HIGH-STRENGTH COLD ROLLED SHEET HAVING EXCELLENT FORMABILITY AND CRASHWORTHINESS AND METHOD FOR MANUFACTURING THE SAME

Info

Publication number: 20130133792
Type: Application
Filed: Aug 12, 2010
Publication Date: May 30, 2013
Applicant: JFE STEEL CORPORATION (Tokyo)
Inventors: Tatsuya Nakagaito (Tokyo), Saiji Matsuoka (Tokyo), Shinjiro Kaneko (Tokyo), Yoshiyasu Kawasaki (Tokyo)
Application Number: 13/816,561

Abstract

A high-strength cold rolled steel sheet has excellent formability and crashworthiness and includes, on a mass % basis, C: 0.05 to 0.3%, Si: 0.3 to 2.5%. Mn: 0.5 to 3.5%, P: 0.003 to 0.100%, 5: 0.02% or less, Al: 0.010 to 0.5%, the balance being iron and unavoidable impurities, the high-strength cold rolled steel sheet having a microstructure including 20% or more of ferrite on an area fraction basis, 10 to 60% of tempered martensite on an area fraction basis, 0 to 10% of martensite on an area fraction basis, and 3 to 15% of retained austenite on a volume fraction basis.

Description

Description

RELATED APPLICATIONS

This is a §371 of International Application No. PCT/JP2010/063949, with an international tiling date of Aug. 12, 2010 (WO 2012/020511 A1, published Feb. 16, 2012), the subject matter of which is incorporated herein by reference.

TECHNICAL FIELD

This disclosure relates to a high-strength cold rolled steel sheet having excellent formability for use in structural parts and suspension parts mainly used in the automobile industry field, and to a method for manufacturing the same.

BACKGROUND

In recent years, from the viewpoint of preserving the global environment, improving fuel efficiency of automobiles has become a key issue. There has been a trend toward increasing the strength of automobile body materials to achieve thickness reduction and decrease the weight of car bodies. However, increasing the strength of steel sheets leads to a decrease in ductility, i.e., a decrease in formability and workability. Thus, development of materials that have both high strength and high formability has been anticipated.

To fulfill such a need, various multi-phase cold rolled steel sheets including ferrite-martensite dual phase steel (hereinafter referred to as “DP steel”) and TRIP steel that utilizes the transformation-induced plasticity of retained austenite have been developed.

For example, Japanese Unexamined Patent Application Publication No. 2-101117 discloses a method for manufacturing a high-strength steel sheet having good formability, with which high ductility is achieved by adding large quantities of Si and thereby reliably obtaining retained austenite.

However, although DP steel and TRIP steel have good elongation properties, they have poor stretch flangeability. The stretch flangeability is an indicator of formability during flange-forming through expanding holes already made, and is a property as important as the elongation property required for high-strength steel sheets.

Japanese Unexamined Patent Application Publication No., 2004-256872 discloses a method for manufacturing a cold rolled steel sheet having good stretch flangeability with which the stretch flangeability is improved by forming a ferrite-tempered martensite multi-phase microstructure by conducting quenching and tempering after annealing and soaking. However, according to that technology, although high stretch flangeability is achieved, the elongation is low.

According to existing technologies, cold-rolled steel sheets having good elongation property and stretch flangeability have not been obtained.

It could therefore be helpful to provide a high-strength cold rolled steel sheet having excellent ductility and stretch flangeability and a method for manufacturing the same.

SUMMARY

We discovered that when the steel has alloy elements adequately controlled, intensively cooled to a 150 to 350° C. temperature range during cooling from the soaking temperature in the annealing process and reheated, a microstructure containing 20% or more ferrite and 10 to 60% tempered martensite in terms of area ratio and 3 to 15% retained austenite in terms of volume ratio can be obtained and high ductility and stretch flangeability can be achieved.

Typically, when retained austenite is present, the ductility improves due to a TRIP effect of the retained austenite. However, it is known that martensite generated by transformation of retained austenite under application of strain becomes very hard and as a result exhibits a hardness significantly different from that of the main phase ferrite, thereby degrading the stretch flangeability.

However, according to our composition and microstructure, both high ductility and high stretch flangeability are simultaneously achieved. Although the exact reason why high stretch flangeability is achieved despite the presence of retained austenite is unclear, we believe that co-existence of the retained austenite and tempered martensite reduces the adverse effects of the retained austenite on the stretch flangeability.

We also found that when the average crystal grain diameter of the low-temperature transformation-forming phase constituted by martensite, tempered martensite, and retained austenite is 3 μm or less, this steel sheet microstructure can exhibit high formability and improved crashworthiness.

We thus provide a high-strength cold rolled steel sheet having excellent formability and crashworthiness including, on a mass % basis, C: 0.05 to 0.3%, Si: 0.3 to 2.5%, Mn; 0.5 to 3.5%, P: 0.003 to 0.100%. S: 0.02% or less, Al: 0.010 to 0.5%, and balance being iron and unavoidable impurities, the high-strength cold rolled steel sheet having a microstructure including 20% or more of ferrite on an area fraction basis, 10 to 50% of tempered martensite on an area fraction basis, 0 to 10% of martensite on an area fraction basis, and 3 to 15% of retained austenite on a volume fraction basis.

We also provide a high-strength cold rolled steel sheet having excellent formability and crashworthiness in which a low-temperature transformation-forming phase constituted by the martensite, the tempered martensite, and the retained austenite has an average crystal grain diameter of 3 μm or less.

We further provide a high-strength cold rotted steel sheet having excellent formability and crashworthiness further including, on a mass % basis, at least one element selected from Cr: 0.005 to 2.00%, Mo: 0.005 to 2.00%, V: 0.005 to 2.00%, Ni: 0.005 to 2.00%, and Cu: 0.005 to 2.00%.

We still further provide a high-strength cold rolled steel sheet having excellent formability and crashworthiness, further including, on a mass % basis, one or both of Ti: 0.01 to 0.20% and Nb: 0.01 to 0.20%.

We yet further provide a high-strength cold rolled steel sheet having excellent formability and crashworthiness further including, on a mass % basis, 8: 0.0002 to 0.005%.

We also provide a high-strength cold rolled steel sheet having excellent formability and crashworthiness further including, on a mass % basis, one or both of Ca: 0.001 to 0.005% and REM: 0.001 to 0.005%.

We still further provide a method for manufacturing a high-strength cold roiled steel sheet having excellent formability and crashworthiness, the method including hot-rolling and cold-rolling a slab having a composition described in any one of the first to sixth aspects of the invention to manufacture a cold rolled steel sheet and continuously annealing the cold rolled sheet, in which, during the continuous annealing, the steel sheet is held at a temperature of 750° C. or more for 10 seconds or more, cooled front 750° C. to a temperature in a temperature range of 150 to 350° C. at a cooling rate of 10° C./s or more on average, heated to a temperature of 350 to 600′c, held thereat for 10 to 600 seconds, and cooled to room temperature.

We yet provide a method for manufacturing a high-strength cold rolled steel sheet having excellent formability and crashworthiness in which the average heating rate in the range of 500° C. to Ac₁transformation point is 10° C./is or more.

A high-strength cold rolled steel sheet having excellent formability is thus obtained. We achieve advantageous effects such as realizing both weight reduction and improved crash safety of automobiles and greatly contributing to improving performance of automobile bodies.

DETAILED DESCRIPTION

Our steel sheets and methods will now be described in detail.

1. Regarding Composition

The reasons for limiting the steel composition to those described above are first described. Note that the meaning of % regarding components is mass % unless otherwise noted. C: 0.05 to 0.3%

Carbon (C) is an element that stabilizes austenite and promotes generation of phases other than ferrite. Thus, carbon is needed to increase the steel sheet strength, generate a multiphase structure, and improve the TS-EL balance. At a C content less than 0.05%, it is difficult to reliably obtain phases other than ferrite even when the production conditions are optimized and TS×EL decreases as a result. At a C content exceeding 0.3%, hardening of welded portions and heat-affected zones is significant, and mechanical properties of the welded portions are deteriorated. Thus, the C content is 0.05 to 0.3% and preferably 0.08 to 0.15%. Si: 0.3 to 2.5% 1002$ Silicon(Si) is an element, effective that strengthens the steel. Silicon is also a ferrite-generating element, suppresses C from becoming concentrated and forming carbides in the austenite, and thus accelerates generation of retained austenite. \\Ilea the Si content is less than 0.3%, the effects of addition are low. Thus, the lower limit is 0.3%. Excessive addition deteriorates the surface quality and weldability. Thus, the Si content is 2.5% or less. The Si content is preferably 0.7 to 2.0%.

Mn: 0.5 to 3.5%

Manganese (Mn) is an element effective that strengthens the steel and accelerates generation of low-temperature transformation-forming phase such as tempered martensite. Such an effect is observed at a Mn content of 0.5% or more. However, when the Mn, content exceeds 3.5%, the second phase fraction increases excessively, the ductility deterioration of ferrite due to solid solution strengthening becomes significant and formability is degraded. Accordingly, the Mn content is 0.5 to 3.5% and preferably 1.5 to 3.0%.

P: 0.003 to 0.100%

Phosphorus (P) is an element effective that strengthens the steel and this effect is achieved at a P content of 0.003% or more. When P is contained exceeding 0.100%, brittleness is induced by grain segregation and crashworthiness is deteriorated. Accordingly, the P content is 0.003% to 0.100%.

S: 0.02% or less

Sulfur (S) forms inclusions such as MnS and causes deterioration of crashworthiness and cracking along the metal flow of a welded portion. Thus, the S content is preferably as low as possible, but is limited to 0.02% or less from the production cost point of view.

Al: 0.010 to 0.5%

Aluminum (Al) acts as a deoxidizing agent and is an element effective for cleanliness of the steel. Aluminum is preferably added in the deoxidizing process. When the Al content is less than 0.01%, the effect of addition is little and thus the lower limit is 0.01%. However, addition of large quantities of Al increases the risk of slab cracking during continuous casting and decreases the productivity. Thus, the upper limit of the Al content is 0.5%.

Our high-strength cold rolled steel sheet contains the above-described components as the basic components and the balance is iron and unavoidable impurities. However, the following components can be adequately contained according to the desired properties.

At least one selected from Cr: 0.005 to 2.00%. Mo: 0.005 to 2.00%, V: 0.005 to 2.00%. Ni: 0.005 to 2.00%, Cu: 0.005 to 2.00%

Chromium (Cr), molybdenum (Mo), vanadium (V), nickel (Ni), and copper (Cu) suppress generation of pearlite during cooling from the annealing temperature, promote generation of low-temperature transformation-forming phases, and effectively serve to strengthen the steel. Such effects are obtained when 0.005% or more of at least one of Cr, Mo, V. Ni, and Cu is contained. However, when the content of each of Cr, Mo, V. Ni, and Cu exceeds 2.00%, the effect is saturated and the cost will rise. Thus, the Cr, Mo, V, Ni, and Cu contents are each 0.005 to 2.00%,

One or both of Ti: 0.01 to 0.20% and Nb: OMI to 0.20%

Titanium (Ti) and niobium (Nb) form carbon nitrides and have an effect of strengthening the steel by precipitation. Such effects are observed at a content of 0.01% or more for each element. In contrast, when Ti and Nb are contained in amounts exceeding 0.20%, excessive strengthening occurs and the ductility is decreased. Thus, the Ti and Nb contents are each 0.01 to 0.20%.

B: 0.0002 to 0.005%

Boron (B) suppresses generation of ferrite from austenite grain boundaries and increases strength. Such effects are obtained at a B content of 0.0002% or more. However, the effects saturate when the B content exceeds 0.005% and the cost rises. Accordingly, the B content is 0.0002 to 0.005%.

One or both of Ca: 0.001 to 0.005% and REM; 0.001 to 0.005%

Calcium (Ca) and a rare earth element (REM) improve formability through sulfide morphology control. If needed, one or both of Ca and REM may be contained at an amount of 0.001% or more each. However, since excessive addition may adversely affect the cleanliness, the amount of each element is 0.005% or less.

2. Regarding Microstructure

The microstructure of the steel will now be described.

Area fraction of ferrite: 20% or more

When the area fraction of the ferrite is less than 20%. TS×EL decreases. Thus, the area fraction of ferrite is limited to 20% or more and preferably 50% or more.

Area fraction of tempered martensite: 10 to 60%

Tempered martensite is a ferrite-cementite multiphase having a high dislocation density and obtained by heating martensite to a temperature equal to or lower than Ac₁transformation point and preferably to a temperature lower than Ac₁transformation point. Tempered martensite effectively strengthens the steel. The microstructure obtained by heating martensite to a temperature exceeding Ac₁transformation point is a microstructure that does not contain cementite in ferrite and is fundamentally different from our tempered martensite.

Compared to martensite, the tempered martensite has less adverse effects on stretch flangeability and is a phase effective to reliably obtain the strength without significantly decreasing stretch flangeability. When the area fraction of the tempered martensite is less than 10%, it becomes difficult to reliably obtain the strength. When the area fraction exceeds 60%. TS×EL is decreased. Thus, the area fraction of the martensite is limited to 10 to 60%.

Area fraction of martensite: 0 to 10%

Manensite effectively increases the strength of the steel, but significantly decreases stretch flangeability once the area fraction of the martensite exceeds 10%. Thus, the area fraction of the martensite is 0 to 10%.

Volume fraction of retained austenite: 3 to 15%

Retained austenite not only contributes to strengthening of the steel, but also effectively improves TS×EL of the steel. Such effects are achieved at a volume fraction of 3% or more. When the volume fraction of the retained austenite exceeds 15%, stretch flangeability is decreased. Accordingly, the volume fraction of the retained austenite is 3 to 15%.

Average crystal grain diameter of low-temperature transformation-forming phases constituted by martensite, tempered martensite, and retained austenite: 3 μm or less

Low-temperature transformation-forming phases constituted of martensite, tempered martensite, and retained austenite effectively improve crashworthiness, in particular, finely dispersing the low-temperature transformation-forming phases improves the crashworthiness, and this effect becomes notable when the average crystal grain diameter of the low-temperature transformation-forming phases is 3 μm or less. Accordingly, the average crystal grain diameter of the low-temperature transformation-forming phases is 3 μm or less.

The phases other than ferrite, tempered martensite, martensite and retained austenite may include pearlite and bainite, but such phases do not present a problem as long as the above-described phase structure is satisfied. However, the amount of pearlite is preferably 3% or less from the view point of ductility and stretch flangeability,

3. Manufacturing Conditions

A steel having a composition controlled as described above is melted in a converter or the like and formed into a slab by continuous casting or the like. This steel is hot-rolled, cold-rolled, and continuously annealed. The manufacturing methods regarding casting, hot-rolling, and cold-rolling are not particularly limited, but preferable manufacturing methods are described below.

Casting Conditions

The steel slab is preferably manufactured by continuous casting to prevent macrosegregation of the components, but an ingot casting technique or a thin slab casting technique may be employed. In addition to an existing method of cooling the manufactured steel slab to room temperature and then reheating the slab, an energy-saving process such as hot direct rolling or direct roiling which involves sending the hot slab to a heating furnace without cooling the slab to room temperature or which involves rolling the slab immediately after a short period of heat retention may be employed without any difficulty.

Hot rolling conditions
Slab heating temperature: 1100° C. or more

The slab heaving temperature is preferably low from the viewpoint of energy consumption. At a heating temperature less than 1100T, carbides cannot be sufficiently dissolved or the risks of troubles during hot-rolling increases our to an increased rolling load. The slab heating temperature is preferably 1300° C. or less to prevent the increase in scale loss attributable to oxidation weight gain, the slab heating temperature is preferably 1300° C. or less.

A sheet bar heater that heats the sheet bar may be employed to avoid troubles during hot-rolling despite the decreased slab heating temperature.

Finishing temperature: Ar₃transformation point or more.

When the finishing temperature is less than the Ar₃transformation point, ferrite and austenite are generated during rolling and a band-like microstructure readily occurs in the steel sheet. Such a band-like microstructure remains after cold rolling and annealing, may generate anisotropy in the material properties, and may decrease formability. Accordingly, the finishing temperature is preferably equal to or higher than Ar₃transformation point.

Coiling temperature: 450 to 700° C.

When the coiling temperature is less than 450° C., the control of the coiling temperature is difficult and temperature nonuniformity may occur, thereby causing problems such as deterioration of cold-rolling properties. Problems such as decarburization in the base iron surface layer may occur when the coiling temperature exceeds 700° C. Thus, the coiling temperature is preferably 450 to 700° C.

In our hot-rolling process, to decrease the rolling load during hot rolling, pan or all of the finish rolling may be conducted by lubrication rolling. Lubrication rolling is effective from the viewpoint of uniform steel sheet shape and material homogeneity. Note that the coefficient of friction during lubrication rolling is preferably 0.25 to 0.10. Preferable is a continuous rolling process of joining sheet bars next to each other and continuously finish-rolling the sheet bars. The continuous rolling process is also preferable from the viewpoint of operation stability of hot rolling.

Next, the oxidized scales on the surface of the hot-rolled steel sheet are preferably removed by pickling and the steel sheet is cold-rolled to form a cold-rolled steel sheet having a particular thickness. The pickling conditions and the cold rolling conditions are not particularly limited and typical conditions may be used. The reduction of cold rolling is preferably 40% or more

Average heating rate from 500° C. to Ac₁transformation point: 10° C./s or more

When the average heating rate in the recrystallization temperature zone, 500° C. to Ac₁transformation point is 10° C./s or more, recrystallization during heating is suppressed, austenite generated at Ac₁transformation temperature or higher becomes finer, and the microstructure after annealing and cooling becomes finer. As a result, the average grain diameter of the low temperature transformation-forming phase can be reduced to 3 μm or less.

When the average heating rate is less than 10° C./s, α recrystallization occurs during heating and strain introduced into ferrite is released and thus the sufficient refining of grains cannot be achieved. Thus, the average heating rate front 500° C. to Ac₁transformation point is limited to 10° C./s or more and more preferably 20° C./s or more.

Holding a temperature of 750° C. or more for 10 seconds or more.

When the heating temperature is loss than 750° C. or the holding time is less than 10 seconds, generation of austenite during annealing is insufficient and a sufficient amount of low-temperature transformation-forming phases cannot be reliably obtained after annealing and cooling. Although the upper limits of the holding temperature and the holding time are not particularly defined, the effects saturate and the cost will increase when the holding temperature is 900° C. or more and the holding time is 600 seconds or more, Accordingly, the holding temperature is preferably less than 900° C. and the holding time is preferably less than 600 seconds.

Cooling from 750° C. to a temperature range of 150 to 350° C. at an average cooling rate of 10° C./s or more

When the cooling rate from 750° C. is less than PVC's, pearlite is generated and TS EL and stretch flangeability are degraded. Thus, the cooling rate from 750° C. is limited to 10° C./s or more. The temperature condition of ending the cooling is one of the most crucial conditions of this method. At the time cooling is stopped, part of austenite transforms into martensite and the rest forms untransformed austenite. When reheated, plated and alloyed, and cooled to room temperature, martensite turns into tempered martensite and untransformed austenite transforms into retained austenite or martensite. When the temperature of ending the cooling from annealing is low, the amount of martensite generated during cooling increases and the amount of the untransformed austenite decreases. Thus, controlling the temperature of ending the cooling determines the final area fractions of the martensite, the retained austenite, and the tempered martensite.

When the temperature of ending the cooling is higher than 350° C., martensite transformation at the time cooling is stopped is insufficient and the amount of untransformed austenite is large, thereby ultimately generating excessive amounts of martensite or retained austenite and degrading stretch flangeability. When the temperature of ending the cooling is lower than 150° C., most of austenite transforms into martensite during cooling, the amount of untransformed austenite decreases, and 3% or more of retained austenite is not obtained. Accordingly, the temperature of ending the cooling is 150 to 350° C. As for the cooling method, any cooling method such as gas jet cooling, mist cooling, water cooling, or metal quenching, may be employed as long as the target cooling rate and cooling end temperature are achieved. Heating to 350 to 600° C. and holding thereat for 10 to 600 seconds

When the steel is held at 350 to 600° C. for 10 seconds or more after being cooled to a 150 to 350° C., the martensite generated during cooling is tempered and forms tempered martensite. As a result, stretch flangeability is improved, the untransformed austenite that did not transform into martensite during cooling is stabilized, and 3% or more of retained austenite is obtained at the final stage, thereby improving ductility.

Although the detailed mechanism of stabilization of the untransformed austenite by reheating and holding is not clear, we believe that carbon diffuses from martensite, in which dissolved C is oversaturated, into untransformed austenite, thereby increasing the C concentration in the untransformed austenite and stabilizing the austenite. During this process, if precipitation of cementite in the martensite occurs faster than diffusion of carbon, the concentration of C in the untransformed austenite becomes insufficient. Thus, it is important to delay cementite precipitation and this requires addition of 0.3% or more of Si.

If the reheating temperature is less than 350° C., the martensite is not sufficiently tempered and the austenite is not sufficiently stabilized, thereby degrading stretch flangeability and ductility. If the reheating temperature exceeds 600° C., untransformed austenite at the time cooling is stopped transforms into pearlite and 3% or more of retained austenite cannot be obtained at the final stage. Accordingly, the heating temperature is 350 to 600° C.

If the holding time is less than 10 seconds, the austenite is not sufficiently stabilized. If the holding time exceeds 600 seconds, untransformed austenite at the time the cooling is stopped transforms into bainite and 3% or more of retained austenite cannot be obtained at the final stage. Accordingly, the reheating temperature is 350 to 600° C. and the holding time within that temperature range is 10 to 600 seconds.

The annealed steel sheet may be subjected to temper roiling to correct shape, adjust surface roughness or the like. Moreover, treatment such as resin or oil/fat coating and various other coating may be performed.

Example 1

A steel having the composition shown in Table 1 and balance being Fe and unavoidable impurities was melted in a converter and continuously casted into a slab. The slab was hot-rolled to a thickness of 3.0 mm. The hot rolling conditions were as follows: finishing temperature: 900° C., cooling rate after rolling: 10° C./s, and coiling temperature: 600° C. Then the hot-rolled steel sheet was pickled and cold-rolled to a thickness of 1.2 mm to manufacture a cold roiled steel sheet.

The cold rolled steel sheet was annealed under the conditions described in Table 2 by using a continuous annealing line.

The cross-sectional microstructure, tensile properties, and stretch flangeability of the resulting steel sheet were investigated. The results are shown in Table 3.

TABLE 1 Steel type C Si Mn P S Al N Cr Mo V Ni Cu Ti Nb B Ca Rem (mass %) A 0.10 1.2 2.3 0.020 0.003 0.033 0.003 Example B 0.07 1.7 2.0 0.025 0.003 0.036 0.004 0.30 Example C 0.18 1.0 1.6 0.013 0.005 0.028 0.005 0.4 Example D 0.25 1.5 1.4 0.008 0.006 0.031 0.003 0.05 Example E 0.08 0.5 2.2 0.007 0.003 0.030 0.002 0.2 0.4 Example F 0.12 1.1 1.9 0.007 0.002 0.400 0.001 0.05 Example G 0.14 1.5 2.3 0.014 0.001 0.042 0.003 0.04 Example H 0.10 0.9 1.9 0.021 0.005 0.015 0.004 0.02 0.001 Example I 0.08 1.2 2.5 0.006 0.004 0.026 0.002 0.004 Example J 0.09 2.0 1.8 0.012 0.003 0.028 0.005 0.002 Example K 0.04 1.3 1.8 0.013 0.002 0.022 0.002 Comparative Example L 0.17 0.6 4.0 0.022 0.001 0.036 0.002 Comparative Example M 0.10 1.1 0.3 0.004 0.003 0.029 0.002 Comparative Example Note: Underlined items are outside the range of the present invention.

TABLE 2 Average heating AC1 rate from Average transformation 500° C. Maximum Holding cooling Temperature Reheating Holding time Steel point to Ac₁ temperature time rate after cooling temperature after reheating No. type ° C. ° C./s ° C. Sec ° C./s ° C. ° C. Sec 1 A 721 15 830 60 50 200 400 80 Example 2 A 15 810 60 50 100 420 80 Comparative Example 3 B 740 20 850 90 80 180 430 60 Example 4 B 20 720 60 80 250 430 60 Comparative Example 5 C 734 5 820 90 30 160 450 45 Example 6 C 5 820 5 30 120 450 45 Comparative Example 7 C 5 820 90 30 30 450 45 Comparative Example 8 D 735 30 780 150 70 150 450 60 Example 9 D 30 780 120 3 210 450 60 Comparative Example 10 D 30 780 120 100 380 450 50 Comparative Example 11 E 708 7 850 75 80 180 400 30 Example 12 E 7 850 60 80 200 250 60 Comparative Example 13 E 7 830 75 80 200 650 60 Comparative Example 14 E 7 850 75 80 40 400 30 Comparative Example 15 F 723 15 800 240 90 200 400 90 Example 16 F 15 820 240 90 220 400 0 Comparative Example 17 F 15 800 240 90 240 500 900 Comparative Example 18 G 725 15 850 60 100 200 500 30 Example 19 H 720 15 840 120 90 180 400 30 Example 20 I 718 15 830 75 150 220 500 45 Example 21 J 743 15 800 45 80 180 400 20 Example 22 K 730 15 800 200 100 210 550 10 Comparative Example 23 L 686 15 820 120 150 220 400 60 Comparative Example 24 M 745 15 840 90 150 160 400 20 Comparative Example Note: Underlined items are outside the range of the present invention.

TABLE 3 Absorp- Average grain tion diameter of Hole energy low-temperature expan- up to Tempered Retained transformation- sion 10% Steel Ferrite Martensite martensite austenite forming-phase Other TS EL TS × EL ratio (AE) No. type area % area % area % volume % μm phases MPa % MPa · % % MJ/m AE/TS 1 A 65 0 29 6 2.7 900 26 23400 85 57 0.063 Example 2 A 63 0 35 2 2.8 915 20 18300 92 58 0.063 Comparative Example 3 B 70 0 26 4 2.4 870 26 22620 88 56 0.064 Example 4 B 73 0 8 0 1.9 P 835 21 17535 60 46 0.055 Comparative Example 5 C 55 0 39 6 3.4 990 23 22770 75 57 0.058 Example 6 C 62 0 9 1 2.6 P 935 20 18700 55 49 0.052 Comparative Example 7 C 57 0 42 1 3.5 980 19 18620 92 56 0.057 Comparative Example 8 D 57 0 31 12 1.7 975 26 25350 81 65 0.067 Example 9 D 65 0 25 1 2.1 P 920 20 18400 63 50 0.054 Comparative Example 10 D 58 20 0 14 1.8 B 970 25 24250 32 65 0.067 Comparative Example 11 E 69 5 21 5 3.6 850 26 22100 89 47 0.055 Example 12 E 70 13 15 2 3.6 859 22 18898 74 49 0.057 Comparative Example 13 E 65 0 20 1 3.7 P 823 23 18929 88 40 0.049 Comparative Example 14 E 75 0 24 1 3.5 820 22 18040 105 44 0.054 Comparative Example 15 F 72 0 21 7 2.1 840 27 22680 74 54 0.064 Example 16 F 70 12 17 1 2.0 865 21 18165 62 56 0.065 Comparative Example 17 F 72 0 18 1 2.1 B 796 23 18308 82 50 0.063 Comparative Example 18 G 53 0 37 10 1.8 1015 26 26390 76 72 0.071 Example 19 H 65 0 30 5 2.2 900 25 22500 95 59 0.066 Example 20 I 51 0 42 7 2.8 1068 23 24564 85 68 0.064 Example 21 J 75 0 20 5 2.7 923 24 22152 92 60 0.065 Example 22 K 91 0 8 1 1.8 611 28 17108 73 33 0.054 Comparative Example 23 L 15 0 76 9 2.9 1325 14 18550 75 69 0.052 Comparative Example 24 M 86 0 5 0 2.7 P 562 30 16860 65 31 0.055 Comparative Example Note: Underlined items are outside the range of the present invention. * B represents bainite and P represents pearlite.

The cross-sectional microstructure of the steel sheet was observed by exposing the microstructure by using a 3% nitAl solution (3% nitric acid+ethanol), observing the position ¼ of the thickness in the depth direction by using a scanning electron microscope, and conducting an image processing of a picture of the microstructure taken to determine the fraction of the ferrite phase (the image processing can be performed by using commercially available image processing software). The area fractions of the martensite and tempered martensite were determined by taking SEM photographs of adequate magnification, e.g., about 1000 to 3000 magnification, depending on the fineness of the microstructure and then determining the quantity by using image processing software. The average grain diameter of the low-temperature transformation-forming phase was determined by dividing the area of the low-temperature transformation-forming phases in the observed area by the number of the low-temperature transformation-forming phases, determining the average area therefrom, and raising the average to the power of ½.

The volume ratio of the retained austenite was determined by polishing the steel sheet to a surface ¼ in the thickness direction and measuring X-ray diffraction intensity of the ¼ thickness surface. A MoKa, line was used as the incident X ray, the intensity ratios were determined for all combinations of the integrated intensities of peaks of {111}, {200}, 201, and {311} faces of the retained austenite phase and the {110}, {200}, and {211} faces of the ferrite phase, and the average value was assumed to be the volume fraction of the retained austenite.

The tensile property was determined by using a HS No. 5 specimen sampled from the steel sheet in such a manner that the tensile direction was orthogonal to the roiling direction, conducting a tensile test according to JIS Z2241 to measure TS (tensile strength) and EL (elongation), and determining the strength-elongation balance value represented by the product of the strength and elongation (TS×EL).

The hole expanding ratio was measured as an indicator of stretch flangeability. The hole expanding ratio λ was determined by conducting a hole expanding test according to the Japan Iron and Steel Federation standard JFST1001 and determining the ratio from the initial diameter (10 mmφ) of the hole upon punching and the diameter of hole at the time the crack at the hole edge penetrated the sheet upon hole expanding.

The shock absorption property was determined by using a specimen 5 mm in width and 7 mm in length sampled from the steel sheet in a direction orthogonal to the rolling direction, conducting a tensile test at a strain rate of 2000/s, and integrating the stress-true strain curve obtained by the tensile test within the range of 0 to 10% to calculate the absorption energy (refer to Tetsu-to-Hagane, 83 (1997) p, 748).

The steel sheets of OUT examples have excellent strength, ductility, and stretch flangeability, i.e., TS×EL of 22000 MPa·% or more and λ of 70% or more.

In contrast, the steel sheets of comparative examples outside our range did not achieve excellent strength, ductility, and stretch flangeability unlike the steel sheets of our examples since TS×EL was less than 22000 MPa. % and/or λ was less than 70%. Moreover, when the average grain diameter of the low-temperature transformation-forming phase is 3 μm or less, the ratio of the absorption energy to TS (AE/TS) is 0.063 or more, thereby achieving excellent crashworthiness.

INDUSTRIAL APPLICABILITY

Our steel sheets can contribute to weight reduction and decreasing the fuel consumption of automobiles by providing a high-strength cold rolled steel sheet having excellent formability and crashworthiness.

Claims

1. A high-strength cold rolled steel sheet having excellent formability and crashworthiness comprising, on a mass % basis, C: 0.05 to 0.3%, Si: 0.3 to 2.5%. Mn: 0.5 to 3.5%, P: 0.003 to 0.100%, S: 0.02% or less. Al: 0.010 to 0.5%, and balance being iron and unavoidable impurities, the high-strength cold rolled steel sheet having a microstructure including 20% or more of ferrite on an area fraction basis, 10 to 60% of tempered martensite on an area fraction basis, 0 to 10% of martensite on an area fraction, basis, and 3 to 15% of retained austenite on a volume fraction basis.

2. The high-strength cold rolled steel sheet according to claim 1, wherein a low-temperature transformation-forming phase constituted of the martensite, the tempered martensite, and the retained austenite has an average crystal grain diameter of 3 μm or less.

3. The high-strength cold rolled steel sheet according to claim 1, further comprising, on a mass % basis, at least one element selected from the group consisting of Cr: 0.005 to 2.00%, Mo: 0.005 to 2.00%. V: 0.005 to 2.00%, Ni: 0.005 to 2.00%, and Cu: 0.005 to 2.00%.

4. The high-strength cold roiled steel sheet according to claim 1, further comprising, on a mass % basis, one or both of Ti: 0.01 to 0.20% and Nb: 0.01 to 0.20%.

5. The high-strength cold roiled steel sheet according to claim 1, further comprising, on a mass % basis, B: 0.0002 to 0.005%.

6. The high-strength cold rolled steel sheet according to claim 1, further comprising, on a mass % basis, one or both of Ca: 0.001 to 0.005% and REM: 0.001 to 0.005%.

7. A method of manufacturing a high-strength cold rolled steel sheet having excellent formability and crashworthiness, comprising:

hot-roiling and cold-rolling a slab having a composition described in claim 1 to manufacture a cold rolled steel sheet; and

continuously annealing the cold rolled sheet, wherein, during the continuous annealing, the steel sheet is held at a temperature of 750° C. or more for 10 seconds or more, cooled from 750° C. to a temperature range of 150 to 350° C. at a cooling rate of 10° C./s or more on average, heated to a temperature of 350 to 600° C., held thereat for 10 to 600 seconds, and cooled to room temperature.

8. The method according to claim 7, wherein the average heating rate at 500° C. to Ac1 transformation point is 10° C./s or more.

9. The high-strength cold rolled steel sheet according to claim 2, further comprising, on a mass % basis, at least one element selected from the group consisting of Cr: 0.005 to 2.00%. Mo: 0.005 to 2.00%. V: 0.005 to 2.00%, Ni: 0.005 to 2.00%, and Cu: 0.005 to 2.00%.

10. The high-strength cold roiled steel sheet according to claim 2, further comprising, on a mass % basis, one or both of Ti: 0.01 to 0.20% and Nb: 0.01 to 0.20%.

11. The high-strength cold rolled steel sheet according to claim 3, further comprising, on a mass % basis, one or both of Ti: 0.01 to 0.20% and Nb: 0.01 to 0.20%.

12. The high-strength cold rolled steel sheet according to claim 2, further comprising, on a mass % basis, B: 0.0002 to 0.005%.

13. The high-strength cold rolled steel sheet according to claim 3, further comprising, on a mass % basis, B: 0.0002 to 0.005%.

14. The high-strength cold rolled steel sheet according to claim 4, further comprising, on a mass % basis, B: 0.0002 to 0.005%.

15. The high-strength cold rolled steel sheet according to claim 2, further comprising, on a mass % basis, one or both of Ca: 0.001 to 0.005% and REM: 0.001 to 0.005%.

16. The high-strength cold rolled steel sheet according to claim 3, further comprising, on a mass % basis, one or both of Ca: 0.001 to 0.005% and REM: 0.001 to 0.005%.

17. The high-strength cold rolled steel sheet according to claim 4, further comprising, on a mass % basis, one or both of Ca; 0.001 to 0.005% and REM: 0.001 to 0.005%.

18. The high-strength cold rolled steel sheet according to claim 5, further comprising, on a mass % basis, one or both of Ca: 0.001 to 0.005% and REM: 0.001 to 0.005%.