolled material may become coarse.
- Subsequently, the hot-rolled steel sheet produced above may be coiled into the shape of a coil, preferably at a temperature of 750° C. or less while exceeding Ms. If the coiling temperature is Ms or less, the strength of the hot-rolled material may become excessively high, thus increasing the load for subsequently performed cold rolling. If the coiling temperature exceeds 750° C., the oxidation of grain boundaries of the hot-rolled material may be excessive, thereby causing pickling properties to deteriorate.
- The cold-rolled steel sheet may be produced, preferably by pickling, cold rolling, and annealing the hot-rolled steel sheet produced above.
- At this point, the cold rolling is to manufacture a cold-rolled steel sheet having a desired thickness, and may be preferably performed at a reduction ratio of 10-80%.
- The cold-rolled steel sheet obtained above may be preferably annealed in a continuous annealing furnace to lower the strength thereof. The strength of the steel sheet may be effectively lowered by performing continuous annealing at a temperature of 600-900° C. for 1-1000 seconds.
- Also, the hot-rolled steel sheet before or after performing the pickling treatment, prior to performing the cold rolling, may be subjected to a batch annealing process. This is to lower the strength of the hot-rolled material, and may preferably be performed at a temperature of 400-700° C. for 1-100 hours, in particular.
- It may be preferable that the hot-rolled steel sheet or cold-rolled steel sheet produced as described above be subjected to a plating process to produce a coated steel sheet.
- The plating process is not limited to any particular process, but may be zinc or zinc alloy plating. In particular, when the base steel sheet is a hot-rolled steel sheet, hot dip zinc plating, hot dip zinc alloy plating, or electrical zinc plating may all be applicable. However, when the base steel sheet is a cold-rolled steel sheet, it may be preferable that electrical zinc plating be performed. For example, the hot dip zinc alloy plating may be zinc-aluminum alloy plating, zinc-aluminum-manganese alloy plating, or the like. Such plating processes may be performed to their respective conventional conditions, so such conditions are not limited to particular conditions.
- Further, prior to the plating process, metal coating with iron (Fe), nickel (Ni), or the like may be performed for the purpose of improving plating adhesion.
- As described above, the coated steel sheet obtained according to an embodiment of the present disclosure may be hot formed to produce a hot press-formed member.
- First, it may be preferable that the coated steel sheet be heated to and maintained at a temperature equal to or greater than a certain temperature. For example, it may be preferable that the coated steel sheet be introduced in a heating furnace and heated to a temperature equal to or greater than Ac3, which is equal to or greater than a single phase of austenite, at a heating rate of 1-1,000° C./s, and be maintained for 5-10,000 seconds.
- More preferably, when heating at the above-described heating rate, a maximum heating temperature is preferably within a temperature range from more than Ac3+10° C. to less than Ac3+200° C. When the maximum heating temperature is Ac3+10° C. or less, even if heated to a temperature equal to or greater than Ac3, local regions may exist where carbon (C) and/or manganese (Mn) are not segregated, thus, complete transformation to austenite may not take place, causing prior-ferrite to remain, and thus, yield strength may not be sufficiently improved. In addition, springback of the hot press-formed member may be excessive, making it difficult to achieve shape fixability. However, when the maximum heating temperature is Ac3+200° C. or more, it may be easy to achieve sufficient strength and shape fixability, but spot weldability may deteriorate due to an excessive formation of oxides on the surface of the plating layer.
- Accordingly, it may be preferable that the coated steel sheet be maintained in the above-described temperature regions, however, if the maintaining time is less than 5 seconds, complete austenization may not take place, and also, it may be difficult to achieve a Mn/Zn content ratio of 0.1 or more in surface oxides. The maintaining time exceeding 10,000 seconds may reduce spot weldability due to an excessive formation of oxides on the surface.
- It may be preferable that the coated steel sheet, heated and maintained as described above, after being extracted from the heating furnace, be cooled to a hot forming temperature. At this point, it may be preferable that a cooling rate be controlled to be less than 50° C./s, since in order to keep the cooling rate to be 50° C./s or more, separate cooling equipment may be required, undesirably incurring an increase in manufacturing costs. Therefore, it may be more preferable that the cooling be performed at a cooling rate less than 30° C./s, and even more preferably, at a cooling rate less than 15° C./s.
- The cooling rate less than 1° C./s may cause ferrite to be formed during the cooling, thus undesirably lowering the strength of the hot press-formed member. Accordingly, when performing the cooling, it may be preferable that a lower limit of the cooling rate be limited to 1° C./s.
- It may be preferable that hot forming be performed once the cooling is completed as described above. In the present disclosure, in order to improve microcrack formation and crack propagation resistance, the hot forming temperature is controlled to 400-650° C.
- Conventionally, it is preferable to increase the hot forming temperature as much as possible in order to improve processability and reduce a press load. However, when a zinc or zinc alloy plating steel sheet is thermally treated at a high temperature, zinc may be dispersed and introduced into grain boundaries, thus lowering the strength of grain boundaries of the base iron, and consequently, this may undesirably facilitate microcrack formation and crack propagation in the hot press-formed member.
- In light of the above, in the present disclosure, it may be preferable that the hot forming be performed at a temperature of 650° C. or less, and not at conventional temperatures. When the hot forming temperature is 650° C. or less, although it may vary depending on the heating temperature, the composition of the base iron, or the like, the strength of grain boundaries may become greater than the strength of the base iron, thus, it may be possible to improve microcrack formation and propagation resistance in the hot press-formed member. However, if the hot forming temperature is too low, below 400° C., martensitic or bainitic transformation may occur prior to hot forming, causing hot forming properties to deteriorate.
- Accordingly, in the present disclosure, it may be preferable that the hot forming be performed at a temperature of 400-650° C.
- Immediately after performing the hot forming in the above-described temperature ranges, it may be preferable that cooling be performed to a temperature of 100° C. or less at a cooling rate of 1° C./s or more, to produce a final hot press-formed member.
- At this point, when the cooling rate is less than 1° C./s, ferrite may be formed as a final microstructure, making it undesirably difficult to achieve ultra-high strength.
- Conventionally, in case of 22MnB5 steel, the critical cooling rate is 25° C./s or higher; however, in the present disclosure, manganese (Mn), a component of the steel composition, is added in an amount of 3.1% or more, so even at a slow cooling rate of 1° C./s higher, ferrite may not be formed. However, with regard to productivity, the cooling may preferably be performed at a cooling rate of 5° C./s or higher, and more preferably, at a cooling rate of 10° C./s or higher. The upper limit of the cooling rate is not limited to any particular value; however, with regard to equipment costs, it is preferable to limit the upper limit of the cooling rate to 1,000° C./s.
- Once the cooling is completed, a hot press-formed member comprising 1-20 area % of retained austenite, and remaining at least one of martensite and bainite, as a microstructure, may be obtained.
- In addition, a tempering step of heating the hot press-formed member cooled as described above to a temperature of 150-600° C. and maintaining the hot press-formed member for 1-100,000 seconds may be further comprised. This is to increase the stability of retained austenite, a microstructure of the hot press-formed member. When the cooling is completed after such a tempering treatment is performed, a hot press-formed member comprising 1-30 area % of retained austenite, and remaining at least one of tempered martensite and bainite, as a microstructure, may be obtained.
- When the tempering temperature is less than 150° C. or the maintaining time is less than one second, it may be undesirably difficult to achieve a sufficient stability of retained austenite phase. When the tempering temperature exceeds 600° C., the strength of the hot press-formed member may be markedly lowered, and the prior austenite grain size may grow to be coarse, thus lowering impact toughness and causing heat-induced deformation, and consequently, lowering precision in the shape of a member. Alternatively, the maintaining time exceeding 100,000 seconds may markedly reduce the strength of the hot press-formed member and may consume time excessively, thus undesirably reducing the productivity of the member.
- Hereinbelow, the present disclosure will be more fully described with reference to specific embodiments. However, it should be understood that the following embodiments are only examples and therefore, should not be used as an aid in determining the scope of the present disclosure, since the scope of the invention is determined by appended claims and reasonable equivalents thereof.
- A 40 mm-thick ingot, having the alloy composition shown in Table 1, was melted under vacuum and heated for one hour in a heating furnace at 1,200° C., and thereafter, was finish hot rolled at 900° C. and coiled at 680° C. to produce hot rolled steel sheets having a final thickness of 3 mm, wherein the furnace cooling temperature was 680° C.
- Next, the hot-rolled steel sheets were pickled and cold-rolled at a cold reduction rate of 50% to produce cold-rolled steel sheets. Only when the hot-rolled steel sheet had a tensile strength of 1,500 MPa or greater, batch annealing was performed prior to the cold rolling. The batch annealing was performed by heating to 600° C. at a rate of 30° C./hour, maintaining for 10 hours, and cooling to room temperature at a cooling rate of 30° C./hour. Thereafter, the cold-rolled steel sheets were continuously annealed at 780° C., and were subjected to hot-dip galvanization (GI) or galvannealing (GA) to produce coated steel sheets. Some of the cold-rolled steel sheets were subjected to electrogalvanization (EG) to produce coated steel sheets. The GI, the GA, and the EG were performed under respective conventional conditions.
- The coated steel sheets produced above were each produced as a hat-shaped hot pressed formed member as shown in
FIG. 1 . The coated steel sheets were introduced into a heating furnace maintained under air atmosphere, and were heated to a maximum target temperature and maintained for a target time, and then extracted from the heating furnace. Subsequently, the coated steel sheets were cooled to a hot forming temperature, and then hot formed and rapid cooled at the hot forming temperature to produce hat-shaped hot press-formed members. The conditions for the heating, cooling, and hot forming are shown in Table 2. - Tensile testing, microstructure observation, and XRD and GDS analyses were performed using respective hot press-formed member specimens. The tensile testing was performed at a testing rate of 10 mm/min using a JIS 5 test piece, and phase fractions of microstructures were calculated from the following equation using the integrated intensities of retained austenite peaks (γ) and martensite peaks obtained from the Cu target X-ray diffraction analysis, and the results are shown in Table 2.
-
- After prior austenite grain boundaries were exposed by an etching method using hydrofluoric acid, a prior austenite grain size (PAGS) was calculated as an average value of average grain sizes measured at 5 different points at a ¼ point of thickness of each base iron by using an image analyzing program, and the results are shown in Table 2.
- In addition, a cross-section of the plating layer at R=4-30 mm from the lower end of a curved surface of the hat-shaped hot press-formed member was observed using an optical microscope, and a maximum crack depth penetrating a base iron from a boundary between the base iron and the plating layer was measured through an optical image analysis. As requested by the client, the specimens with a maximum crack depth exceeding 10 μm were determined to be unacceptable. To measure a Mn/Zn content ratio in surface oxides, an average Mn/Zn content ratio value was obtained from 1 μm point from each surface layer by using a glow discharge spectrometer (GDS), and the results are shown in Table 2.
- Some of the hat-shaped hot press-formed members were introduced in a heating furnace preheated to a target temperature, and were tempered and air-cooled. The tempering conditions were as shown in Table 3.
- As described above, mechanical properties and microstructure phase fractions (retained austenite) were measured by performing tensile testing and XRD analyses in the same manner as the above, using the tempered hot press-formed member specimens, and the results are shown in Table 3.
-
TABLE 1 Alloy Composition (wt %) Steel C Si Mn P S Al N B Others Notes A 0.18 0.20 3.8 0.015 0.0030 0.03 0.0033 0 0 Inventive Steel B 0.15 0.14 5.0 0.014 0.0025 0.03 0.0042 0 Ti: Inventive 0.03 Steel C 0.21 1.52 5.9 0.007 0.0011 0.02 0.0050 0.0035 Ti: Inventive 0.04 Steel D 0.20 0.15 6.7 0.009 0.0030 0.03 0.0050 0.0026 0 Inventive Steel E 0.25 1.51 6.8 0.007 0.0015 0.01 0.0037 0 Mo: Inventive 0.1 Steel F 0.26 0.10 7.5 0.017 0.0018 0.008 0.0062 0.0032 Ti: Inventive 0.02 Steel G 0.23 0.20 1.2 0.014 0.0024 0.03 0.0038 0.0025 Ti: Comparative 0.03 Steel -
TABLE 2 Hot Forming Conditions Maxi- Heating Main- Cooling Forming Mechanical Retained mum Tem- taining Rate Tem- Properties γ Mn/Zn Crack perature Time (° C./ perature TS El Fraction PAGS Content Depth Steel Plating (° C.) (sec) s) (° C.) (Mpa) (%) (%) (μm) Ratio (μm) Notes A-1 GI 800 60 10.3 620 1583 7.9 3.9 6.9 0.30 7.2 Inventive Example 1 A-2 GI 800 60 10.1 500 1547 7.2 3.3 6.8 0.32 3.5 Inventive Example 2 A-3 GI 800 60 31.5 500 1554 7.3 3.4 6.8 0.32 3.4 Inventive Example 3 A-4 GA 800 60 10.0 450 1490 8.3 3.4 6.2 0.31 0.0 Inventive Example 4 A-5 EG 800 60 9.7 400 1465 7.6 3.8 6.3 0.34 0.2 Inventive Example 5 A-6 GI 800 60 10.8 710 1662 7.8 3.1 6.3 0.28 22.3 Com- parative Example 1 A-7 GI 800 6 10.5 690 1627 8.1 3.5 6.0 0.29 17.8 Com- parative Example 2 A-8 GI 800 1 10.6 550 1592 7.8 3.5 6.2 0.09 10.6 Com- parative Example 3 B-1 GA 800 60 10.3 500 1653 9.6 4.0 4.1 0.39 0.0 Inventive Example 6 C-1 EG 780 120 10.5 500 2035 7.9 5.7 2.8 0.52 0.0 Inventive Example 7 D-1 GI 780 120 10.3 500 2089 6.7 6.5 2.5 0.64 0.0 Inventive Example 8 E-1 EG 780 120 10.4 500 2231 6.6 7.1 2.3 0.67 0.0 Inventive Example 9 F-1 GA 750 60 10.2 500 2407 7.3 11.3 1.8 0.72 0.0 Inventive Example 10 G-1 GI 930 60 12.7 750 1539 6.6 0.3 12.7 0.07 28.5 Com- parative Example 4 G-2 GI 930 60 11.5 550 631 18.2 0.1 12.5 0.05 10.3 Com- parative Example 5 - (In Table 1, TS represents tensile strength, and El represents elongation. Also, in Table 1, fractions other than the fraction of a retained austenite phase are of one or more types selected from bainite and martensite.)
-
TABLE 3 Tempering Conditions Re- Tem- Mechanical tained per- Properties γ ature Time YS TS El Fraction Steel (° C.) (sec) (MPa) (MPa) (%) (% ) Notes A-3 A-3-1 170 1800 1342 1581 9.4 4.3 Embodi- ment 11 B-1 B-1-1 170 1800 1311 1564 10.4 7.1 Embodi- ment 12 C-1 C-1-1 200 30 983 1931 10.5 6.4 Embodi- ment 13 C-1-2 300 30 1260 1770 11.7 8.1 Embodi- ment 14 C-1-3 400 30 1383 1572 12.9 12.8 Embodi- ment 15 C-1-4 500 30 1400 1452 15.8 17.8 Embodi- ment 16 D-1 D-1-1 200 30 989 1917 10.8 6.8 Embodi- ment 17 D-1-2 300 30 1240 1730 11.2 7.5 Embodi- ment 18 D-1-3 400 30 1239 1569 13.7 14.9 Embodi- ment 19 D-1-4 500 30 1231 1435 15.6 17.2 Embodi- ment 20 D-1-5 600 30 1072 1279 18.4 19.8 Embodi- ment 21 E-1 E-1-1 200 300 921 2052 11.9 7.8 Embodi- ment 22 E-1-2 300 300 1147 1836 13.4 13.6 Embodi- ment 23 E-1-3 400 30 1244 1671 14.9 15.6 Embodi- ment 24 E-1-4 500 30 1351 1568 18.9 20.7 Embodi- ment 25 F-1 F-1-1 500 30 1180 1423 12.6 23.9 Embodi- ment 26 G-1 G-1-1 200 1800 1162 1482 6.9 0.3 Com- parative Example 6 G-1-2 250 1800 1154 1425 7.1 0.4 Com- parative Example 7 G-1-3 300 1800 1185 1351 3.1 0.5 Com- parative Example 8 G-1-4 400 1800 1060 1162 3.1 0.6 Com- parative Example 9 G-1-5 500 1800 842 903 9.1 0.9 Com- parative Example 10 - (In Table 1, YS represents yield strength, TS represents tensile strength, and El represents elongation. Also, in Table 1, fractions other than the fraction of a retained austenite phase are of one or more types selected from bainite and tempered martensite.)
- Steel G in Table 1 has the alloy composition of 22MnB5 steel, and has a low content of manganese (Mn) of 1.2%. Meanwhile, Steels A to F all have a content of manganese (Mn) in the range of 3.1-8.0%, all satisfying the alloy composition of the present disclosure.
- As shown in Table 2, Steels A-1 to A-5 are Inventive Examples satisfying the hot press forming conditions proposed in the present disclosure, all of which have a retained austenite phase fraction of 1% or more, a PAGS of 10 μm or less, a Mn/Zn content ratio of 0.1 or more, and a maximum crack depth of 10 μm or less. Also, these Inventive Examples have achieved excellent ductility as well as ultra-high strength.
- Steels A-6 and A-7 are the cases with a high hot forming temperature of 710° C., and maximum crack depths exceeding 10 μm were observed even when the retained austenite phase fraction was 1% or more. Steel A-8 is the case with too short a maintaining time after heating, and it failed to achieve a Mn/Zn content ratio of 0.1 or more, thus, the maximum crack depth exceeded 10 μm.
- Steels B-1, C-1, D-1, E-1, and F-1 all have satisfied the hot press forming conditions proposed in the present disclosure, and thus, all have a retained austenite phase fraction of 1% or more, a PAGS of 10 μm or less, and a Mn/Zn content ratio of 0.1 or more, and had no observable microcracks. In addition, these Inventive Examples have achieved excellent ductility as well as ultra-high strength.
- However, Steel G-1 has, not only an insufficient alloy composition, but also, due to a high hot forming temperature, an insufficiently formed retained austenite phase, a coarse PAGS, and a Mn/Zn content ratio of less than 0.1, and thus, an extremely large maximum crack depth of 28.5 μm was observed. In the case of Steel G-2, although the hot forming temperature satisfied the present disclosure, it had a coarse PAGS and a Mn/Zn content ratio of less than 0.1, and thus, the maximum crack depth exceeded 10 μm, and the tensile strength was 631 MPa, thus failing to achieve ultra-high strength.
-
FIG. 2 shows microcracks observed in hot press-formed members of Steel B-1 (Inventive Example 6) and Steel A-6 (Comparative Example 1). - Although in Inventive Example 6, a microcrack penetrating the base iron was hardly observed, however, in Comparative Example 1, a crack penetrating the base iron from the plating layer exceeded 10 μm.
- As shown in Table 3, tempering was performed on produced hot press-formed members, and in Inventive Examples 11 to 26 (A-1-1 to F-1-1), the retained austenite phase was sufficiently formed after the tempering, and thus, ductility was further improved, and yield strength was high.
- However, in Comparative Examples 6 to 9 (G-1-1 to G-1-4), even after the tempering, the retained austenite phase was not sufficiently formed, thus resulting in inferior ductility, and Comparative Example 10 (G-1-5) failed to achieve ultra-high strength.
Claims (11)
1. A hot press-formed member comprising:
a base steel sheet; and
a plating layer comprising Zn or Zn alloy on the base steel sheet,
wherein a Mn(wt %)/Zn(wt %) content ratio measured at a point 1 μm from a surface of the plating layer is 0.1 or more,
wherein a maximum crack depth penetrating the base steel sheet from an interface between the base steel sheet and the plating layer is 10 μm or less.
2. The hot press-formed member of claim 1 ,
wherein a microstructure of the hot press-formed member comprises 1-30 area % of retained austenite.
3. The hot press-formed member of claim 1 ,
wherein the microstructure of the hot press-formed member comprises 1-20 area % of retained austenite.
4. The hot press-formed member of claim 1 ,
wherein the microstructure of the hot press-formed member comprises at least one of martensite and bainite, or at least one of tempered martensite and bainite.
5. The hot press-formed member of claim 1 ,
wherein a prior austenite grain size of the hot press-formed member is 10 μm or less.
6. The hot press-formed member of claim 1 ,
wherein a prior austenite grain size of the hot press-formed member is 7 μm or less.
7. The hot press-formed member of claim 1 ,
wherein a prior austenite grain size of the hot press-formed member is 5 μm or less.
8. The hot press-formed member of claim 1 ,
wherein the hot press-formed member comprises a metal coating comprising Fe or Ni between the base steel sheet and plating layer.
9. The hot press-formed member of claim 1 ,
wherein the Mn(wt %)/Zn(wt %) content ratio is measured in an oxide layer of the plating layer.
10. The hot press-formed member of claim 1 ,
wherein the base steel sheet comprises, by wt %, carbon (C): 0.08-0.30%, silicon (Si): 0.01-2.0%, manganese (Mn): 3.1-8.0%, aluminum (Al): 0.001-0.5%, phosphorus (P): 0.001-0.05%, sulfur (S): 0.0001-0.02%, nitrogen (N): 0.02% or less, and a balance of iron (Fe) and other impurities.
11. The hot press-formed member of claim 1 ,
wherein the base steel sheet further comprises at least one selected from the group consisting of, by wt %,
(1) at least one of chromium (Cr) and molybdenum (Mo), a total content thereof being 0.001-2.0%;
(2) at least one of titanium (Ti), niobium (Nb), and vanadium (V), a total content thereof being 0.001-0.2%;
(3) at least one of copper (Cu) and nickel (Ni), a total content thereof being 0.005-2.0%; and
(4) Boron (B): 0.0001-0.01%.
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KR1020160086248A KR101819345B1 (en) | 2016-07-07 | 2016-07-07 | Hot press formed member having excellent crack arrest property and ductility and method for manufacturing thereof |
PCT/KR2017/007328 WO2018009041A1 (en) | 2016-07-07 | 2017-07-07 | Hot forming member having excellent crack propagation resistance and ductility, and method for producing same |
US201916315767A | 2019-01-07 | 2019-01-07 | |
US18/375,764 US20240026479A1 (en) | 2016-07-07 | 2023-10-02 | Hot press-formed member having excellent crack propagation resistance and ductility, and method for producing same |
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PCT/KR2017/007328 Continuation WO2018009041A1 (en) | 2016-07-07 | 2017-07-07 | Hot forming member having excellent crack propagation resistance and ductility, and method for producing same |
US16/315,767 Continuation US11827947B2 (en) | 2016-07-07 | 2017-07-07 | Hot press-formed member having excellent crack propagation resistance and ductility, and method for producing same |
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DE102019108459B4 (en) * | 2019-04-01 | 2021-02-18 | Salzgitter Flachstahl Gmbh | Process for the production of a steel strip with improved adhesion of metallic hot-dip coatings |
DE102019108457B4 (en) * | 2019-04-01 | 2021-02-04 | Salzgitter Flachstahl Gmbh | Process for the production of a steel strip with improved adhesion of metallic hot-dip coatings |
KR102213974B1 (en) * | 2019-04-30 | 2021-02-08 | 현대제철 주식회사 | Hot stamping component and method of manufacturing the same |
CN110273111B (en) * | 2019-07-30 | 2020-11-24 | 马鞍山钢铁股份有限公司 | Zinc-based coating hot forming steel with wide hot forming heating process window and preparation method thereof |
DE102020204356A1 (en) | 2020-04-03 | 2021-10-07 | Thyssenkrupp Steel Europe Ag | Hardened sheet metal component, produced by hot forming a flat steel product and process for its production |
KR102240850B1 (en) * | 2020-07-10 | 2021-04-16 | 주식회사 포스코 | Manufacturing method of hot fress formed part having excellent productivity, weldability and formability |
KR102308832B1 (en) * | 2020-10-29 | 2021-10-05 | 현대제철 주식회사 | Aluminum coated blank and manufacturing method thereof |
CN113042525B (en) * | 2021-02-24 | 2023-04-07 | 广西柳钢华创科技研发有限公司 | Method for increasing thickness of iron scale on surface of high-speed bar and production method of HRB400E straight threaded steel bar |
CN115305412B (en) * | 2021-05-05 | 2024-02-06 | 通用汽车环球科技运作有限责任公司 | Press hardened steel with combination of excellent corrosion resistance and ultra high strength |
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CA2520814C (en) * | 2003-03-31 | 2009-09-15 | Nippon Steel Corporation | Alloyed molten zinc plated steel sheet and process of production of same |
JP5347393B2 (en) | 2008-09-12 | 2013-11-20 | Jfeスチール株式会社 | Hot press member excellent in ductility, steel plate for hot press member, and method for producing hot press member |
KR101253885B1 (en) | 2010-12-27 | 2013-04-16 | 주식회사 포스코 | Steel sheet fir formed member, formed member having excellent ductility and method for manufacturing the same |
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MX2016015400A (en) * | 2014-05-29 | 2017-02-22 | Nippon Steel & Sumitomo Metal Corp | Heat-treated steel material and method for producing same. |
WO2016063467A1 (en) * | 2014-10-24 | 2016-04-28 | Jfeスチール株式会社 | High-strength hot-pressing member and method for producing same |
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EP3483297A1 (en) | 2019-05-15 |
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ES2917620T3 (en) | 2022-07-11 |
US11827947B2 (en) | 2023-11-28 |
WO2018009041A8 (en) | 2018-04-26 |
CN116837295A (en) | 2023-10-03 |
CN109477191A (en) | 2019-03-15 |
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US20200010915A1 (en) | 2020-01-09 |
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