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  • 7/24/2019 Improvement of Mechanical Properties and Microstructure of 22MnB5 Steel by Hot Stamping and Direct Cooling -

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    Improvement of Mechanical Properties and

    Microstructure of 22MnB5 Steel by

    Hot Stamping and Direct Cooling

    Fernando Aurelio Flandoli* and Sergio Tonini Button*** Centro Universitario da FEI, So Bernardo do Campo SP Brazil 09850-901

    ** Universidade Estadual de Campinas Campinas SP Brazil 13083-970

    [email protected]

    [email protected]

    Abstract: In this work it was studied how hot stamping and direct cooling couldimprove the mechanical properties of stamped parts made with the high strength

    hardenable steel 22MnB5, Hot stamping of a B-pillar sector was first simulated by finite

    element method to define the best conditions like blank geometry and stamping

    temperature. Experimental tests were carried out with four initial temperatures: room (to

    represent cold stamping), 900, 950 and 980oC, in a hydraulic press with tools cooled to

    17oC. Stamped parts were tempered by direct cooling between the tools immediately

    after hot stamping. Samples taken from stamped parts were analyzed by optical

    microscopy and micro-hardness Vickers, and other samples were analyzed by tensile

    tests. Tests results have shown that all hot stamped parts presented mechanical

    properties higher than cold stamped parts, and that the microstructure and the

    mechanical properties were obtained with tests carried out at 950oC.

    Keywords: metal forming, numerical analysis, phase transformation

    1. INTRODUCTION

    Hot stamping presents a wide application in the automotive industry from external

    components that define the body of the vehicle to internal structural components which

    require durability, rigidity and impact resistance that conventional cold stamping cannot

    match without subsequent heat treatment. Many recent researches have been published

    analysing important aspects of this process, like materials and products quality.

    [Yanagida, and Azushima, 2009] state that numerical simulation is still not

    efficient to predict how process variables influence hot stamping because manymetallurgical data and especially tribological parameters are not well established. They

    tested two high strength hardenable steels (SPHC and 22MnB5) and three furnace

    temperatures and concluded that the new tribological test they developed were effective

    to evaluate the friction coefficient in hot stamping.

    [Geiger et al., 2008] present a cup drawing test to evaluate tribological conditions

    within hot stamping and showed that a significant dependency of blank temperature on

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    the friction coefficient could be detected. With increasing sheet temperature, decreasing

    friction values were observed at the interaction contact area.

    [Barcellona and Palmieri, 2009] considering that little knowledge exists on the

    continuous cooling transformations (CCTs) that reproduce the typical work conditions

    of the press quenching process, describe experimental methods they employed to obtain

    the hardness and microstructural changes of pre-strained and thermally treated

    microalloyed boron steel. They investigated strains, transformation temperatures,

    microstructure and micro-hardness of 22MnB5 steel samples under uniaxial tensile tests

    at temperatures between 873 and 1223 K with a constant strain rate of 0.08 s-1

    , and

    concluded that high values of hot deformation during hot stamping, especially at lower

    temperatures, require a strict control of post-cooling to ensure cooling rates that will

    result in stamped parts with good mechanical properties.

    [Bardelcik et al., 2010] present a similar work to investigate the effect of cooling

    rate on the high strain rate behavior of hardened boron steel. In quenching tests

    22MnB5 steel samples were heated to 950 oC and quenched in three different media:water bath at 22

    oC, heated oil bath at 85

    oC, and compressed air at low and high flow

    rates. They concluded that mechanical properties and microstructure are strongly

    dependent on quenching rate, and that ideal conditions can be achieved with the proper

    selection of furnace temperature and quenching rate.

    [Lee et al., 2009] present a numerical model based on finite element method to

    analyze hot pressing considering phase transformation plasticity (TRIP) when stamping

    a high carbon steel. They also present an extensive experimental procedure to validate

    the numerical analysis, and concluded that phase transformation significantly influence

    part strengthening by transforming hard martensitic phase and reducing dimensional

    change by additional plastic deformation during phase transformation.

    Numerical simulation has been applied considering more reliable frictioncoefficients, and material constitutive equations [Naderi et al., 2008], resulting in more

    effective models to represent hot stamping industrial conditions [Tekkaya et al., 2007],

    and [Liu et al., 2009]. New procedures have been proposed to employ induction heating

    of blanks instead of convective heating in continuous furnaces [Kolleck et al., 2009].

    The main objective of this work was to study how hot stamping and direct cooling

    could improve the mechanical properties of a B-pillar sector made of 22MnB5. First,

    hot stamping was simulated by finite element method to define the best process

    conditions like blank geometry and stamping temperature to be applied in the following

    experimental procedure were blanks were hot stamped, and then analysed by optical

    microscopy, tensile tests, and micro-hardness test.

    2. MATERIALS AND METHODS

    2.1. Numerical analysisHot stamping of a B-pillar sector (Figure 1) was simulated with software Deform 6 3D

    based on the finite element method to define the best process conditions, and to evaluate

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    the forming load and variatio

    the parameters used in the mo

    The material simulated

    experimentally, modelled wi

    2008]. The constant frictiontribological conditions within

    Based on the CCT cu

    temperatures were chosen: 90

    (80mm x 120 mm) were auste

    Blanks were modeled w

    considered rigid and modele

    initial and final steps of sim

    the lower die, and completely

    Table I Process and m

    Blank M

    Wi

    46Furnace tempe

    Room temperaHydraulic pres

    Resting time a

    of blank temperature along the process. Tabl

    dels simulated in this work.

    Figure 1 B-pillar sector.

    in all models was the 22MnB5 steel, the s

    h the constitutive equations provided by [Na

    factor model was adopted equal to 0.7 consthe blank-tools interface.

    ves presented by [Naderi et al., 2008] thr

    , 950 and 980oC. For all temperatures rectang

    nitized for five minutes.

    ith elasto-plastic tetrahedral elements and the

    d with 45000 tetrahedral elements. Figure 2

    lation respectively with the blank initially po

    deformed within closed dies.

    aterial parameters used in the numerical simul

    terial: 22MnB5 steel as cold rolled

    dth x length x thickness (mm): 80x124.5x1.9

    13 tetrahedral elementsrature (

    oC): 900, 950 and 980

    ture: 20oC Transfer time to press: 15 s

    s Speed: 8 mm/s Stroke: 25 mm

    ter stamping: 4 s

    I presents

    ame tested

    deri et al.,

    idering the

    e furnace

    ular blanks

    dies were

    shows the

    itioned on

    tion.

    egion X

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    Figure 2 Nu

    2.2 Experimental p

    Some experimental tests wershown in Table II) and the s

    condition cold rolled were e

    were evaluated by optic micro

    Table II Some chara

    2.2.1. Tensile testinBased on ASTM E8 standard

    axes oriented at 0, 45 and 90o

    sheets were anisotropic or not

    isothermally hot tested at two

    Cold tensile tests were c

    mechanical properties of t

    [ArcelorMittal, 2010]. Hot te

    hot stamping temperatures an

    [Naderi et al., 2008].

    2.2.2. Hot stampingStamping tests were carried o

    (Table I). Each blank was

    temperature (900, 950 or 9

    transferred to the stamping to

    Chemical comp

    C Si

    0.24 0.27

    As received con

    Sheet nominal t

    (a)

    Blank

    erical simulation: (a) initial step, (b) final step

    rocedure

    carried out to evaluate the blank material (chaamped products. 22MnB5 steel sheets as rece

    aluated by cold and hot tensile tests. Stampe

    scopy, tensile test and micro-hardness measure

    teristics of the blank material before hot stamp

    of the 22MnB5 sheets as received[ASTM, 2009], samples were machined from

    in respect to the rolling direction to evaluate

    . These samples were cold tested at room temp

    furnace temperatures: 900 and 950oC.

    arried out to evaluate anisotropy and also to c

    e sheets used in this work to those pr

    nsile tests were also carried out to evaluate an

    d to compare the flow stress curves to those

    testsut with the same conditions used in numerical

    eld in a furnace for five minutes at the a

    0oC). Then, the blank was taken off the f

    ling assembled in a hydraulic press (Figure 3-a

    sition (in weight %):

    Mn P (max) S (max) Cr Ti B

    1.14 0.015 0.001 0.17 0.036 0.003

    ition: cold rolled

    ickness: 1.9 mm

    (b)

    Upper

    die

    Lower

    die

    .

    racteristicsived in the

    d products

    ents.

    ing.

    sheets with

    hether the

    rature and

    mpare the

    sented by

    isotropy at

    btained by

    simulation

    stenitizing

    rnace and

    ).

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    The dies were lubricat

    molybdenum grease to facilit

    was measured during the pro

    At least three stamping test

    stamped the part rested duri

    martensite transformation and

    Figure 3. (a) Hot stamping

    2.2.3. Analysis of hSamples were cut off the

    microstructure and micro-har

    Tensile tests were carri

    Samples were machined fro

    were replicated at least twicemodel 810.

    Samples were cut off in a

    2% to observe, with a optical

    obtained after stamping and d

    height) and R3 (lower fillet)

    B-B in Figure 1. These sa

    measurements with hardness t

    Figure 4 Stamp

    (a)

    d before each test with a mixture of mine

    ate the extraction of the stamped product. Sta

    ess with a load cell and a digital data acquisiti

    s were carried out at each furnace tempera

    g four to five seconds within the tools to co

    then extracted to cool to room temperature (Fi

    tooling assembled in a hydraulic press (b) stam

    t stamped productsstamped products to evaluate mechanical

    ness.

    ed out based on ASTM E8 standard [AS

    strips cut off from the region X in Figure 1.

    for each furnace temperature with testing ma

    transversal plane, grinded, polished and etche

    microscope Olympus model BX51M, the mic

    irect cooling near to points R1 (upper fillet), R

    hown in Figure 4 which represents a half of cr

    ples were finally evaluated by Vickers mic

    ester Buehler model 2100 and an indentation lo

    ed part half cross section - regions R1, R2 and

    (b)

    R1

    R2

    R3

    Upperdie

    Lowerdie

    al oil and

    ping load

    on system.

    ture. After

    mplete the

    ure 3-b).

    ed part.

    properties,

    M, 2009].

    hese tests

    hine MTS

    with Nital

    rostructure

    (wall half

    oss section

    o-hardness

    ad of 3 N.

    3.

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    3.

    RESULTS AND DIS

    3.1. Numerical analThe simulations with the re

    irregular shape and edges w

    problem the blank shape had

    Figure 5-b was chosen becaus

    All numerical and exp

    simulations with this modifie

    Figure 5. (a) Misshaped part

    Figure 6 shows the load

    stamping at furnace temperatpresented the highest loads.

    the different temperatures si

    yield stress (Table IV).

    All temperatures present

    was observed that each load v

    shown in Figure 6: the high l

    associated to the first contact

    A first steady state is re

    Then the load is reduced to

    the lower tool. In the third st

    slight increase of the stampi

    stroke when the dies are close

    (a)

    CUSSION

    ysisctangular blank (80x124.5x1.9) formed a pr

    ith a wrong length as seen in Figure 5-a. To

    to be modified and after many trials the shap

    e it formed products with correct shape and dim

    rimental results shown in this work were

    blank.

    tamped with a rectangular blank, (b) modifie

    curves obtained in simulations of cold stampi

    res of 900, 950 and 980

    o

    C. As expected, colot stamping load did not show a significant

    ulated, what can be explained for the small di

    ed curves with the same aspect, and during si

    ariation was related to a specific deformation g

    ad found in the beginning is merely a numeric

    lank-tools and can be neglected in this analysi

    lated to the free bending of the blank by the

    second steady state corresponding to the ben

    age, after the blank edges touch the upper die

    ng load, and finally a rapid increase near to

    d and the part completely formed.

    (b)

    duct with

    solve this

    shown in

    ensions.

    btained in

    blank.

    g, and hot

    stampingariation at

    fference in

    mulation it

    eometry as

    al problem

    .

    upper tool.

    ing inside

    , there is a

    the end of

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    Figure 6 Stamping load x process time numerical results.

    3.2. Experimental results

    3.2.1. Tensile testing of the 22MnB5 sheets as receivedTable III shows the mechanical properties of the as received sheets in the directions

    tested. Yield and ultimate tensile strength obtained at room temperature are similar to

    those indicated by [Saltzgitter, 2005].

    Sample orientationto rolling direction

    Yield strength (0.2%offset) [MPa]

    Ultimate strength[MPa]

    Elongation[%]

    0o 418 13 463 20 333

    45o 424 17 468 16 353

    90o 415 15 462 14 322

    Table III Mechanical properties of 22MnB5 sheets as received cold tensile tests.

    There are no significant differences among the three directions and therefore the

    material is anisotropic so the blank may be cut off in any position of the sheet regardless

    the rolling direction.

    Table IV shows the results of hot tensile tests. The material is anisotropic for both

    furnace temperatures. By increasing temperature the tensile properties decrease

    significantly, what is expected considering that softening mechanisms are most effective

    at higher temperatures. These results are significantly smaller than those obtained by

    [Naderi et al., 2008], maybe because the smaller strain rate used in these tests.

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    Sample orientationto rolling direction

    Furnacetemperature

    [oC]

    Yield strength(0.2% offset)

    [MPa]

    Ultimatestrength [MPa]

    Area reductionat fracture

    [%]

    0o

    900 272 442 856950 232 383 785

    45o

    900 272 452 795

    950 203 352 785

    90o

    900 292 462 766

    950 222 352 less than 754

    Table IV Mechanical properties of 22MnB5 sheets as received hot tensile tests.

    3.2.2. Results of tests with the hot stamped productsTable V presents the mechanical properties obtained in the tensile tests with the samples

    extracted from parts stamped at room temperature, 900, 950 and 980 oC. Cold stamped

    parts present properties higher than the as received sheets (Table III) because of workhardening caused by cold stamping.

    Furnace

    Temperature

    [oC]

    Yield strength

    (0.2% offset)

    [MPa]

    Ultimate strength [MPa]

    Elongation

    at fracture

    [%]

    Cold 436 24 491 16 26.6 5

    900 1156 34 1543 24 6.4 3

    950 1296 28 1700 27 6.1 4

    980 1273 14 1734 31 7.5 5

    Table VI Mechanical properties of stamped products.

    Hot stamped samples presented the highest properties, especially when stamped intests with furnace temperature at 950 or 980 oC that presented similar results,

    significantly higher than those presented by one producer of 22MnB5 steel which shows

    that after quenching a cold rolled sheet (without hot stamping) this steel can reach 1100

    MPa (yield strength) and 1500 MPa (ultimate strength) [ArcelorMittal, 2010].

    Table VII presents the micro-hardness Vickers measured in the regions R1, R2 and

    R3 of the stamped parts. Higher micro-hardness values were found in samples of tests

    with furnace temperature at 950 and 980 oC confirming the best results found for yield

    and ultimate strength of these samples.

    Furnace

    temperature [

    o

    C]

    Region R1 Region R2 Region R3

    900 41430 46827 32928

    950 42135 52948 45537

    980 404 49 549 26 46132

    Table VII Micro-hardness Vickers indentation load 3 N.

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    Each region presented

    depending on local deforma

    [Bardelick et al., 2010] micro

    under 25 oC/s, not enough to

    al., 2008], as observed

    (martensite+bainite). Otherw

    hardness near to 470 HV

    microstructures only formed

    at 950 and 980 oC.

    Furnace temperature

    [oC]

    Re

    900

    950

    Figure 7 Microstructure

    4.

    CONCLUSIONS

    Numerical simulation proved

    to choose the ideal processi

    stress and temperature distrib

    achieve a martensitic microstr

    Experimental results s

    properties higher than cold st

    without bainite colonies) and

    carried out at 950 and 980oC

    the lower energy necessary an

    5. ACKNOWLEDGME

    Authors wish to thank FAPES

    ifferent micro-hardness and microstructures

    tion, and cooling rate during hot stamping.

    -hardness less than 450 HV is obtained with c

    form a microstructure completely martensitic

    in Figure 7 for furnace temperature at

    ise, those authors observed that samples w

    re related to a cooling rate of 45 oC/s and

    y martensite, as resulted in tests with temperat

    gion R1 Region R2 Regi

    of hot stamped and cooled samples Nital 2%

    to be an important tool to design the best blan

    g conditions. With simulation it is possible

    ution and therefore define the best furnace tem

    ucture and consequently the higher mechanical

    ow that all hot stamped parts presented

    amped parts, and that the best microstructure

    the best mechanical properties were obtained

    , being the lower furnace temperature preferre

    d less surface oxidation.

    NT

    P and CNPq for the financial support to this w

    (Figure 7)

    According

    oling rates

    [Naderi et

    900 oC

    ith micro-

    presented

    re furnace

    n R3

    - 500X.

    shape and

    to analyze

    perature to

    properties.

    echanical

    (martensite

    with tests

    regarding

    rk.

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    REFERENCES

    [ArcelorMittal, 2010]ArcelorMittal Flat Carbon Europe S.A., A54 Quenchable boron

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    [ASTM, 2009] ASTM International, ASTM E8 / E8M - 09 Standard Test Methods

    for Tension Testing of Metallic Mateials; DOI: 10.1520/E0008_E0008M-09.

    [Barcellona and Palmieri, 2009] Barcelllona, A. and Palmieri, D., Effect of Plastic

    Hot Deformation on the Hardness and Continuous Cooling Transformations of

    22MnB5 Microalloyed Boron Steel;Metallurgical and Materials Transactions A,

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    [Bardelcik et al., 2010] Bardelcik, A., Salisbury, C.P., Winkler, S., Wells, M.A.,

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    [Kolleck et al., 2009] Kolleck, R., Veit, R., Merklein, M., Lechler, J., Geiger, M.,

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