scholarly journals FEM ANALYSIS OF TEMPERATURE DISTRIBUTION OF A FLAT PLATE MOLD WITH HOLLOWS, HEATED BY DIRECT RESISTANCE HEATING

2017 ◽  
Author(s):  
KAZUTO TANAKA ◽  
SHUN AKAMATSU ◽  
JUN NAKATSUKA ◽  
TSUTAO KATAYAMA
Keyword(s):  
Temperature Distribution ◽  
Flat Plate ◽  
Fem Analysis ◽  
Resistance Heating

scholarly journals FEM Analysis of Temperature Distribution of Flat Mold by Direct Resistance Heating Method

2018 ◽  
Vol 67 (3) ◽  
pp. 367-374
Author(s):  
Kazuto TANAKA ◽  
Jun NAKATSUKA ◽  
Tsutao KATAYAMA ◽  
Hideyuki KUWAHARA
Keyword(s):  
Temperature Distribution ◽  
Fem Analysis ◽  
Resistance Heating ◽  
Heating Method

Embedded resistive heating in composite scarf repairs

2016 ◽  
Vol 51 (18) ◽  
pp. 2575-2583 ◽  
Author(s):  
Mahdi Ashrafi ◽  
Brandon P Smith ◽  
Santosh Devasia ◽  
Mark E Tuttle
Keyword(s):  
Temperature Distribution ◽  
Outer Surface ◽  
Thermal Gradient ◽  
Thermal Damage ◽  
Electrical Current ◽  
Tensile Tests ◽  
Resistance Heating ◽  
Uniform Temperature ◽  
Uniform Temperature Distribution ◽  
Bond Strengths

Composite scarf repairs were cured using heat generated by passing an electrical current through a woven graphite-epoxy prepreg embedded in the bondline. Resistance heating using the embedded prepreg resulted in a more uniform temperature distribution in the bondline while preventing any potential thermal damage to the surface of the scarf repairs. In contrast, conventional surface heating methods such as heat blankets or heat lamps lead to large through thickness thermal gradient that causes non-uniform temperature in the bondline and overheating the outer surface adjacent to the heater. Composite scarf repair specimens were created using the proposed embedded heating approach and through the use of a heat blanket for circular and rectangular scarf configurations. Tensile tests were performed for rectangular scarf specimens, and it was shown that the bond strengths of all specimens were found to be comparable. The proposed embedded curing technique results in bond strengths that equal or exceed those achieved with external heating and avoids overheating the surface of the scarf repairs.

Flow of Liquid Metal Past a Porous Flat Plate

1960 ◽  
Vol 27 (4) ◽  
pp. 749-750
Author(s):  
G. Horvay
Keyword(s):  
Boundary Layer ◽  
Temperature Distribution ◽  
Liquid Metal ◽  
Flat Plate ◽  
Approximation Formula ◽  
Boundary Layer Approximation ◽  
Simple Boundary ◽  
Porous Flat Plate

A simple boundary-layer approximation formula is derived for the temperature distribution in liquid metal which flows past a porous flat plate at zero incidence at velocity U and is sucked into it at velocity V.

scholarly journals Thermal characterization of a plate heated by a multi-jet system

2018 ◽  
Vol 19 (5) ◽  
pp. 503
Author(s):  
Amar Zerrout ◽  
Ali Khelil ◽  
Larbi Loukarfi
Keyword(s):  
Temperature Distribution ◽  
Numerical Analysis ◽  
Flat Plate ◽  
Turbulence Model ◽  
Thermal Characterization ◽  
Experimental Results ◽  
Experimental Device ◽  
Inlet Temperature ◽  
Thermal Transfer

This study is an experimental and numerical analysis of the influence from changes in the conditions of inputs temperature and velocity on the behavior thermal and dynamic of a multi-jet swirling system impacting a flat plate. The experimental device comprising three diffusers arranged in line, of diameter D aloof 2D between the axes of their centers, impinging the plate perpendicularly at an impact height H = 6D. The swirl is obtained by a generator (swirl) of composed 12 fins arranged at 60° relative to the vertical placed just at the exit of the diffuser. By imposing the temperature and velocity for three input conditions with three studied configurations. The paper deals with find the configuration that optimizes the best thermal homogenization. The results show that the configuration having an equilibrated inlet temperature (T, T, T) is derived from a good temperature distribution on the baffle wall and a better thermal transfer from the plate. The system was numerically simulated by the fluent code by using the turbulence model (k–ε). This last has yielded results accorded to those experimental results.

Local Prevention of Hardening for Punching of Hot-Stamped Parts

2015 ◽  
Vol 639 ◽  
pp. 205-212 ◽  
Author(s):  
Kenichiro Mori ◽  
Tomoyoshi Maeno ◽  
Takuya Suganami
Keyword(s):  
Temperature Distribution ◽  
Laser Cutting ◽  
Heating Temperature ◽  
Resistance Heating ◽  
Hardness Distribution ◽  
Delayed Fracture ◽  
Austenitic Transformation ◽  
Sheared Edge ◽  
Heat Transfers

Punching portions of the sheet are sandwiched between the ceramic billets during rapid resistance heating to prevent hardening of these portions. When the heating temperature is locally lower than that of the austenitic transformation, i.e. below 800 oC, this portion is not hardened without occurrence of martensitic transformation, and thus cold punching of hot-stamped parts becomes easy. The ceramic billets are made of alumina and the heat transfers to the billets. The temperature distribution just after resistance heating, the hardness distribution of the hot-stamped sheet, the cold punching load, the quality of the punched hole, etc. were measured. Hardening of punching portions was successfully prevented by sandwiching between the ceramic billets. The cold punching load for the local prevention of hardening was half of that without local prevention and the delayed fracture was also prevented, whereas the drop in hardness around the sheared edge became larger than that for laser cutting.

Significance of Ms and Validation of Reference Stress Solutions for Crack Like Flaws: Part 2

2020 ◽  
Author(s):  
Yoichi Ishizaki ◽  
Greg Thorwald ◽  
Futoshi Yonekawa
Keyword(s):  
Flat Plate ◽  
Correction Factor ◽  
Fem Analysis ◽  
Limit Load ◽  
Metal Loss ◽  
Loss Assessment ◽  
Reference Stress ◽  
Load Analysis ◽  
Similar Factor ◽  
Surface Correction

Abstract This is Part 2 of two papers discussing the significance of two key factors of crack like flaw assessment in the Fitness for Service assessment. While FEM analysis technology has been advancing amazingly in recent years, and FEM based fitness-for-service assessment of a damaged components, such as crack like flaws and local metal loss assessment, has become mainstream in assessments, it is still important to understand the reference stress solution based on a limit load analysis and the role of each factor in the failure mode to control the damaged component safely until the end of its life. In API 579-1/ASME FFS-1[1], Part 9, Assessment of Crack like Flaws, those reference stress solutions were developed based on the limit load analysis using Folias factor Mt and surface correction factor Ms. Folias factor Mt and surface correction factor Ms, are factors that account for the bulging effect around flaws. Those factors enable prediction of a maximum allowable pressure of a damaged cylindrical shell from a simple flat plate model that contain same size of a damaged area. As for Folias factor, Mt, it is well known to express the relationship between the reference stress of a through-wall crack flat plate and a through-wall crack cylinder. The application of Mt is clearly defined in ASME/API 579 FFS-1 part 9C, as well as papers by Folias et al. The the significance of the surface correction factor for surface flaw, Ms, has not been commonly understood well enough in general. Unfortunately, API 579-1/ASME FFS-1 also does not clearly mention its significance and how Ms is to be applied in the stress analysis. At a glance, Ms looks like a similar factor to Mt, and it is tempting to simply apply Ms to primary membrane stress term like Mt, but that is not correct. Eventually, an incorrect application of Ms would lead to an incorrect discussion of a flaw characterization. Often, there is a question about ASME/API 579 FFS-1 Part 9C reference stress solutions, especially for ASME/API 579 FFS-1 eq. 9C.76, from the misunderstanding meaning of the Ms factor. Addressing this issue is important to maintain the integrity of the Fitness-For-Service technology. In this Part 2 of two papers, validation of equations obtained in Part 1 are discussed and proven based on FEM analysis.

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