Development of a tool for the structural design of the vertical load‐bearing capacity of unreinforced masonry

Before the introduction of EC 6, simple codes permitted masonry to be designed manually. The simplified procedure according to EN 1996‐3 still allows manual design, but its application is restricted. Therefore, a more laborious design according to EN 1996‐1‐1 is often required. This article presents a newly developed software tool, which facilitates the structural design of the vertical load‐bearing capacity of unreinforced masonry according to EN 1996‐1‐1. The tool is intuitive to use and has been developed based on experience from working in the field. The tool assists the planner in making decisions during the masonry design process. This article describes and explains the implemented, theoretical assumptions as well as the software tool N_Rd‐Pro‐Tool itself. This software tool facilitates simple, clear und transparent structural design of the vertical load bearing capacity of unreinforced masonry.     

Design of masonry buildings of three‐layered units according to Eurocode 6 / Bemessung von Mauerwerksbauten aus Dreischichtsteinen nach Eurocode 6

In the recent past, the masonry industry has developed many different solutions for optimising the heat protection of buildings. This took place for the building materials, geometric design, but also by development of multiple layered stones in which the components masonry unit, insulation and outer shell have been integrated into a block.     

Arching effect in case of exterior walls with low surcharge under wind action / Ausbildung der Bogentragwirkung bei Außenwänden mit geringer Auflast unter Windbeanspruchung

It is very important to have a minimum surcharge on external masonry walls to help the wall resisting wind actions. The present contribution describes the behaviour of masonry wall under wind action with low surcharge. The behaviour has been investigated using a finite element non‐linear model that considers the large displacement non‐linearity. An increasingly wind load has been applied and the deformation state and the thrust line within the wall have been investigated. The results of the analysis show that the behaviour of the wall under low surcharge was greatly characterized by the arching effect. Due to the low surcharge the influence of the second order effect was very small and can be neglected.     

Confined Masonry subjected to Lateral Loads / Eingefasstes Mauerwerk unter Plattenbeanspruchung

Just as with shear stress on the edges of masonry walls, prestressing through the confinement and restraint of all four sides of the wall improves the load‐carrying capacity under lateral loads. The extra load arising from prestressing leads to increased flexural strength of the masonry. The confinement of the edges results in relatively smaller span moments. In this case, the torsional stiffness of the reinforced concrete frame is important. This is determined by the frame itself as well as by its integration within the building. As a supplement to [4], an examination of panel loading was also performed within the guidelines of a research project at the TU Dresden, Chair for Structural Design, on behalf of the Federal Office for Building and Regional Planning on the subject of “Confined Masonry as an Option for Increasing the Load‐Carrying Capacity of Stiffening Walls”[9]. The various influences are to be initially researched on the basis of various analytical observations and a small numerical study. A thorough, experimentally‐based clarification of the load‐carrying capacity of the panels was not possible within the framework of the research project.     

Characterization of uncertainty (probabilistic models) in verification of unreinforced masonry shear wall / Charakterisierung der Unschärfe (probabilistische Modelle) beim Nachweis von Wandscheiben aus unbewehrtem Mauerwerk

The model uncertainty has significant role in determination of safety factor. Eurocode has been considered partial factor covering uncertainties in the resistance model. Moreover, the model uncertainty has important role in full probabilistic verification. A stochastic analysis may yield to realistic results, only if the uncertainties have been involved in the calculation, properly. The uncertainty in predicted load‐carrying model may be identified by comparing the observed (experimental records) load‐carrying behaviour with the predicted value. Some general recommendations for considering uncertainty in probabilistic verifications are available in literature. In this study, the deviation of predicted values according to DIN EN 1996‐1‐1/NA model of masonry shear wall from test results has been derived. The best‐fitted distribution with associated statistical parameters (type of distribution, mean and coefficient of variation) has been proposed for uncertainty model. The uncertainty models have been compared with recommendations in the literature.     

Design tables for the utilisation factor α6,fi for the structural fire design of masonry according to DIN EN 1996‐1‐2/NA in the simplified calculation method

Easy‐to‐use verification equations are available for the verifications in the simplified calculation method. This applies also for the structural fire design of those masonry types for which a verification with the utilisation factor α_fi is given in the National Annex DIN EN 1996‐1‐2/NA. In specific applications, however, a classification can only be made applying the utilisation factor α_6,fi. In these cases, the verification for the structural fire design by calculation is considerably more complex than the mathematical verification of the structural design in the ”cold state“. The present paper shows how the design equation for α_6,fi can be made significantly easier with regard to its application by reference to the design value of the vertical load bearing resistance in the simplified method. Moreover, an upper limit value for the utilisation factor α_6,fi for the simplified method is summarised in tables.     

Differentiation between the terms ”confined masonry“ and ”infill masonry“

This publication concerns the differentiation between the terms ”confined masonry“ and ”infill masonry“ using the example of the national technical approval Z‐17.1‐1145 – POROTON S9 MW –vertically perforated clay units with integrated thermal insulation using thin layer mortar [1].     

System analysis of Neo‐Gothic vaults / Systemanalyse neugotischer Gewölbe

From the middle of the 19th century until the beginning of World War I, many buildings were built in the Neo‐Gothic style. In this period, Gothic elements were built regarding the former needs to save material. These lightweight and thin vaults are often relatively fragile support systems. They tend to show systemic damages in the form of significant crack patterns in the vault caps and arches. In the research project Preservation of Neo‐Gothic vault structures, typical damages of Neo‐Gothic vaulted structures are analyzed with the objective to find sustainable and rehabilitative measures. In this context, since 2011, numerical and experimental studies have been carried out on a reference structure. Measured values of a 3D laser scanning, including all the imperfections of the structure, provide the basis of the geometry model, created for the finite element simulation. The system behavior was studied experimentally in the non‐critical load range with a load test for the calibration of this numerical model. In this paper, the project framework as well as the implementation and the evaluation of the load test are presented. In further papers, the transfer of the geodetic measurement data to the numerical model and the consideration of the load test results within a realistically finite element simulation will be addressed.     

Schubtragfähigkeit von Wänden aus Kalksand‐Planelementen mit geringem Überbindemaß — Experiment und rechnerische Simulation

Der Querkraftwiderstand V_R von Mauerwerkswänden, die in ihrer Ebene durch Wind‐ oder Erdbebeneinwirkungen beansprucht werden, hängt auch vom Überbindemaß ü bzw. vom Verhältnis des Überbindemaßes zur Steinhöhe ü/h_st ab. Das nach Norm derzeit zulässige Überbindemaß von ü ≥ 0,4 h_st kann bei der Verwendung von Planelementen in der Praxis nicht immer eingehalten werden. Für diese Fälle ist in den allgemeinen bauaufsichtlichen Zulassungen (abZ) des Deutschen Instituts für Bautechnik (DIBt) für Kalksand‐Planelemente im Bereich 0,4 > ü ≥ 0,2 h_st bzw. 12,5 cm bisher ein verminderter zulässiger Rechenwert der charakteristischen Schubfestigkeit f_vk von 60 % des Wertes nach DIN 1053‐100:2007‐09 (ü ≥ 0,4 h_st ) anzuwenden. Diese, auf Ergebnissen alter Versuche mit überholten Prüfanordnungen beruhenden, hohen Tragfähigkeitseinbußen waren im Zuge der Aufnahme von Planelementen in die Bemessungsnormen für Mauerwerk mit neuem Schubbemessungskonzept zu überprüfen. Daher wurden umfangreiche experimentelle und theoretische Untersuchungen an 17,5 cm dicken, 2,50 m hohen Schubwänden aus Kalksand‐Planelementmauerwerk mit Dünnbettmörtel und unvermörtelten Stoßfugen durchgeführt. Ziel war es, den Einfluss geringer Überbindemaße ü/h_st < 0,4 auf die Schubtragfähigkeit dieser Wände, insbesondere bei statisch‐zyklischen Horizontalverformungen in Wandebene, quantitativ zu bestimmen. Als Versuchsparameter wurden die Wandauflast (σ = 0,5/1,0/1,43 N/mm²), das Überbindemaß (ü/h_st = 0,2/0,4) und die Einspannung am Wandkopf und ‐fuß variiert. Die Untersuchungen ergaben im Bereich der normativ bemessungs relevanten geringen Überbindemaße 0,2 ″ ü/h_st ″ 0,4 keine signifikanten Traglasteinbußen. Bei erweiterten theoretischen FE‐Analysen für das baupraktisch übliche Spektrum vorhandener Überbindemaße 0,2 ″ ü/h_st ″ 1,0 von Wänden mit Auflastspannungen von 0,5 N/mm² bzw. 1,0 N/mm² wurde eine Traglastminderung von maximal 12 bis 16 % berechnet. Der Abtrag der Horizontallast vom Wandkopf zum Wandfuß erfolgt über ein schräges Druckspannungsfeld. Im Überbindebereich der Elemente auftretende Spannungskonzentrationen können zu örtlich begrenzten Rissbildungen führen, ohne dass die Tragfähigkeit der Wand hierdurch beeinträchtigt wird. Diese ist erst dann erschöpft, wenn insbesondere am Wandfuß die vom gerissenen Mauerwerk übertragbaren, schrägen Druckspannungen nicht mehr aufgenommen werden können. Shear load bearing capacity of masonry walls made of calcium silicate element units with a low overlap length — Experimental and numerical simulation analysis. The shear force resistance capacity V_R of masonry walls subjected, in their plane, to loads from winds or earthquakes, amongst other things, depends on the overlap length of the units ü or on the ratio of the overlap length and the height of the unit ü/h_st . The currently permissible overlap length, according to German design standards and norms, of ü ≥ 0.4 h_st can not always be adhered to in building practice, when using element units. In such cases and according to general technical approval code (abZ) of the German Institute for Building Technology (DIBt) for calcium silicate element units within the range 0.4 > ü ≥ 0.2 h_st or 12.5 cm, a reduced permissible calculation value of the characteristic shear strength f_vk of 60 % of the value according to DIN 1053‐100:2007‐09 (ü ≥ 0.4 h_st ) has been used to date. This high loss of load bearing capacity, based on results of older experiments with ob solete test setups, was to be tested in the course of the inclusion of element units in the calculation standards for masonry walls, with a new shear calculation concept. As a result, extensive experimental and theoretical tests were carried out on 17.5 cm thick and 2.50 m high shear walls made of masonry calcium silicate element units and ungrouted butt joints. The objective was to quantatively determine the influence of low overlap length ü/h_st < 0.4 on the shear resistance of these masonry walls and in particular with static‐cyclical horizontal displacement at the wall top. The vertical load pressure (σ = 0.5/1.0/1.43 N/mm²), the overlap length (ü/h_st = 0.2/0.4) and the fixing at the top and bottom of the wall were varied and used as experimental parameters. Within the range of normative calculation with low overlap lengths 0.2 ″ ü/h_st ″ 0.4, the investigations showed no significant load bearing capacity loss. With more extensive theoretical Finite Element analyses for the normal building practice spectrum of overlap lengths 0.2 ″ ü/h_st ″ 1.0 for walls with a vertical load of 0.5 N/mm² or 1.0 N/mm², a reduction of load bearing capacity of maximum 12 % to 16 % was calculated. The transmission of the horizontal shear load from the top of the wall to the bottom of the wall takes place through a diagonal compression stress field. Cracks may occur in the overlap area of the element units as a result of stress concentration, which are limited to the overlap area and do not cause any impairment to the load bearing capacity of the wall. This capacity is only then exhausted when the trans missible, diagonal compression stress can no longer be absorbed, especially at the bottom of the wall with cracked masonry.     

Lebensdauervorhersage auf Basis von Finite Elemente Ergebnissen

Fatigue Life Prediction Based on Finite Element Results The ever‐increasing pressure of competition leads to continuously decreasing product development cycle times. Therefore, information about the life time and the dimensioning of machine parts is required already in the early stages of development. Frequently, a weight optimization is desired, which implies that the local stress must come as close as possible to the strength limit for wide regions of the component under concern. This leads to an increasing use of simulation methods in design as well as in testing. For a life time prediction based on stress results from finite element computations, local S/N curves are needed, which frequently have to be deduced from S/N curves obtained from laboratory specimens. In the present contribution, the transferability from specimen S/N curves to component S/N curves is pointed out exemplarily by taking into account the influences of notches, component size, and microstructure of cast aluminum. Based on such S/N curves, which are computed for each material point in the component, the life time may be calculated by taking into account the local stresses and stress gradients obtained from finite element simulations.